STEAM REFORMING OF CARBO-METALLIC OILS

Abstract: Process for economically converting carbo-metallic oils to liquid fuel products by bringing a converter feed containing 650<o>F+ material characterized by a carbon residue on pyrolysis of at least about (1) and by containing at least about 4 ppm of Nickel Equivalents of heavy metals, including nickel, into contact with a particulate cracking catalyst in a progressive flow type reactor (2) having an elongated conversion zone. The suspension of catalyst and feed in the reactor has a vapor residence time in the range of about 0.5 to about 10 seconds, a temperature of about 900<o>F to about 1400<o>F and a pressure of about 10 to about 50 pounds per square inch absolute for causing a conversion per pass in the range of about 50 to about 90 percent while depositing nickel on the catalyst and coke on the catalyst in amounts in the range of about 0.3 to about 3 percent by weight. The coke-laden catalyst is separated from the resulting stream of hydrocarbons and regenerated by combustion of the coke with oxygen, the regenerated catalyst being characterized by deposited nickel in at least a partially oxidized state and a level of carbon on catalyst of about 0.25 percent by weight or less. The regenerated catalyst is contacted with a reducing gas under reducing conditions sufficient to reduce at least a portion of the oxidized nickel deposits to a reduced state and the regenerated catalyst with reduced nickel deposits is recycled to the conversion zone for contact with fresh feed. Water is also introduced into the reactor conversion zone and the amount of water and the amount of reduced nickel on the recycled catalyst are sufficient to provide a steam reforming reaction so that hydrogen deficient components of the feed are converted to products having higher hydrogen to carbon ratios and the amount of feed converted to coke is reduced. The amount of deposited nickel on catalyst is preferably in the range from about 2,000 to about 20,000 ppm and the mole ratio of water relative to feed in the conversion zone is preferably in the range from about 2 to about 14.

Description: STEAM REFORMING OF CARBO-METALLIC OILS * Technical Field This invention relates to processes for converting heavy ■ * hydrocarbon oils into lighter fractions, and especially to processes for converting heavy hydrocarbons contain¬ ing high concentrations of coke precursors and heavy metals into gasoline and other liquid hydrocarbon f els, Background Art In general, gasoline and other liquid hydrocarbon fuels boil in the range of about 100 to about 650°F. However, the crude oil from which these fuels are made contains a diverse mixture of hydrocarbons and other compounds which vary widely in molecular weight and therefore boil over a wide range. For example, crude oils are known in which 30 to 60% or more of the total volume of oil is composed of compounds boiling at temperatures above 650°F. Among these are crudes in which about 10% to about 30% or more of the total volume consists of compounds so heavy in molecular weight that they boil above 1025°F or at least will not boil ' below 1025°F at atmospheric pressure. Because these relatively abundant high boiling components of crude oil are unsuitable for inclusion in gasoline and other liquid hydrocarbon f els, the petroleum refining industry has developed processes for cracking or breaking i the molecules of the high molecular weight, high boiling compounds into smaller molecules which do boil over an j . appropriate boiling range. The crac3-:ing process which is most widely used for this Durυose is known as fluid cata- lytic cracking (FCC) - Although the FCC process has reached a highly advanced state, and many modified forms and vari- actions have been developed, their unifying factor is that a vaporized hydrocarbon feedstock is caused to crack at an elevated temperature in contact with a cracking catalyst that is suspended in the feedstock vapors. Upon attainment of the desired degree of molecular weight and boiling point reduction the catalyst is separated from the desired products, Crude oil in the natural state contains a variety of ma¬ terials which tend to have quite troublesome effects on FCC processes, and only a portion of these troublesome materials can be economically removed from the crude oil. Among these troublesome materials are coke precursors {such as asphaltenes, polynuclear aromatics, etc.), heavy metals (such as nickel, vanadium, iron, copper, etc.) , lighter metals (such as sodium, potassium, etc.), sulfur, nitrogen and others. Certain of these, such as the lighter metals, can be economically removed by desalting opera¬ tions, which are part of the normal procedure for pretreat- ing crude oil for fluid catalytic cracking. Other materials, such as coke precursors, asphaltenes and the like, tend to break down into coke during the cracking operation, which coke deposits oh the catalyst, impairing contact between the hydrocarbon feedstock and the catalyst, and generally reducing its potency or activity level- The heavy metals transfer almost quantitatively from the feedstock to the catalyst surface. If the catalyst is reused again and again for processing additional feedstock, which is usually the case, the heavy metals can accumulate on the catalyst to the point that they unfavorably alter the con-position of the catalyst and/or the nature of its effect upon the feeds-cock. For example, vanadium tends to form fluxes with certain com¬ ponents of commonly used FCC catalysts, lowering the elt- ing point of portions of the catalyst particles sufficiently so that they begin to sinter and become ineffective crack- ing catalysts. Accumulations of vanadium and other heavy metals, especially nickel, also "poison" the catalyst. They tend in varying degrees to promote excessive dehydro- genation and aromatic condensation, resulting in excessive production of carbon and gases with consequent impairment ■ of liquid fuel yield. An oil such as a crude or crude fraction or other oil that is particularly abundant in nickel and/or othe _-metals exhibiting siπilar behavior, while containing relatively large quantities of coke pre¬ cursors, is referred to herein as a carbo-metallic oil, and represents a particular challenge to the petroleum refiner. In general, the coke-forming tendency or coke precursor content of an oil can be ascertained by determining the weight percent of carbon ramaining after a sample of that oil has been pyrolyzed. The industry accepts this value as a measure of the extent to which a given oil tends to form non-catalytic coke when employed as feed¬ stock in a catalytic cracker. Two established tests are recognized, the Conradson Carbon and Ramsbottom Carbon tests, the former being described in ASTM D189-76 and the latter being described in ASTM Test No. D524-76. In conventional FCC practice, Conradson carbon values on the order of about 0.05 to about 1.0 are regarded as * indicative of acceptable feed. The present invention is concerned with the use of hydrocarbon feedstocks which *• have higher Conradson carbon values and thus exhibit substantially greater potential for coke formation than the usual feeds. Since the various heavy metals are not of equal catalyst poisoning activity, it is convenient to express the poi¬ soning activity of an oil containing a given poisoning OMP metal or metals in terms of the amount of a single metal which is estimated to have equivalent poisoning activity. Thus, the heavy metals content of an oil can be expressed by the following formula (patterned after that of . L. Nelson in Oil -and Gas Journal, page 143, October 23, 1961) in which the content of each metal present is expressed in parts per million of such metal, as metal, on a weight basis, based on the weight of feed: Nickel Eq^uivalents = Ni + —4.8r + 7.-1-, ÷ *1-π.2*3τ - According to conventional FCC practice, the heavy metal content of feedstock for FCC- rocessing is controlled at a relatively low level, e.g., about 0.25 ppm Nickel Equiv¬ alents or less. The present invention is concerned with the processing of feedstocks containing metals substan¬ tially in excess of this value and which therefore have a significantly greater potential for accumulating on and poisoning catalyst. The above formula can also be employed as a measure of the accumulation of heavy metals on cracking catalyst, except that the quantity of metal employed in the formula is based on the weight of catalyst (moisture free basis) instead of the weight of feed. In conventional FCC prac¬ tice, in which a circulating inventory of catalyst is used again and again in the processing of fresh feed, with periodic or continuing minor addition and withdrawal of fresh and spent catalyst, the metal content of the cata¬ lyst is maintained at a level which may for example be in the range of about 200 to about 600 ppm Nickel Equiva¬ lents. The process of the present invention is concerned with the use of catalyst having a substantially larger metals content, and which therefore has a much greater than normal tendency to promote ehydrogenatio , aromatic condensation, gas production or coke formation. There- fore, such higher metals accumulation is normally regarded as quite undesirable in FCC processing. There has been a long standing interest in the conversion of carbo-metallic oils into gasoline and other liquid fuels. For example, in the 1950s it was suggested that a variety of carbo-metallic oils could be successfully converted to gasoline and other products in the Houdresid process. Turning, from the FCC mode of operation, the Houdresid process employed catalyst particles of "granu¬ lar size" (much larger than conventional FCC catalyst particle size) in a compact gravitating bed, rather than suspending catalyst particles in feed and produce vapors in a fluidized bed. Although the Houdresid process obviously represented a step forward in dealing with the effects of metal con¬ tamination and coke formation on catalyst performance, its productivity was limited. Because its operation was uneconomical, the first Houdresid unit is no longer oper¬ ating. Thus, for the 25 years which have passed ' since the Houdresid process was first introduced commercially, the art has continued its arduous search for suitable modi¬ fications or alternatives to the FCC process which would permit commercially successful operation on reduced crude and the like. During this period a number of proposals have been made; some have been used commercially to a certain extent. Several proposals involve treating the heavy oil feed to remove the metal therefrom prior to cracking, such as by hydrotreating, solvent extraction and complexing with Friedel-Crafts catalysts, but these techniques have been criticized as unjustified economically. Another proposal employs a combination cracking process- having "dirty oil" and "clean oil" units. Still another proposal blends OM - 6 - residual oil with gas oil and controls the quantity of residual oil in the mixture in relation to the equilibrium flash vaporization temperature at the bottom of the riser type cracker unit employed in the process. Still another proposal subje-cts the feed to a mild preliminary hydro- cracking or hydrotreating operation before it is intro¬ duced into the cracking unit. It has also been sug¬ gested to contact a carbo-metallic oil such as reduced crude with hot taconite pellets to produce gasoline. This is a small sampling of the many proposals which have appeared in the patent literature and technical papers. Notwithstanding the great effort which has been expended and the fact that each of these proposals overcomes some of the difficulties involved, conventional FCC practice today bears mute testimony to the dearth of carbo-metal¬ lic oil-cracking techniques that are both economical and highly practical in terms of technical feasibility. Some crude oils are relatively free of coke precursors or heavy metals or both, and the troublesome components of crude oil are for the most part concentrated in the highest boiling fractions. Accordingly, it has been possible to largely avoid, the problems of coke precur¬ sors and heavy metals by sacrificing the liquid fuel yield which would be potentially available from the high¬ est boiling fractions. More particularly, conventional FCC practice has employed as feedstock that a fraction of crude oil which boils at about 650°F to about 1,000°F, such fractions being relatively free of coke precursors and heavy metal contamination. Such feedstock, known as "vacuum gas oil" (VGO) is generally prepared from crude oil by distilling off the fractions boiling below about 650°F at atmospheric pressure and then separating by further vacuum distillation from the heavier fractions a cut boiling between about 650°F and about 900° to 1025°F. The vacuum gas oil is used as feedstock for convention¬ al FCC processing. The heavier fractions are normally employed for a variety of other purposes, such as for instance production of asphalt, residual fuel oil, #6 fuel oil, or marine Bunker C fuel oil, which represents a great waste of the potential value of this portion of the crude oil, especially in light of the great ef¬ fort and expense which the art has been willing to ex¬ pend in the attempt to produce generally similar ma¬ terials from coal and shale oils. The present invention is aimed at the simultaneous cracking of these heavier fractions containing substantial quantities of both coke precursors and heavy metals, and possibly other trouble¬ some components, in conjunction with the lighter oils, thereby increasing the overall yield of gasoline and other hydrocarbon liquid fuels from a given quantity of crude. As indicated above, the present invention by no means constitutes the first attempt to develop such a process, but the long standing recognition of the desir¬ ability of cracking carbo-metallic feedstocks, along with the slow progress of the industry toward doing so, show the continuing need for such a process. It is believed that the present process is uniquely advantageous for dealing with the problem of treating such carbo-metallic oils in an economically and technically sound manner. One method of cracking these high boiling fractions, name Reduced Crude Conversion (RCC) after a particularly common and useful carbo-metallic feed, is disclosed in copending applications Serial No. 94,092 and Serial No. 94,216, each filed November 14, 1979, for "Carbo-Metallic Oil Conversion" and each being incorporated herein by ref¬ erence. The oils disclosed as capable of being cracked by the methods of these applications are carbo-metallic oils of which at least about 70 percent boils above 650°F and which contain a carbon residue on pyrolysis of at least about 1 and at least about 4 parts per million of nickel equivalents of heavy metals. Examples of these oils are crude oils, topped crudes, reduced crudes, residua, and extracts from -solvent deasphalting. The cracking reaction for the method disclosed in appli¬ cation Serial No. 94,216 is sufficiently severe to convert 50% or more of the feedstock to gasoline per pass and produce coke in the amount of 6 to 14% by weight based on weight of fresh feed. In a typical RCC cracking process the ratio of weight of catalyst to weight of feedstock is from about 3 to about 18, coke is laid down on the cata¬ lyst in amounts in the range of about 0.3 to about 3 per¬ cent by weight based on the weight of the catalyst, and heavy metals accumulate on the catalyst to a concentration of from about 3000 to about 30,000 ppm nickel equivalents. OM For purposes of this application, the term "heavy metals" re fers to nickel, vanadium, copper and iron, although trace amounts of other heavy metal elements may sometimes be pres¬ ent. The total amount of heavy metals in a carbo-metallic o feed is usually comprised principally of nickel and vanadium (more than SO weight percent based on weight of total heavy metals) . Although the feed may contain principally either nickel or vanadium, vanadium is often present relative to nickel at weight_ , ratios of 1.0 or greater. During the crack ing process, the h-=_avy metal inventory of the feed transfers " almost quantitatively from the feedstock oil to the catalyst particles. Although the heavy metals initially tend to de¬ posit near the surface of a porous catalyst matrix, signifi¬ cant proportions of these metals migrate to the interior of the catalyst matrix where they can deposit on zeolite or oth catalytic promoters carried within the matrix. Heavy metal deposits on the catalyst,particularly nickel, hav in the past catalyzed undesirable dehydrogenation reactions which increased coke production and decreased the selectivity of the catalyst for gasoline production. Although these de- hydrogenation reactions produce hydrogen gas in the exiting product stream, it appears that this hydrogen does not signi¬ ficantly increase within the riser the hydrogen to carbon ratio of the hydrogen deficient hydrocarbons in the feed. Similarly, steam introduced to the riser in the past has not resulted in significant reforming of the hydrocarbons in eith the feed or the cracked product. In fact, the prior art sug¬ gests to the contrary that significant steam reforming reac¬ tions require high pressures (mere than 100 psia) , low temp¬ eratures (less than 900°F) , low coke depositions (less than 1 Conradson carbon) , and long contact times between the reactio mixture and a catalyst (more than 10 second) . The unusually large amount of coke which deposits on the catalyst in carbo-metallic oil processing presents criti¬ cal problems, one problem arising from the fact that the reactions . in the regenerator which convert coke to water, carbon monoxide and carbon dioxide are highly exothermic. using a carbo-metallic feed with its un¬ usually high content of coke precursors as compared to FCC feeds, can increase the amount of coke burned in the regenerator and the temperature in the regenerator to the point that regeneration temperatures become excessive if there is thorough burning of coke. Excessive temperatures can permanently deactivate the catalyst and/or damage the regenerating equipment. The heat of combustion of coke depends upon the concen¬ tration of hydrogen in the coke and the ratio of CO- to CO in the products of combustion. Carbon produces 13,910 BTTJ per pound when burned to CO- and only 3,962 BTU per pound when burned to CO. Hydrogen produces 61,485 BTU per pound when burned to H_0. The heats of combustion of coke for three representative levels of hydrogen and four different ratios of C0 2 /CD are given in the following table: TABLE I Heat of Combustion BTU/lb Coke Percent Hvdroσen C0 2 /CO Ratio 0.5 8,362 9,472 10,582 1.0 11,038 12,083 3.0 14,446 4.0 12,912 14,894 These problems encountered in regenerating catalysts coated with a high concentration of coke may be exacerbated v.hen catalysts of the zeolite or molecular sieve type are used. These catalysts are crystalline aluminosilicates made up of tetra-coordinated aluminum atoms associated through oxygen atoms with silicon atoms in the crystal¬ line structure ' . They have been shown to be more adversely affected by coke in respect to loss of cracking activity, than are certain other catalysts, such as for example, the non-zeolite, ..silica-alumina catalysts. U.S. Patent Applications Serial Nos. 94,094 and 94,227, filed November 14, 1979, disclose processes for the con¬ version of carbo-metallic oils to liquid fuel in which various regeneration techniques are employed that assist in controlling the heat load in the regeneration step, each of said applications being incorporated herein by reference. One method of controlling the heat load in the regenerator is disclosed in U.S. Patent Application Serial No. 251,032- or "Addition of Water to Regenerator Air" filed April 3, 1981, by George D. Myers, et al., and the disclosure of this application is herein incorporated by reference. It is thought that the ratio of CO- to CO may be decreased to no more than about 4 and preferably to less than about 3 in order to reduce the amount of energy released within the regenerator, while optionally providing a flue gas high enough in CO content to be a useful fuel. The CO/CO- ratio may be increased by providing chlorine in an oxidiz¬ ing atmosphere within the regenerator the concentration of chlorine preferably being in the range of about 100 to about 400 ppm- This method of increasing the CO/CO,, ratio is disclosed in copending applications Serial No. 247,751 filed March 23, 1981, for "Addition of gCl 2 to Catalyst" and Serial No. 246,732 filed March 23, 1981, for "Addition of Chlorine to Regenerator", both in the name of George D. _ «.. OMM Myers. The contents of these applications are herein incor¬ porated by reference. As will be appreciated the carbo-metallic oils can vary widely in their Conradson carbon content. Such varying content of carbon residue in the feedstock, along with variations in riser operating conditions such as catalyst to oil ratio and others, can result in wide variations of the percent coke found .on the spent catalyst. Accordingly, where the feed and riser operating conditions are such as to produce rather large coke yields, necessitating the burning of very substantial amounts of coke from the catalyst in regeneration, such as at least about 0.5 weight percent based on the catalyst, or more,chlorine additives may prove useful in controlling the heat load in the regenerator. OMP Summary of the Invention One object of the present invention is to provide a catalytic cracking method for converting carbo-metallic oils to liquid fuels wherein- a steam reforming reaction is provided within the conversion zone to reduce the amount of coke deposited on the catalyst and increase the amount of hydrogen available in the product vapors. Another object of the invention is to provide a catalytic crack¬ ing process involving contacting in a progressive flow reactor a carbo-metallic oil feed and a conversion catalyst in the presence of a sufficient amount of reduced nickel on the cata¬ lyst and a sufficient amount of water relative to the amountof f and catalyst to provide a steam reforming reaction generating significant amounts of labile hydrogen in the conversion zone of the reactor- Still another object of the invention is to provide a carbo- metallic oil conversion process wherein high ratios of water to carbo-metalli oil feed are provided in the conversion zone and high levels of reduced nickel are provided on the conver¬ sion- catalyst so as to decrease coke yield and increase gaso¬ line yield. A further object of the invention is to provide a carbo-metal¬ lic oil conversion process which includes provision for reduc¬ ing nickel deposited on the conversion catalyst from the oxide form provided by the regenerator to a reduced form prior to contact between the conversion catalyst and the carbc-metallic oil feed, and thereby provide increased volume percent yields of both gasoline boiling range products and liquid fuels boil¬ ing above the gasoline range. A still further object of the invention is to provide a carbo- metallic oil conversion process which includes provisions for reducing oxidized heavy metals on the conversion catalyst passing from the regeneration zone to the conversion zone and for introducing water into the conversion zone so as to cause steam reforming in the presence of a carbo-metallic oil feed and a conversion catalyst having substantially more than 600 ppm nickel deposited thereon. In accordance with the invention, nickel deposited on the cata lyst during the conversion reaction is reduced from the oxide state formed in th°_-regenerator and the catalyst with deposite nickel in a reduced state is contacted with an oil feed in the presence of water at relatively high weight ratios of water to feed. This process decreases the amount of coke accumulating on the cracking catalyst and increases the selective cracking provided by the catalyst in the presence of high nickel accumu lations. While not intending to be bound by any one theory or hypothesis for the improvements realized, it is believed that reduced nickel on a conversion catalyst in the presence of an oxygen deficient feed and relatively high mole ratios of water to feed results in a steam reforming reaction in which hydro¬ carbon molecules react with water to form carbon monoxide and labile hydrogen- The resulting carbon monoxide may also react with water through the water—gas shift reaction to form carbon dioxide and further hydrogen- These reactions may be illus¬ trated by the following equations based on an n—heptane feed: (1) n-C 6 H s ÷ 7Ξ 2 0 -^ 7CO ÷ 15K 2 (2) CO + H 2 0 -^ H 2 + C0 2 Although metal dehydrogenation and coking reactions may involv many different mechanisms, one dehydrogenaticn/cokin mechanis may be illustrated by the following equation in which "CH" rep¬ resents coke and H x" represents the hydrogen to carbon ratio i the coke, the actual values for "x" usually being in the range from about 0.5 to about 1-2, preferably about 0.7 to 1.0: ( 3 ) 2 -C 7 H 16 — ■ > 1 CH X ÷ C16 - 7x)H - 15 - According to the invention, this coke may then be consumed by a steam reforming reaction which may be illustrated by the fo lowing equation: (4) 2CH + 2H-0 2CO + (.2 + x)H ∑ As illustrated by the foregoing equations, this invention pro vides a process for generating labile hydrogen in the riser s as to reduce the conversion " of hydrogen deficient carbo-metal oils to coke. Simultaneously, the labile hydrogen generated helps convert these heavy carbonaceous materials to useful pr ducts having increased hydrogen to carbon ratios. The invent contemplates using an equilibrium cracking catalyst having le els of deposited nickel greater than 2000 ppm, preferably gre than 3000 ppm, more preferably greater than 6000 ppm, and mos preferably in the range of 7000 to 20,000 ppm, to crack and re form carbo-metallic oil feeds in the presence of steam at wei ratios of water to feed up to 1.0, preferably up to 0.5, more preferably up to 0.3, and most preferably in the range of 0.2 0.3. Based on an average hydrocarbon molecular weight of abo 275 in the feed, these weight ratios correspond to the follow ing respective ratios of water partial pressure to feed parti pressure in the riser: up to 14:1, preferably up to 7:1, more preferably up to 4:1, and most preferably in the range of abo 3:1 to 4:1. The water may be introduced into the riser eithe directly or with the feed and as either liquid water or steam. The water contacts the nickel containing catalyst and the fee under conversion conditions such that the steam is reformed i the riser to provide the labile hydrogen and the feed is con¬ verted in the presence of this labile hydrogen to provide in¬ creased yields of gasoline and other liquid fuel products. In prior art conversion processes, nickel accumulating on the catalyst is placed in an oxidized state in the regenerator and is still in that state when it is introduced -into the riser from the regenerated catalyst stanάpipe. It has been found that in this oxidized state, little if any steam reforming wil take place in the riser, even at catalyst residence times in excess of 10 seconds. The resent invention contemola es treating the catalyst from the regenerator with a reducing gas so that the nickel on the catalyst is in a reduced state at the time the catalyst is brought into contact with the feed and/or water. Treatment of regenerated catalyst with reduc¬ ing gas may take place either in an upstream portion of the riser before significant amounts of feed and/or water are in¬ troduced or in a separate vessel or system between the riser wye and the regenerated catalyst outlet of the regenerator. In either case, care should be taken to prevent any backflow of hydrogen toward the regenerator. To ensure effective reduction of the nickel , carbon on the " re¬ generated catalyst is preferably less than 0.25 weight percent, more preferably less than 0.1 weight percent, and most pref¬ erably less than 0.05 weight percent. The amount of vanadium present on the catalyst also is preferably minimized because large ratios of vanadium to nickel may interfere with the steam reforming reaction. The ratio of vanadium to nickel both in the feed and on the catalyst is preferably less than about 3.0, more preferably less than about 2.0 and most preferably about 1.0 or less. Because relatively high accumulations of heavy metals and coke precursors on the catalyst can block steam reforming sites, as well as catalytic cracking sites, the invention preferably em¬ ploys a catalyst having both a relatively high surface area and a relatively high pore volume. The high surface area pro¬ vides places for adsorption of coke precursors and deposition of heavy metals without undue covering of cracking sites wh le the high pore volume makes blockage of pore passageways by these materials less likely. The surface area of the catalyst is preferably greater than 40 square meters per gram, more preferably greater than 80 square meters per gram, and most preferably in the range of 30 to 250 square meters per gram. The pore volume of the catalyst is preferably greater than 0.2 cc/gm, more preferably at least 0-3 cc/gm and most preferably at least about 0.5 cc/gm. The steam reforming conditions employed in the prior art usu involve relatively high pressures, relatively low temperatur an absence of coke deposition on the reforming catalyst and relatively long contact times between catalyst and reactants In comparison, the process conditions of the present inventi are at what might be considered the opposite extreme, namely, low pressure, high temperature, high coke deposition and sho contact times. Accordingly, the carbo-metallic oil conversi process disclosed herein employs riser pressures of preferab less than 100 psia and more preferably in the range of about 35 to about 45 psia; catalyst temperatures at the inlet to t riser of preferably ' greater than 1000°F and more preferably the range of 1200 to 1400°F; coke levels on the catalyst of to about 3 weight percent and preferably in the range of abo 0.3 to about 1.0 weight percent based on weight of catalyst; and contact times of preferably less than 3 seconds and more preferably in the range of 0.5 to 2 seconds. ΓOR OMH Depending on how the process of the invention is prac¬ tised, one or more of the following additional advantages may be realized. If desired, and preferably, the process may be operated without added hydrogen in the reaction chamber. If desired, and preferably, the process may be operated without prior hydrotreating of the feed and/or without other process of removal of asphaltenes of metals from the feed, and this is true even where the carbo- metallic oil as a- whole contains more than about 4, or more than about 5 cr even more than about 5.5 ppm Nickel Equivalents by weight of heavy metal and has a carbon residue on pyrolysis greater than about 1% or greater than about 2% by weight. Moreover, all of the converter feed, as above described, may be cracked in one and the same conversion chamber. The cracking reaction may be carried out with a catalyst which has previously been used (recycled, except for such replacement as required to compensate for normal losses and deactivation) to crack a carbo-metallic feed under the above described condi¬ tions. Heavy hydrocarbons not cracked to gasoline in a first pass may be recycled with or without hydrotreating for further cracking in contact with the same kind of feed in which they were first subjected to cracking con¬ ditions, and under the same kind of conditions; but op¬ eration in a substantially once-through or single pass mode (e.g. less than about 15% by volume of recycle based on volume of fresh feed) is preferred. Brief Description of the Drawings Fig. 1 is a graph showing the relationship between catalyst relative activity and volume percent MAT conversion. Fig. 2 is a schematic diagram of an apparatus for carrying out the process of the invention. Fig. 3 is a schematic diagram of another apparatus for carrying out the process of the invention- Best and Other Illustrative Modes for Carrying Out the Invention In accordance.with this invention a process is provided for converting carbo-metallic feedstocks containing 650°F ma¬ terial and having a residue on pyrolysis of at least about one and containing at least about four ppm nickel equiva¬ lents of heavy metals comprising bringing said feedstock in contact with a cracking catalyst in a progressive flow reactor under conditions whereby light products and coke are formed and coke and heavy metals deposit onto the catalyst. The spent catalyst is regenerated by contacting it with an oxygen-containing gas under conditions whereby at least a portion of said coke is converted to carbon oxides and the regenerated catalyst is recycled to the reactor for contact with fresh feed. - OMPI In order to decrease the amount of coke accumulating on the cracking catalyst and increase the selective cracking provided by the catalyst in the presence of high nickel accumulations on the catalyst, nickel deposits on the catalyst are reduced from the oxide state provided by the regenerator and the cata¬ lyst with deposited nickel in the reduced state is contacted with a carbo-metallic oil feed in the presence of water at relatively high weight ratios of water to feed. While not intending to be bound by any one theory or hypothesis for the improvements realized, it is believed that the reduced nickel on the conversion catalyst in the presence of an oxygen defi¬ cient carbo-metallic oil feed and relatively high mole ratios of water to feed result in steam reforming reactions in which hydrocarbon molecules react with water to form carbon oxides and labile hydrogen. • • The initial level of nickel on the conversion catalyst may be deposited on the catalyst by the carbo-metallic oil feed itself during the conversion process of the invention or by some other means, such as prior use of the catalyst in an FCC process employing a nickel containing feed, such " as a VGO mixed with a relatively small amount of reduced crude or other nickel containing fraction. The term "deposited nickel" is used in this specification to distinguish catalyst in which nickelmigh otherwise be present in the materials from which the catalyst composition is made, such as natural clays or other components-- containing nickel. Any such nickel that might incidentally be present inthe catalyst composition is usually tied up in com¬ pounds or covered over by catalyst matrix material so as not to be in a sufficiently active form for purposes of the present invention. It is believed that to be effective in the steam reforming reactions of the invention, the deposited nicke should be present in the form of relatively large crystallites of reduced nickel, the largest dimension of which is preferably greater than about 10, more preferably greater than about 20, and most preferably greater than about 40 " angstrom units. "Nickel crystallites of this size may be present either on the zeolitic component or the matrix comoonent of the catalyst. It is furs. ther believed that the formation of such nickel crystallites, as opposed to a monolayer of nickel atoms, requires deposited nickel levels substantially greater than 600 ppm and more likely greater than about 1000 ppm. Accordingly, a preferre catalyst for practicing the invention comprises an equilibriu conversion catalyst having levels of deposited nickel of at least 2000 ppm, preferably at least 3000 ppm, more preferably in the range of 6000 to 30,000 ppm, and most preferably in th range of 7000 to 20,000 ppm. When the foregoing catalyst is passed through a regenerator t burn off deposited coke in the presence of an oxidizing gas, such as air, the nickel deposits on the catalyst are placed in an oxidized state. According to the present invention, catalyst from the ' .regenerator is treated with a reducing gas so that the nickel on the regenerated catalyst is in a reduce state at the time it is introduced into the conversion zone of the riser. Without this reduction treatment, it is believed that little, if any, steam reforming will take place in the riser. Treatment of the regenerated catalyst with reducing gas may take place either in the regenerated catalyst stand- pipe, in a separate vessel or system between the regenerated catalyst outlet of the regenerator and the riser wye, and/or in an upstream section or reducing zone of the riser itself. If an explosive", reducing gas is used, care should be taken to prevent any backflow toward the regenerator or a component discharging gases to the regenerator, suchas the regenerated catalyst stripper and portions of the regenerated catalyst standpipe upstream of the reducing vessel or zone. The amount of reducing gas used is preferably sufficient to provide al¬ most a pure reducing atmosphere in contact with the nickel deposits on the catalyst. Where an upstream portion of the riser is used as the reducing zone, such as near the bottom of a vertical, upflow riser, the reducing gas may also serve as a lift gas to assist in trans¬ porting catalyst along or up the riser to the point at which OM the reduced catalyst is mixed with the feed and water componen If the amount of reducing gas does not provide sufficient cata lyst lift, other lift gases, such as steam and/or liquid water may be used. However, it is preferably to keep the partial pr sure of these additional lift gases relatively low relative to the reducing gas so as to keep the reducing atmosphere as pure as practicable. It is particularly desirable to keep the amou of water used for lifting to a minimum because the presence of water, either as liquid or steam, may interfere with the reduc ing reaction. -* The preferred reducing gases for practicing the invention in¬ clude hydrogen, carbon monoxide, methane and/or natural gas. The term "reducing gas" also contemplates materials which are liquid at ambient conditions but vaporize at riser conditions, such as portions of the feedstock itself. Because the other gases specified are explosive * * at regenerator conditions, it is preferable to use carbon monoxide as the reducing gas where there may be at least some backflow into the regenerator, such as when using the lower section of the regenerated catalyst standpipe as a reducing zone. In this arrangement, the carbon dioxide formed by the reduction reaction and the excess carbon monoxide over that consumed in the reduction reaction may pass back into the regenerator and be discharged from the system with the regenerator flue gases. A preferred source of carbon monoxide is the flue gas from the first stage of a two stage regenerator which is operated with an oxygen deficient first stage and a relatively high CO/CO- ratio as explained elsewher in this specification. The reducing reaction with carbon mono ide is preferably controlled so as to avoid depositing signifi cant amounts of carbon on the catalyst since such carbon depos its may preferentially migrate to and cover steam reforming nickel sites. Where the reducing zone is isolated from the regenerator, such as in the bottom of the riser or in a sep¬ arate reducing vessel, the reducing gas is preferably hydrogen for the reasons explained more fully below. After reduction of the nickel deposits on the catalyst (referr to hereafter as "reduced catalyst"), the reduced catalyst is contacted with the carbo-metallic feed in the presence of stea at weight ratios of water to feed up to 1.0, preferably up to 0.5, more preferably in the range from about 0.15 to about 0.3 and most preferably in the range of about 0.2 to about 0.3. Based on an average hydrocarbon molecular weight of about 275 in the feed, these weight ratios correspond approximately to t following respective ratios of water partial pressure to feed partial pressure in the riser: up to about 14:1, preferably u to about 7:1, more preferably in the range from about 2:1 to about 5:1, and most preferably in the range of about 3:1 to 4:1. The water may be introduced initially into the riser either directly or with the feed and as either liquid water or steam. The water contacts the nickel containing catalyst and the carb metallic oil feed under conversion conditions such that the st is reformed in the riser to provide labile hydrogen and the fe is converted in the presence of this labile hydrogen to provid increased yields of gasoline and other liquid fuel products. While not intending to be bound by any one theory, it is be¬ lieved that as the heavy carbonaceous fractions of the feed ar cracked, the labile hydrogen reacts with the cracked fraσments to increase the hydrogen/carbon ratio of the carbonaceous frag ments and provide useful liquid fuel products. In the absence of the reduced nickel and steam reforming conditions of the in vention, it is believed that these carbonaceous fragments com¬ bine to form heavy hydrocarbon deposits which are non-strippabl and comprise one of the coke components on spent catalyst. To ensure effective reduction of the nickel deposits, carbon on the regenerated catalyst is preferably less than 0.25 weight percent, more preferably less than 0.1 weight percent, and most preferably less than 0.05 weight percent. The amount of vana¬ dium present on the catalyst also is preferably minimized be^. cause large ratios of vanadium to nickel, which is about the same as the atomic ratio, both in the feed and on the catalyst is preferably less than about 3.0, more preferably less than about 2.0 and most preferably about 1.0 or less. As high levels of hydrogen sulfide may interfere with the steam reforming reactions by tying up reduced nickel sites as less reactive nickel sulfides, the amounts of hydrogen sulfide present in the riser are preferably minimized, particularly in ^ the lower half of the riser conversion zone where the steam reforming reactions are initiated. Accordingly, any outside process streams used inpracticing the invention, such as those that may be used to provide diluent and/or lift gases in the riser, preferably do not contain significant amounts of hydro¬ gen sulfide. The catalyst employed in the carbo-metallic oil conversion pro cess preferably has a high surface area to provide places for the adsorption of coke precursors and the deposition of heavy metals without undue covering of catalytic sites, whether for steam reforming or catalytic cracking. The catalyst also pref erably has a high pore volume so that blockage of pore passage ways by accumulations of heavy metals and coke precursors is less likely to occur. The relatively high accumulations of heavy metals and coke precursors on the catalyst when cracking carbo-metallic oils readily cover and block catalytic sites on catalyst having relatively low surface areas and/όr pore volum Accordingly, catalysts for the present invention preferably have surface areas of at least 40 square meters per gram, more preferably at least 80 square meters per gram and most prefera¬ bly in the range of 80 to 250 square meters per gram, and pore volumes of at least about 0.2 cc/gm, more preferably at least about 0.3 cc/gm, still more preferably in the range of about 0.2 to 0.5 cc/gm and most preferably at least about 0.5 cc/gm. In marked contrast to the prior art, the process conditions of the present invention for steam reforming include relatively low pressures, relatively high temperatures, relatively large amounts of deposited coke, and relatively short contact times between catalyst and the feed and steam reactants. Accordingly, pressures in the riser are preferably less than about 100 psia and more preferably in the range of about 35 to about 45 psia, catalyst temperatures at the inlet to the riser are preferably greater than 1000°F - more preferably in the range of 1200 to 1400°F, coke levels on the catalyst leaving the riser may be up to about 3 weight percent based on weight of catalyst and more preferably in the range of about 0.3 to about 1.0 weight percent, catalyst temperatures at the exit from the riser are preferably greater than 900°F and more preferably in the range of about 1000 to about 1100°F, and the contact time between catalyst and feed is preferably less than -about 3 seconds and more preferably in the range of 0.5 to 2 seconds. The prior art suggests that the steam reforming of hydro¬ carbons to produce hydrogen and carbon monoxide mixtures require highly active and stable catalysts with high concentrations of nickel, say in the range of 10-40 weight percent. These catalysts are stabilized by the addition of alkali metal compounds such as potassium oxide. In comparison, the catalyst used in practicing the present invention utilizes nickel concen¬ trations of 0.5-2 wt% with emphasis placed on the elimination of as much of the alkali metals and their salts as practicable from the feedstock and the catalyst. The second area of major difference between the process of this invention and conventiona steam reforming is related to carbon deposition on catalyst. In conventional steam reforming, a fixed catalyst bed is used and carbon deposition must be kept to almost nil because relatively- low levels of coke and/or carbide formation lower catalyst activity to unacceptable levels. In comparison, the method of this invention employs a large circulating inventory of catalyst which is continuously regenerated so that: the coke and/or deposition does not adversel affect the lone term activi erf; OMP -25b- the catalyst for steam reforming. The prior art suggests that nickel deposits on conversion cata¬ lyst tend to increase coke production by catalyzing adverse de- hydrogenation/coking reactions. However, the steam reforming process of the present invention sufficiently predominatesover such countervailing coking reactions to provide significant decreases in the overall coke make of. the carbo-metallic oil conversion process. Thus, the amount of contaminant coke, which is that coke produced by both cracking and dehydrogenation reactions, may be reduced by as much as one half or more compared to the - . same conversion process in the same equipment but without re¬ ducing the nickel on the catalyst and with water present in amounts less than 0.15 weight percent relative to eight of feed. The consumption of coke by the steam re¬ forming reaction of the process may also reduce the levels of Conradson coke on spent catalyst fed to the regenerator froπr- the spent catalyst stripper. Furthermore, the presence of re¬ duced catalyst and relatively high levels of water in the con¬ version zone are believed to greatly enhance the selective cracking activity of the conversion catalyst itself. Nickel Equivalents by weight and by a carbon residue on pyrolysis of at least about 1% and more preferably at least about 2% by weight. In accordance with the in¬ vention, the carbo-metallic feed, in the' form of a pump- able liquid, is brought into contact with hot conver¬ sion catalyst in a weight ratio of catalyst to feed in the range of about 3 to about 18 and preferably more than about 6. . The feed in said mixture undergoes a conversion step which includes cracking while the mixture of feed and catalyst is flowing through a progressive flow type reactor. The reactor includes an- elongated reaction chamber which is at least partly vertical or inclined and in which the feed material, resultant products and catalyst are maintained in contact with one another while flowing as a dilute phase or stream for a predetermined riser residence time in the range of about 0.5 to about 10 seconds. The feed, catalyst, and other materials may be introduced into the reaction chamber at one or more points along its length. The reaction is conducted at a temperature of about 900° to about 1400°F, measured at the reaction chamber exit, under a total pressure of about 10 to about 50 psia (pounds per square inch absolute) under conditions sufficiently severe to provide a conversion per pass in the range of about 50% or more and to lay down coke on the catalyst in an amount in the range of about 0-3 to about 3% by weight of catalyst and preferably at least about 0.5%. The overall rate of coke production, based on weight of fresh feed, is in the range of about 4 to about 14. by weight. At the end of the predetermined residence time, the cata- - 26 - The present invention provides increased levels of labile hydro¬ gen in the riser without the necessity of hydrotreating the feed and/or the use of hydrocracking processes which require large amounts of hydrogen at high pressure and expensive high pressure hydrocracking equipment. .The amounts of hydrogen produced are sufficiently large to provide the quantities of hydrogen needed for recycling the product as the reducing- gas for the process. Thus, the steam reforming process of the invention may provide 50 _ times or more hydrogen by weight based on weight of feed as com¬ pared to the same conversion process in the same conversion ap¬ paratus but in the absence of reduced catalyst and with less than 0.15 weight percent water based on weight of feed. In this re¬ gard, the dry gas product from the conversion process may be comprised of 30 or more weight percent hydrogen based on total weight of dried gas. The conversion process and apparatus must also take into account the increased volumes both of vapor product in the riser and of dry gas product. Thus, steam reforming may increase the total vapor product volume by as much as two or three times and re¬ sult in contact times of less than 0.5 seconds in pre-existing riser designs. Similarly, the capacity of vapor product and dry gas handling equipment may have to be increased to ac¬ commodate the larger volumes of hydrogen produced by the process. The present invention is notable in providing a simple, relatively straightforward and highly productive approach to the conversion of carbo-metallic feed, such as reduced crude or the like, to various lighter products such as gasoline- The carbo-metallic feed comprises or is composed of oil which boils above about 650 C F. Such oil, or at least the 650°F÷ portion thereof, is characterized by a heavy metal content of at least about 4, preferably more than about 5, and most preferably at least about 5.5 ppm of - 28 - lyst is separated from the products, is stripped to remove high boiling components and other entrained or adsorbed hydrocarbons and is then regenerated with oxygen-contain¬ ing combustion-supporting gas under conditions of time, temperature and atmosphere sufficient to reduce the car¬ bon on the regenerated catalyst to about 0-25% or less and preferably about 0-05% or less by weight. Depending on how the process of the invention is practiced, one or more of the following additional advantages may be realized. If desired, and preferably, the process may be operated without added hydrogen in the reaction chamber. If desired, and preferably, the process may be operated without prior hydrotreating of the feed and/or without other process of removal of asphaltenes of metals from the feed, and this is true even where the carbo-metallic oil as a whole contains more than about 4, or more than about 5 or even more than about 5.5 ppm Nickel Equivalents by weight of heavy metal and has a carbon residue on py¬ rolysis greater than about 1%, greater than about 1.4% or greater than about 2% by weight- Moreover, all of the converter feed, as above described, may be cracked in one and the same conversion chamber. The cracking re¬ action may be carried out with a catalyst which has pre¬ viously been used (recycled, except for such replacement as required to compensate for normal losses and deactivation to crack a carbo-metallic feed under the above described conditions. Heavy hydrocarbons not cracked to gasoline in a first pass may be recycled with or without hydrotreating for further cracking in contact -with the same kind of feed in which they were first subjected to cracking conditions, and under the same kind of conditions; but operation in a substantially once-through or single pass mode (e.g. less than about 15% by volume of recycle based on volume of fresh feed) is preferred. - 29 - According to one preferred embodiment or aspect of the invention, at the end of the predetermined residence time referred to above, the catalyst is projected in a direction established by the elongated reaction chamber or an extension thereof, while the products, having les¬ ser momentum, are caused to make an abrupt change of di¬ rection, resulting in an abrupt, substantially instan¬ taneous ballistic separate of products from catalyst. The thus separated catalyst is then stripped, regenerated and recycled to thi-/""reactor as above described. According to another preferred embodiment or aspect of the invention, the converter feed contains 650°F- * - material which has not been hydrotreated and is characterized in part by containing at least about 5.5 parts per million of Nickel Equivalents of heavy metals. The converter feed is brought together not only with the above mentioned cracking catalyst, but also witϋ additional gaseous ma¬ terial including steam whereby the resultant suspension of catalyst and feed also includes gaseous material wherein the ratio of the partial pressure of the added gaseous material relative to that of the feed is in the range of about 0.25 to about 4-0. The vapor residence time is in the range of about 0.5 to about 3 seconds when practicing this embodiment or aspect of the invention. This preferred embodiment or aspect and the one referred to in the preced¬ ing paragraph may be used in combination with one another or separately. According to another preferred embodiment or aspect of the invention, the carbo-metallic feed is not only brought into contact with the catalyst, but also with one or more addi¬ tional materials including particularly liquid water in a weight ratio relative to feed ranging from about 0.04 to about 0.25, more preferably about 0-04 to about 0.2 and still more preferably about 0-05 to about 0-15- Such addi- - 30 - tional materials, including the liquid water, may be brought into admixture with the feed prior to, during or after mixing the feed with the aforementioned catalyst, and either after or, preferably, before, vaporization of the feed. The " feed, catalyst and water (e.g. in the form of liquid water or in the form of steam produced by vap¬ orization of liquid water in contact with the f ed) are introduced into the progressive flow type reactor, which may or may not be, a reactor embodying the above described ballistic separatioi, at oneor more points along the re¬ actor. While the mixture of feed, catalyst and steam produced by vaporization of the liquid water flows through the reactor, the feed undergoes the above mentioned con¬ version step which includes cracking. The feed material, catalyst, steam and resultant products are maintained in contact with one another in the above mentioned elongated reaction chamber while flowing as a dilute phase or stream for the above mentioned predetermined riser residence time which is in the range of about 0.5.to about 10 seconds, pref¬ erably about 0.5 to about 2 seconds. The present invention provides a process for the continu¬ ous catalytic conversion of a wide variety of carbo- metallic oils to lower molecular weight products, while maximizing production of highly valuable liquid products, and making it possible, if desired, to avoid vacuum distil¬ lation and other expensive treatments such as hydrotreating. The term "oils", includes not only those predominantly hydrocarbon compositions which are liquid at room tempera¬ ture (i.e., 63°F) , but also those predominantly hydrocarbon compositions which are asphalts or tars at ambient temp¬ erature but liquify when heated to temperatures in the range of up to about 800°F- The invention is applicable to carbo-metallic oils, whether of petroleum origin or not- For example, provided they have OMPI - 31 - the requisite boiling range, carbon residue on pyrolysis and heavy metals content, the invention may be applied to the processing of such widely diverse materials as heavy bot¬ toms from crude oil, heavy bitumen crude oil, those crude oils known as "heavy crude" which approximate the proper¬ ties of reduced crude, shale oil, tar sand extract, pro¬ ducts from coal liquification and solvated coal, atmospheric and vacuum reduced crude, extracts and/or bottoms (raf- finate) from solvent deasphalting, aromatic extract from lube oil refining, tar bottoms, heavy cycle oil, slop oil, other refinery waste streams and mixtures of the foregoing. Such mixtures can for instance be prepared by mixing available hydrocarbon fractions, including oils, tars, pitches and the like. Also, powdered coal may be suspended in the carbo-metallic oil. Persons skilled in the art are aware of techniques for demetalation of carbo- metallic oils, and demetalated oils may be converted using the invention; but it is an advantage of the invention that it can employ as feedstock carbo-metallic oils that have had no prior demetalation treatment. Likewise, the inven¬ tion can be applied to hydrotreated feedstocks; but it is an advantage of the invention that it can successfully convert carbo-metallic oils which have had substantially no prior hydrotreatment.. However, the preferred appli¬ cation of the process is to reduced crude, i.e., that fraction of crude oil boiling at and above 650°F, along or in admixture with virgin gas oils- While the use of material that has been subjected to prior vacuum distilla ¬ tion is not excluded, it is an advantage of the invention that it can satisfactorily process material which has had no prior vacuum distillation, thus saving on capital in¬ vestment and operating costs as compared to conventional FCC processes that require a vacuum distillation unit. - 32 - In accordance with the invention one provides a carbo- metallic oil feedstock, at least about 70%, more pref¬ erably at least about 85% and still more preferably about 100% (by volume) of which boils at and above about 650°F. All boiling temperatures herein are based on standard at¬ mospheric pressure conditions. In carbo-metallic oil partly or wholly composed of material which boils at and above about 650°F, such material is referred to herein as 650°F+ material; and 65C°F+ material which is part of or has been separated from an oil containing component boiling above and below 650°F may be referred to as a 650°F+ fraction. But the terms "boils above" and "650 o F+" are not intended to imply that all of the material characterized by said terms will have the capability of boiling. The carbo- metallic oils contemplated by the invention may contain material which may not boil under any conditions; for example, certain asphalts and asphaltenes may crack thermally during distillation, apparently without boil¬ ing. Thus, for example, when it is said that the feed comprises at least about 70% by volume of material which boils above about 650°F, it should be understood that the 70% in question may include some material which will not boil or volatilize at any temperature. These non-boilable materials when present, may frequently or for the most part be concentrated in portions of the feed which do not boil below about 1000°F, 1025°F or higher. Thus, when it is said that at least about 10%,. ore preferably about 15%, and still more preferably at least about 20% (by volume) of the 650°F+ fraction will not boil below about l000 o F or 1025°F, it should be understood that all or any part of the material not boiling below about 1000°F or 1025°F, may or may not be volatile at and above the indicated temp¬ eratures. Preferably, the contemplated feeds, or at least the 650 0 F÷ material therein, have a carbon residue on pyrolysis of - 33 - at least about 2 or greater. For example, the Conradson carbon content may be in the range of about 2 to about 12 and most frequently at least about 4. A particularly common range is about 4 to about 8. Those feeds having a Conradson carbon content greater than about 6 may need special means for controlling excess heat in the regenerator. Preferably, the feed has an average composition character¬ ized by an atomic hydrogen to- carbon ratio in the range. of about 1.2 to about 1.9, and preferably about 1.3 to about 1.8. The carbo-metallic feeds employed in accordance with the invention, or at least the 650°F+ material therein, may contain at least about 4 parts per million of Nickel Equivalents, as defined above, of which at least about 2 parts per million is nickel (as metal, by weight). Carbo- metallic oils within the above range can be prepared from mixtures of two or more oils, some of which do and some of which do not contain the quantities of Nickel Equivalents and nickel set forth above. It should also be noted that the above values for Nickel Equivalents and nickel repre¬ sent time-weighted averages for a substantial period of operation of the conversion unit, such as one month, for example. It should also be noted that the heavy metals have in certain circumstances exhibited some lessening of poisoning tendency after repeated oxidations and reductions on the catalyst, and the literature describes criteria for establishing "effective metal" values. For example, see the article by Cimbalo, et al-, entitled "Deposited Metals Poison FCC Catalyst", Oil and Gas Journal, May 15, 1972, pp 112-122, the contents of which are incorporated herein by reference- If considered necessary or desirable, the contents of Nickel Equivalents and nickel in the carbo- metallic oils processed according to the invention may be - 34 - expressed in terms of "effective metal" values. Notwith¬ standing the gradual reduction in poisoning activity noted by Cimbalo, et al-, the regeneration of catalyst under normal FCC regeneration conditions may not, and usually does not, severely impair the dehydrogenation, demethana- tion and aromatic condensation activity of heavy metals accumulated on cracking catalyst. - 35 - It is known that about 0.2 to about 5 weight percent of "sulfur" in the form of elemental sulfur and/or its com¬ pounds (but reported as elemental sulfur based on the weight of feed) appears in FCC feeds and that the sulfur and modi¬ fied forms of sulfur can find their way into thtr resultant gasoline product and, where lead is added, tend to reduce its susceptibility to octane enhancement. Sulfur in the product gasoline often requires sweetening when process¬ ing high sulfur containing crudes. To the extent that sulfur is present ii the coke, it also represents a po¬ tential air pollutant since the regenerator burns it to SO- and SO-. However, we have found that in our pro¬ cess the sulfur in the feed is on the other hand able to inhibit heavy metal activity by maintaining metals such as Ni, V, Cu .and Fe in the sulfide form in the reactor. * These sulfides are much less active than the metals them¬ selves inpromoting dehydrogenation and coking reactions. Accordingly, it is acceptable to carry out the invention with a carbo-metallic oil having at least about 0.3%, ac¬ ceptably more than about 0.8% and more acceptably at least about 1.5% by weight of sulfur in the 650°F+ frac¬ tion. The carbo-metallic oils useful in the invention may and usually do contain significant quantities of heavy, high boiling compounds containing nitrogen, a substantial por¬ tion of which may be basic nitrogen. For example, the total nitrogen content of the carbo-metallic oils may be at least about 0.05% by weight. Since craclcing catalysts owe their cracking activity to acid sites on the catalyst surface or in its pores, basic nitrogen-containing com¬ pounds may temporarily neutralize these sites, poisoning the catalyst- However, the catalyst is not permanently damaged since the nitrogen can be burned off the catalyst during regeneration, as a result of which the acidity of the active sites is restored. - 36 - The carbo-metallic oils may also include significant quanti¬ ties of pentane insolubles, for example at least about 0.5% by weight, and more typically 2% or more or even about 4% or more. These may include for instance as¬ phaltenes and other materials. Alkali and alkaline earth metals generally do not tend to vaporize in large quantities under the distillation condi¬ tions employed in, distilling crude oil to prepare the vacuum gas oils norτ-ally used as FCC feedstocks. Rather, these metals remain for the most part in the "bottoms" fraction (the non-vaporized high boiling portion) which may for instance be used in the production of asphalt or other by-products. However, reduced crude and other carbo- raetallic oils are in many cases bottoms products, and therefore may contain significant quantities of alkali and alkaline earth metals such as sodium. These metals deposit upon the catalyst during cracking. Depending on the composition of the catalyst and magnitude of the regen¬ eration temperatures to which it is exposed, these metals may undergo interactions and reactions with the catalyst (including the catalyst support) which are not normally experienced in processing VGO under conventional FCC processing conditions. If the catalyst characteristics and regeneration conditions so require, one will of course take the necessary precautions to limit the amounts of alkali and alkaline earth metal in the feed, which metals may enter the feed not only as brine associated with the crude oil in its natural state, but also as components of water or steam which are supplied to the cracking unit. Thus, careful desalting of the crude used to prepare the carbo-metallic feed may be important when the catalyst is particularly susceptible to alkali and alkaline earth metals, In such circumstances, the content of such metals (herein¬ after collectively referred to as "sodium") in the feed can be maintained at about 1 ppm or less, based on the weight • iR-E^ - 37 - of the feedstock. Alternatively, the sodium level of the feed may be keyed to that of the catalyst, so as to main¬ tain the sodium level of the catalyst which is in use sub¬ stantially the same as or less than that of the replacement catalyst which is charged to the unit. According to a particularly preferred emobidment of the in¬ vention, the carbo-metallic oil feedstock constitutes at least about 70% by volume of material which boils above about 650°F, and at least about 10% of the material which boils above about 650°F will not boil below about 1025°F. The average composition of this 650°F+ material may be further characterized by: (a) an atomic hydrogen to carbon ratio in the range of about 1.3 to about 1.8; (b) a Conradson carbon value of at least about 2; (c) at least about four parts per million of Nickel Equivalents, as defined above, of which at least about two parts per million is nickel (as metal, by weight) ; and (d) at least one of the following: (i) at least about 0.3% by weight of sulfur, (ii) at least about 0.05% by weight of nitrogen, and (iii) at least about 0.5% by weight of pentane insolu- bles. Very commonly, the preferred feed will include all of (i) , (ii) , and (iii) , and other components found in oils of petroleum and non-petroleum origin may also be present in varying quantities providing they do not pre¬ vent operation of the process. Although there is no intention of excluding the possibility of using a feedstock which has previously been subjected to some cracking, the present invention has the definite advantage that it can successfully produce large conver¬ sions and very substantial yields of liquid hydrocarbon fuels from carbo-metallic oils which have not been subject¬ ed to any substantial amount of cracking. Thus, for example, and preferably, at least about 85%, more preferably at least about 90% a d most preferably substantially a - 38 - the carbo-metallic feed introduced into the present pro¬ cess is oil which has not previously been contacted with cracking catalyst under cracking conditions. Moreover, the process of the invention is suitable for Operation in a substantially once-through or single pass mode. Thus, the volume of recycle, if any, based on the volume of fresh feed is preferably about 15% or less and more preferably about 10% or less. In general, the weight ratio of catalyst to fresh feed (feed which has not previously been exposed to cracking catalyst under cracking conditions) used in the process is in the range of about 3 to about 18. Preferred and more preferred ratios are about 4 to about 12, more pref¬ erably about 5 to about 10 and still more preferably about 6 to about 10, .a ratio of about 10 presently being con¬ sidered most nearly optimum. Within the limitations of product quality requirements, controlling the catalyst to oil ratio at relatively low levels within the aforesaid ranges tends to reduce the coke yield of the process, based on fresh feed. In conventional FCC processing of VGO, the ratio between the number of barrels per day of plant through-put and the total number of tons of catalyst undergoing circula¬ tion throughout all phases of the process can vary widely. For purposes of this disclosure, daily plant through-put is defined as the number of barrels of fresh feed boiling above about 650°F which that plant processes per average day of operation to liquid products boiling below about 430°F. For example, in one commercially successful type of FCC-VGO operation, about 8 to about 12 tons of catalyst are under circulation in the process per 1000 barrels per day of plant through-put. In another commercially successful process, this ratio is in the range of about 2 - 39 - to 3. While the present invention may be practiced in the range of about 2 to about 30 and more typically about 2 to about 12 tons of catalyst inventory per 1000 barrels of daily plant through-put, it is preferred to carry out the process of the present invention with a very small ratio of catalyst weight to daily plant through-put. More specifically, it is preferred to carry out the process of the present invention with an inventory of catalyst that is sufficient to ' contact the feed for the desired residence time in the above indicated catalyst to oil ratio while minimizing the amount of catalyst inventory, relative to plant through-put, which is undergoing circulation or being held for treatment in other phases of the process such as, for example, stripping, regeneration and the like. Thus, more particularly, it is preferred to carry out the process of the present invention with about 2 to about 5 and more preferably about 2 tons of catalyst inventory or less per thousand barrels of daily plant through-put. In the practice of the invention, catalyst may be added continuously or periodically, such as, for example, to make up for normal losses of catalyst from the system. Moreover, catalyst addition may be conducted in conjunc¬ tion with withdrawal of catalyst, such as, for example, to maintain or increase the average activity level of the catalyst in the unit. For example, the- rate at which virgin catalyst is added to the unit may be in the range of about 0.1 to about 3, more preferalby about 0-15 to about 2, and most preferably to about 0.2 to about 1-5 pounds per barrel of feed. If on the other hand equilibrium catalyst from FCC operation is to be utilized, replacement rates as high as about 5 pounds per barrel can be practiced. Where circumstances are such that the catalyst employed in the unit is below average in resistance to deactivation OMP - 40 - and/or conditions prevailing in the unit are such as to promote more rapid deactivation, one may employ rates of addition greater than those stated above; but in the op¬ posite circumstances, lower rates of addition may be em¬ ployed. By way of illustration, if a unit were operated with a metal(s) loading of 5000 ppm Ni + V in parts by weight on equilibrium catalyst, one might for example employ a replacement rate of about 2.7 pounds of catalyst intro¬ duced for each barrel (42 gallons) of feed processed. How- ^ ever, operation at a " higher level such as 10,000 ppm Ni + V on catalyst would enable one to substantially reduce the replacement rate, such as for example to about 1.3 pounds of catalyst per barrel of feed. Thus, the levels of metal(s) on the catalyst and catalyst replacement rates may in gen¬ eral be respectively increased and decreased to any value consistent with the catalyst activity which is available and desired for conducting the process. Without wishing to be bound by any theory, it appears that a number of features of the process to be described in greater detail below, such as, for instance, the residence time and optional mixing of steam with the feedstock, tend to restrict the extent to which cracking conditions pro¬ duce metals in the reduced state on the catalyst from heavy metal sulfide(s), sulfate(s) or oxide(s) deposited on the catalyst particles by prior exposures of carbo-metallic feedstocks and regeneration conditions. Thus, the process appears to afford significant control over the poisoning effect of heavy metals on the catalyst even when the ac¬ cumulations of such metals are quite substantial. Accordingly, the process may be practiced with catalyst bearing accumulations of heavy metal(s) in the form of elemental metal(s), oxide(s), sulfide(s) or other compounds which heretofore would have been considered quite intoler¬ able in conventional FCC-VGO ooerations. Thus, - 41 - of the process with catalyst bearing heavy metals accumu¬ lations in the range of about 3,000 or more ppm Nickel Equivalents, on the average, is contemplated. The con¬ centration of Nickel Equivalents of metals on catalyst can range up to about 50,000 ppm or higher. More specifically, the accumulation may be in the range of about 3,000 to about 30,000 ppm, preferably in the range of 3,000 to 20,000 ppm, and more preferably about 3,000 to about 12,000 ppm. Within these ranges just mentioned, operation at metals levels of about 4,000 or more, about 5,000 or more, or about 7,0C3 " or more ppm can tend to reduce the rate of catalyst replacement required. The foregoing ranges are based on parts per million of Nickel Equiva¬ lents, in which the metals are expressed as metal, by weight, measured on and based on regenerated equilibrium catalyst. However, in the event that catalyst of adequate activity is available at very low cost, making feasible very high rates of catalyst replacement, the carbo-metallic oil could be converted to lower boiling liquid products with catalyst bearing less than 3,000 ppm Nickel Equiva¬ lents of heavy metals. For example, one might employ equi¬ librium catalyst from another unit, for example, an FCC unit which has been used in the cracking of a feed, e.g. vacuum gas oil, having a carbon residue on pyrolysis of less than 1 and containing less than about 4 ppm Nickel Equivalents of heavy metals. The invention described in this specification may be employed in the processes and apparatuses for carbo-metallic oil con¬ version described in co-pending U-S. Applications Serial Nos. 94,091, 94,092, 94,216, 94,217 and 94,277, all filed November 14, 1979; and Serial Nos. 246,751, 246,782 and 246,791, all filed March 23, 1981; said applications being in the name of George D. Myers alone or jointly with Lloyd E. Busch and assigned or to be assigned to Ashland Oil, Inc., - 42 - and the entire disclosure of each of said applications being incorporated herein by reference. While the processes descri in these applications can handle reduced crudes or crude oils containing high metals and Conradson carbon values not susceptible-previously to direct processing, certain crudes such as Mexican Mayan or Venezuelan and certain other types of oil feeds contain abnormally high heavy metals and Conrads carbon values. If these very poor grades of oil are processe in a carbo-metallic process, they may lead to uneconomical operations because of high heat loads on the regenerator and/or high catalyst addition rates to maintain adequate catalyst activity and/or selectivity. In order to improve the grade of very poor grades of oil, such as those contain¬ ing more than 50 ppm heavy metals and/or more than 8 weight percent Conradson carbon and preferably more than 100 ppm heavy metals and/or more than 10 weight percent Conradson carbon, these oils may be pretreated with a sorbent to reduce the levels of these contaminants to the aforementioned or lower values. Such upgrading processes are described in U.S. Patent No. 4,263,128 of April 21, 1981, in the name of David B. Bartholic, and in International Patent Application No. PCT/US81/00357 filed in the U.S. Receiving Office on March 19, 1981, in the names of Ashland Oil, Inc., et al. , and entitled "Immobilization of Vanadia Deposited on Sorbent Materials During Treatment of Carbo-Metallic Oils", the entire disclosures of said patent and said application being incorporated herein by reference- preferred mode of up¬ grading residual oils in practicing the " present invention is disclosed in PCT Patent application Serial No. , filed simultaneously herewith in the names of Oliver J. Zandona and Lloyd E. Busch and entitled A COMBINATION PROCESS FOR UPGRADING RESIDUAL OILS, the entire disclosure of said PCT application being incorporated herein by reference. OMPI - 43 - In any event, the equilibrium concentration of heavy metals in the circulating inventory of catalyst can be controlled (including maintained or varied as desired or needed) by manipulation of the rate of catalyst addition discussed above. Thus, for example, addition of catalyst may be maintained at a rate which will control the heavy metals accumulation on the catalyst in one of the ranges set forth above. - 44 - In general, it is preferred to employ a catalyst having a relatively high level of cracking activity, providing high levels of conversion and productivity at low residence times. The conversion capabilities of the catalyst may be expressed in terms of the conversion produced during ac¬ tual operation of the process and/or in terms of conversion produced in standard catalyst activity tests. For example, it is preferred to employ catalyst which, in the course of extended operatiox under prevailing process conditions, is sufficiently active for sustaining a level of conversion of at least about 50% and more preferably at least about 60%. In this connection, conversion is expressed in liquid volume percent, based on fresh feed. Also, for example, the preferred catalyst may be defined as one which, in its virgin or equilibrium state, exhibits a specified activity expressed as a ' percentage in terms of MAT (micro-activity test) conversion. For purposes of the present invention the foregoing percentage is the vol¬ ume percentage of standard feedstock which a catalyst under evaluation will convert to 430°F end point gasoline, light¬ er products and coke at 900°F, 16 WHSV (weight hourly space velocity, calculated on moisture free basis, using clean catalyst which has been dried at 1100°F, weighed and then conditioned, for a period of at least 8 hours at about 25°C and 50% relative humidity, until about one hour or less prior to contacting the feed) and 3C/0 (catalyst to oil weight ratio) by ASTM D-32 MAT test D-3907-80, using an ap¬ propriate standard feedstock, e.g. a sweet light primary gas oil, such as that used by Davison, Division of W. R. Grace, having the following analysis and properties: OMPI - 45 - API Gravity at 60°F, degrees 31.0 Specific Gravity at 60°F, g/cc 0.8708 Ramsbottom Carbon, wt. % 0.09 Conradson Carbon, wt. % 0.04 Carbon, wt. % 84.92 Hydrogen, wt- % 12-94 Sulfur, wt. % 0.68 Nitrogen, ppm 305 Viscosity at 100°F, centistokes 10.36 Watson K Factor 11.93 Aniline Point - ~ 182 Bromine No. 2.2 Paraffins, Vol. % 31.7 Olefins, Vol. % 1.6 Naphthenes, Vol. % 44.0 Aromatics, Vol. % 22.7 Average Molecular Weight 284 Nickel Trace Vanadium Trace Iron Trace Sodium Trace Chlorides Trace B S & W Trace Distillation ASTM D-1160 IBP 445 10% 601 30% 664 50% 701 70% 734 90% 787 FBP 834 OM - 46 - The gasoline end point and boiling temperature-volume per¬ cent relationships of the product produced in the MAT con¬ version test may for example be determined by simulated distillation techniques, for example modifications of gas chromate graphic "Sim-D", ASTM D-2887-73. The results of such simulations are in reasonable agreement with the re¬ sults obtained by subjecting larger samples of material to standard laboratory distillation techniques. Conversion is calculated by subtracting from 100 the volume percent (based on fresh feed) of those products heavier than gaso¬ line which remain in the recovered product. On pages 935-937 of Hougen and Watson, Chemical Process Principles, John Wiley & Sons, Inc., N.Y. (1947), the con¬ cept of "Activity Factors" is discussed. This concept leads to the use of "relative activity" to compare the ef¬ fectiveness of an operating catalyst against a standard catalyst. Relative activity measurements facilitate recog¬ nition of how the quantity requirements of various cata¬ lysts differ from one another. Thus, relative activity is a ratio obtained by dividing the weight of a standard or reference catalyst which is or would be required to pro¬ duce a given level of conversion, as compared to the weight of an operating catalyst (whether proposed or actually used) which is or would be required to produce the same level of conversion in the same or equivalent feedstock under the same or equivalent conditions. Said ratio of catalyst weights may be expressed as a numerical ratio, but preferably is converted to a percentage basis. The standard catalyst is preferably chosen from among cata¬ lysts useful for conducting the present invention, such as for example zeolite fluid cracking catalysts, and is chosen for its ability to produce a predetermined level of conver¬ sion in a standard feed under the conditions of temperature, WHSV, catalyst to oil ratio and other conditions set forth OM - 47 - in the preceding description of the MAT conversion test and in ASTM D-32 MAT test D-3 07-80. Conversion is the volume percentage of feedstock that is converted to 430°F end point gasoline, lighter products and coke. For standard feed, one may employ the above—mentioned light primary gas oil, or equivalent. For purposes of conducting relative activity determinations, one may prepare a * "standard catalyst curve", a chart or graph of conversion " (as above defined) vs. reciprocal WHSV for the standard catalyst and feedstock. A sufficient num¬ ber of runs is made under ASTM D-3907-80 conditions (as modified above) using standard feedstock at varying levels of WHSV to prepare an accurate "curve" of conversion vs. WHSV for the standard feedstock. This curve should tra¬ verse all or substantially all of the various levels of conversion including the range of conversion within which it is expected that the operating catalyst will be tested. From this curve, one may establish a standard WHSV for test comparisons and a standard value of reciprocal WHSV corre¬ sponding to that level of conversion which has been chosen to represent 100% relative activity in the standard cata¬ lyst. For purposes of the present disclosure the afore¬ mentioned reciprocal WHSV and level of conversion are, re¬ spectively, 0.0625 and 75%. In testing an operating cata¬ lyst of unknown relative activity, one . conducts a suffi¬ cient number of runs with that catalyst under D-3907-S0 conditions (as modified above) to establish the level of conversion which is or would be produced with the operat¬ ing catalyst at standard reciprocal WHSV- Then, using the above-mentioned standard catalyst curve, one establishes a hypothetical reciprocal WHSV constituting the recipro¬ cal WHSV which would have been required, using the standard catalyst, tc obtain the same level of conversion which was or would be exhibited, by the operating catalyst at stan- - 48 - dard WHSV- The relative activity may then be calculated by dividing the hypothetical reciprocal WHSV by the reciprocal standard WHSV, which is 1/16, or .0625. The result is relative activity expressed in terms of a decimal fraction, which may then be multiplied by 100 to convert to percent relative activity. In applying the results of this deter¬ mination, a relative activity of 0-5, or 50%, means that it would take twice the amount of the operating catalyst to give the same conversion as the standard catalyst, i.e., the production catalyst_is 50% as active as the reference catalys Relative activity at a constant level of conversion is also equal to the ratio of the Weight Hourly Space Velocity (WHSV) of an operational r "test" catalyst divided by the WHSV of a standard catalyst selected for its level of con¬ version at MAT conditions. To simplify the calculation of relative activity for different test catalysts against the same standard catalyst, a MAT conversion versus relative activity curve may be developed. One such curve utilizing a standard catalyst of 75 volume percent conversion to repre¬ sent 100 percent relative activity is shown in Fig. 1. - 49 - The catalyst may be introduced into the process in its vir¬ gin form or, as previously indicated, in other than virgin form; e.g. one may use equilibrium catalyst withdrawn from another unit, .such as catalyst that has been employed in the cracking ofa different feed. Whether characterized on the basis of MAT conversion activity or relative acti- - vity, the preferred catalysts may be described on the basis of their activity "as introduced" into the process of the present invention, or on the basis of their "as withdrawn" or equilibrium activity in the process of the present invention, or on both of these bases. A preferred ac¬ tivity level of virgin and non-virgin catalyst "as intro¬ duced" into the process of the present invention is at least about 60% by MAT conversion, and preferably at least about 20%, more preferably at least about 40% and still more preferably at least about 60% in terms of relative activity. However, it will be appreciated that, parti¬ cularly in the case of non-virgin catalysts supplied at high addition rates, lower activity levels may be accep¬ table- An acceptable "as withdrawn" or equilibrium ac¬ tivity level of catalyst which has been used in the process of the present invention is at least about 20% or more, but about 40% or more and preferably about 60% or more are pre¬ ferred values on a relative activity basis, and an activity level of 60% or more on a MAT conversion basis is also con¬ templated. More preferably, it is desired to employ a catalyst which will, under the conditions of use in the unit, establish an equilibriu activity at or above the in¬ dicated level. The catalyst activities are determined with catalyst having less than 0.01 coke, e.g. regenerated catalyst- One may employ any hydrocarbon cracking catalyst having the above indicated conversion capabilities. A particular¬ ly preferred class of catalysts includes those which have - 50 - pore structures into which molecules of feed material may enter for adsorption and/or for contact with active cataly¬ tic sites within or adjacent the pores. Various types of catalysts are available within this classification, includ¬ ing for example the layered silicates, e.g. smectites. Although the most widely available catalysts within this classification are the well-known zeolite-containing catalysts, non-zeolite catalysts are also contemplated. The preferred zeolite-containing catalysts may include any zeolite, whether natural, semi-synthetic or synthetic, alone or in admixture with other materials which do not significantly impair the suitability of the catalyst, pro¬ vided the resultant catalyst has the activity and pore structure referred to above. For example, if the virgin catalyst is a mixture, it may include the zeolite, compon¬ ent associated with or dispersed in a porous refractory inorganic oxide carrier, in such case the catalyst may for example contain about 1% to about 60%, more preferably about 15 to about 50%, and most typically about 20 to about 45% by weight, based on the total weight of catalyst (water free basis) of the zeolite, the balance of the catalyst being the porous refractory inorganic oxide alone or in combination with any of the known adjuvants for promoting or suppressing various desired and undesired reactions. For a general explanation of the genus of zeolite, mole¬ cular sieve catalysts useful in the invention, attention is drawn to the disclosures of the articles entitled "Refinery Catalysts Are a Fluid Business" and "Making Cat Crackers Work On Varied Diet", appearing respectively in the July 26, 1973 and September 13, 1978 issues of Chemical Week magazine. The descriptions of the aforementioned publications are incorporated herein bv reference. - 51 For the most part, the zeolite components of the zeolite- containing catalysts will be those which are known to be useful in FCC cracking processes. In general, these are crystalline aluminosilicates, typically made up of tetra coordinated aluminum atoms associated through oxygen atoms with adjacent silicon atoms in the crystal structure. However, the term "zeolite" as used in this disclosure contemplates not -only aluminosilicates, but also substances in which the alumii. m has been partly or wholly replaced, such as for instance by gallium and/or other metal atoms, and further includes substances in which all or part of the silicon has been replaced, such as for instance by germanium. Titanium and zirconium substitution may also be practiced. Most zeolites are prepared or occur naturally i .the sodium form, so that sodium cations are associated with the electro¬ negative sites in the crystal structure. The sodium cations tend to make zeolites inactive and much less stable when exposed to hydrocarbon conversion conditions, particul- larly high temperatures. Accordingly, the zeolite may be ion exchanged, and where the zeolite is a component of a catalyst composition, such ion exchanging may occur before or after incorporation of the zeolite as a component of the composi-cion. Suitable cations for replacement of sodium in the zeolite crystal structure include ammonium (decomposable to hydrogen), hydrogen, rare earth metals, alkaline earth metals, etc. Various suitable ion- exchange procedures and cations which may be exchanged into the zeolite crystal structure are well known to those skilled in the art. Examples of the naturally occurring crystalline alu ino- silicate zeolites which may be used as or included in the catalyst for the present invention are faujasite, - 52 - mordenite, clinoptilote, chabazite, analcite, crionite, as well as levynite, dachiardite, paulingite, noselite, fer iorite, heulandite, scolccite, stibite, harmotome, phillipsite, brewsterite, flarite, datolite, gmelinite, caumnite, leucite, lazurite, scaplite, mesolite, ptolite, nephline, matrolite, offretite and sodalite. Examples of the synthetic crystalline aluminosilicate zeolites which are useful as or in the catalyst for car¬ rying out the present invention are Zeolite X, U.S. Patent No. 2,882,244; Zeolite Y, U'.S. Patent No. 3,130,007; and Zeolite A, U.S. Patent No. 2,882,243; as well as Zeolite B, U.S. Patent No. 3,008,803; Zeolite D, Canada Patent No. 661,981; Zeolite E, Canada Patent No. 614,495; Zeolite F, U.S. Patent No. 2,996,358; Zeolite H, U.S. Patent No. 3,010,789; Zeolite J. U.S. Patent No. 3,011,869; Zeolite L, Belgian Patent No. 575,177; Zeolite M, U.S. Patent No. 2,995,423; Zeolite O, U.S. Patent No. 3,140,252; Zeolite Q, U.S. Patent NO. 2,991,151; Zeolite S, U.S. Patent No. 3,054,657; Zeolite T, U.S. Patent No. 2,950,952; Zeolite W, U.S. Patent No. 3,012,853; Zeolite Z, Canada Patent No. 614,495; and Zeolite Omega, Canada Patent No. 817,915. Also, ZK-4HJ, alpha beta and ZSM-type zeolites are useful. Moreover, the zeolites described in U.S. Patent Nos. 3,140,249; 3,140,253; 3,944,482; and 4,137,151 are also useful, the disclosures of said patents being incorporated herein by reference. The crystalline aluminosilicate zeolites having a fauja— site-type crystal structure are particularly preferred for use in the present invention. This includes particularly natural faujasite and Zeolite X and Zeolite Y. The crystalline aluminosilicate zeolites, such as synthetic faujasite, will under normal conditions crystallize as OM - 53 - regularly shaped, discrete particles of about one to about ten microns in size, and, accordingly, this is the size range frequently found in commerical catalysts which can be used in the invention. Preferably, the particle size of the zeolites is from about 0.1 to about 10 microns and more preferably is from about 0-1 to about 2 microns or less. For example, zeolites prepared in situ from calcined kaolin may be characterized by even smaller crystallites. Crystal- line zeolites exhibit both an interior and an exterior surface area, the latter being defined as "portal" surface area, with the largest portion of the total surface area being internal. By portal surface area, we refer to the outer surface of the zeolite crystal through which reactants are considered to pass in order to convert to lower boiling products. Blockages of the internal channels by, for ex¬ ample, coke formation, blockages of entrance to the in¬ ternal channels by deposition of coke in the portal surface area, and contamination by metals poisoning, will greatly reduce the total zeolite surface area. Therefore, to mini¬ mize the effect of contamination and pore blockage, crys¬ tals larger than the normal size cited above are preferably not used in the catalysts of this invention- Commercial zeolite-containing catalysts are available with carriers containing a variety of metal oxides and combina¬ tion thereof, include for example silica, alumina, mag¬ nesia, and mixtures thereof and mixtures of such oxides with clays as e.g. described in U.S. Patent No. 3,034,948. One may for example select any of the zeolite-containing molecular sieve fluid cracking catalysts which are suitable for production of gasoline from vacuum gas oils. However, certain advantages may be attained by judicious selection of catalysts havingmarked resistance to metals. A metal resistant zeolite catalyst is, for instance, described in U.S. Patent Mo. 3,944,482, in which the catalyst contains OM - 54 - 1-40 weight percent of a rare earth-exchanged zeolite, the balance being a refractory metal oxide having specified pore volume and size distribution. Other catalysts de¬ scribed as "metals-tolerant" are described in the above mentioned Cimbala, et al. , article. In general, it is preferred to employ catalysts having an overall particle size in the range of about 5 to about 160, more preferably about 40 to about 120, and most preferably about 40 to about 80 microns. For example, a useful catalyst may have a skeletal density of about 150 pounds per cubic foot and an average particle size of about 60-70 microns, with less than 10% of the particles hav¬ ing a size less than about 40 microns and less than 80% having a size less than about 50-60 microns. Although a wide variety of other catalysts, including both zeolite-containing and non-zeolite-containing may be employed in the practice of the invention the following are examples of commercially available catalysts which may be employed in practicing the invention: TABLE 2 Specific Weiqht Percent Surface Zeolite m 2 /g Content A1 2 0 3 Si0 2 Na 2 0 Fe 2 0 τio 2 AGZ-290 300 11-0 29.5 59.0 0.40 0.11 0.59 GRZ-1 162 14.0 23.4 69.0 0.10 " 0.4 0.9 CCZ-220 129 11-0 34.6 60.0 0.60 0.57 1.9 Super DX 155 13.0 31.0 65.0 0.80 0.57 1.6 F-37 240 10.0 44.0 50.0 0.80 0.70 1.6 FOX-90 240 8.0 44.0 52.0 0.65 0.65 1.1 HFZ 20 310 20.0 59.0 40.0 0.47 0.54 2.75 HEZ 55 210 19.0 59-0 35-2 0.60 0.60 2.5 f OM - 55 - The AGZ-290, GRZ-1, CCZ-220 and Super DX catalysts referred to above are products of W. R. Grace and Co. F-87 and FOC-90 are products of Filtrol, while HFZ-20 and HEZ-55 are products of Engelhard/Houdr . The above are properties of virgin catalyst and, except in the case of zeolite content, are adjusted to a water free basis, i.e. based on material ignited at 1750°F. The zeolite content is derived by compari¬ son of the X-ray intensities of a catalyst sample and of a standard material composed of high purity sodium Y zeolite in accordance with draft #6, dated January 9, 1978, of proposed ASTM Standard Method entitled "Determination of t e ^ Faujasite Content of a Catalyst". Among the above mentioned commercially available catalysts, the Super D family and especially a catalyst designated GRZ-1 are particularly preferred. For example, Super DX has given particularly good results with Arabian light crude. The GRZ-1, although substantially more expensive than the Super DX at present, appears somewhat more metals- tolerant. Although not yet commercially available, it is believed that the best catalysts for carrying out the present inven¬ tion are those which are characterized by matrices with feeder pores having large minimum diameters and large mouths to facilitate diffusion of high molecular weight molecules through the matrix to the portal surface area of molecular sieve particles within the matrix. Such matrices prefera¬ bly also have a relatively large pore volume in order to soak up unvaporized portions of the carbo-metallic oil feed- Thus significant numbers of liquid hydrocarbon mole¬ cules can diffuse to active catalytic sites both in the matrix and in sieve particles on the surface of the matrix. In general it is preferred to employ catalysts having a total pore volume greater than 0.2 cc/gm, preferably at least 0.4 cc/gm, more preferably at least 0.6 cc/gm and - RE OMP - 56 - most preferably in the range of 0.7 to 1.0 cc/gm, and with matrices wherein at least 0.1 cc/gm, and prefer bly at least 0.2 cc/gm, of said total pore volume is comprised of feeder pores having diameters in the range of about 400 to about 6000 angstrom units, more preferably in the range of about 1000 to about 6000 angstrom units. These catalysts and the method for making the same are described more fully in copending international application Serial No. PCT/US81/00492 filed in the U.S. Receiving Office on April 10, 1981, in the names of Ashland Oil, Inc., et al., and entitled "Large Pore Catalysts for Heavy Hydrocarbon Conversion", the entire disclosure of said application being incorporated herein by reference. Additives may be introduced into the riser, the regenerator or other conversion system components to passivate the non-selec¬ tive catalytic activity of heavy metals deposited on the con¬ version catalyst. Preferred additives for practicing the pres ent invention include those disclosed in U.S. Patent Applica¬ tion Serial No. , filed simultaneously herewith in th name of William P. Hettinger, Jr., and entitled PASSIVATING HEAVY METALS IN CARBO-METALLIC OIL CONVERSION, the entire dis¬ closure of said U.S. application being incorporated herein by reference. Catalysts for carrying out the present invention may also employ other metal additives for controlling the adverse effects of vanadium as described in PCT International Applica¬ tion Serial No. PCT/US81/00356 filed in the U.S. Receiving Office on March 19, 1981, in the names of Ashland Oil, Inc., et al., and entitled "Immobilization of Vanadia Deposited on Catalytic Materials During Carbo-Metallic Oil Conversion". The manner in which these other metal additives are believed to interact with vanadium is set forth in said PCT internationa application, the entire disclosure fo which is incorporated herein by reference. - 57 - A particularly preferred catalyst also includes vanadium traps as disclosed in U.S. Patent Application Serial No. 252,967 filed April 10, 1981, in the names of William P. Hettinger, Jr.,. et al., and entitled "Trapping of Metals Deposited on Catalytic Materials During Carbo-Metallic Oil Conversion". It is also preferred to control the valence state of vanadium accumulations on the catalyst during regeneration as disclosed in the U.S. Patent Application - entitled "Immobilization of Vanadium Deposited on Catalytic Materials During Carbo-Metallic Oil Conversion" filed in the names of William P. Hettinger, Jr., et al. , on April 20, 1981, as well as the continuation-in-part of the same ap¬ plication subsequently filed on April 28, 1981. The entire disclosures of said U.S. Patent Applications are incorporated herein by reference. OR OMPI - 58 - It is considered an advantage that the process of the present invention can be conducted in the substantial absence of tin and/or antimony or at least in the pres¬ ence of a catalyst which is substantially free of either or both of these metals. The process of the present invention may be operated with the above- described carbo-metallic oil, catalyst ana water as sub¬ stantially the sole materials charged to the reaction zone. The charging of additional materials is not excluded. The charg¬ ing of recycled oil to the reaction zone has already been mentioned. As described in greater detail below, still other materials fulfilling a variety of functions may also be charged. In such case, the carbo-metallic oil and catalyst usually represent the major proportion by weight of the total of all materials charged to the reaction zone. Certain of the additional materials which may be used per¬ form functions which offer significant advantages over the process as performed with only the carbo-metallic oil and catalyst. Among these functions are: controlling the effects of heavy metals and other catalyst contaminants; enhancing catalyst activity; absorbing excess heat in the catalyst as received from the regenerator; disposal of pollutants or conversion thereof to a form or forms in -ØRI OM - 59 - which they may be more readily separated from products and/or disposed of; controlling catalyst temperature; diluting the carbo-metallic oil vapors to reduce their partial pressure and increase the yield of desired pro¬ ducts; adjusting feed/catalyst contact time; donation of hydrogen to a hydrogen deficient carbo-metallic oil feed- - stock for example as disclosed in copending application Serial No. 246,791, entitled "Use of Naphtha in Carbo- Metallic Oil Conversion", filed in the name of George D. Myers on March 23, 1981, which application is incorpor¬ ated herein by reference; assisting in the dispersion of the feed; and possibly also distillation of products. Certain of the metals in the heavy metals accumulation on . the catalyst are more active in promoting undesired re¬ actions when they are in the form of elemental metal, than they are when in the oxidized form produced by contact with oxygen in the catalyst regenerator. However, the time of contact between catalyst and vapors of feed and product in past conventional catalytic cracking was suf¬ ficient so that hydrogen released in the cracking reac¬ tion was able to reconvert a significant portion of the less harmful oxides back to the more harmful elemental heavy metals. One can take advantage of this situation through the introduction of additional materials which are in gaseous (including vaporous) form in the reaction zone in admixture with the catalyst and vapors of feed and products. The increased volume of material in the reaction zone resulting from the presence of such addi¬ tional materials tend to increase the velocity of flow through the reaction zone with a corresponding decrease in the residence time of the catalyst and oxidized heavy -ø OπMPI - 60 - metals borne thereby. Because of this reduced residence time, there is less opportunity for reduction of the oxi¬ dized heavy metals to elemental form and therefore less of the harmful elemental metals are available for con¬ tacting the feed and products. Added materials may be introduced into the process in any suitable fashion, some examples of which follow. For in¬ stance, they may be admixed with the carbo-metallic oil feedstock prior to contact of the latter with the catalyst. Alternatively, the added materials may, if desired, be admixed with the catalyst prior to contact of the latter with the feedstock. Separate portions of the added ma¬ terials may be separately admixed with both catalyst and carbo-metallic oil. Moreover, the feedstock, catalyst and additional materials may, if desired, be brought to¬ gether substantially simultaneously. A portion of the added materials may be mixed with catalyst and/or carbo- metallic oil in any of the above described ways, while ad¬ ditional portions are subsequently brought into admixture. For example, a portion of the added materials may be added to the carbo-metallic oil and/or to the catalyst before they reach the reaction zone, while another portion of the added materials is introduced directly into- the re¬ action zone. The added materials may be introduced at a plurality of spaced locations in the reaction zone or along the length thereof, if elongated. The amount of additional materials which may be present in the feed, catalyst or reaction zone for carrying out the above functions, and others, may be varied as desired; but said amount will preferably be sufficient to substantially heat balance the process- These materials may for example be introduced into the reaction zone in a weight ratio rela¬ tive to feed of up to about 0.4, preferably in the range of about 0.02 to about 0.4, more Or ferably about 0.03 - 61 - to about 0.3 and most preferably about 0.05 to about 0.25. For example, many or all of the above desirable functions may be attained by introducing Ξ-O to the reaction zone in the form of steam or of liquid water or a combination thereof in a weight ratio relative to feed in the range of about 0.04 or more, or more preferably about 0.05 to about 0.1 or more. The water used for these purposes may or may not contain one or more water soluble additives. Without wishing to be bound by any theory, it appears that the use of H-0 tends to inhibit reduction of catalyst-borne oxides, sulfites and sulfides to the free metallic form which is believed to promote condensation-dehydrogenation with consequent promotion of coke and hydrogen yield and accompanying loss of product. Moreover, Ξ-0 may also, to some extent, reduce deposition of metals onto the cata¬ lyst surface. There may also be some tendency to desorb nitrogen-containing and other heavy contaminant-containing molecules from the surface of the catalyst particles, or at least some tendency to inhibit their absorption by the catalyst. It is also believed that added H_0 tends to increase the acidity of the catalyst by Bronsted acid forma¬ tion which in turn enhances the activity of the catalyst. Assuming the H-0 as supplied is cooler than the regenerated catalyst and/or the temperature of the reaction zone, the sensible heat involved in raising the temperature of the H_0 upon contacting the catalyst in the reaction zone or elsewhere can absorb excess heat from the catalyst- Where the H-0 is or includes recycled water that contains for example about 500 to about 5000 ppm of H 2 S dissolved there¬ in, a number of additional advantages may accrue. The ecologically unattractive H_S need not be vented to the atmosphere, the recycled water does not require further treatment to remove K_S and the Ξ_S may be of assistance in reducing coking of the catalyst, by passivation of the - 62 - heavy metals, i.e. by conversion thereof to the sulfide form which has a lesser tendency than the free metals to en¬ hance coke and hydrogen production. In the reaction zone, the presence of H-0 can dilute the carbo-metallic oil vapors, thus reducing their partial pressure and tending to increase the yield of the desired products. It has been reported that H-0 is useful in combination with other ma¬ terials in generating hydrogen during cracking; thus it may be able to act as a iydrogen donor for hydrogen deficient carbo-metallic oil feedstocks. The H_0 may also serve cer¬ tain purely mechanical functions such as: assisting- in the atomizing or dispersion of the feed; competing with high molecular weight molecules for adsorption on the sur¬ face of the catalyst, thus interrupting coke formation; steam distillation of vaporizable product from unvaporized feed material; and disengagement of product from catalyst upon conclusion of the cracking reaction. It is particu¬ larly preferred to bring together H 2 0, catalyst and carbo- metallic oil substantially simultaneously. For example, one may admix H-0 and feedstock in an atomizing nozzle and immediately direct the resultant spray into contact with the catalyst at the downstream end of the reaction zone. The addition of steam to the reaction zone is frequently mentioned in the literature of fluid catalytic cracking. Addition of liquid water to the feed is discussed relative¬ ly infrequently, compared to the introduction of steam directly into the reaction zone- However, in accordance with the present invention it is particularly preferred that liquid water be brought into intimate admixture with the carbo-metallic oil in a weight ratio of about 0.04 to about 0.25 at or prior to the time of introduction of the oil into the reaction zone, whereby the water (e.g., in the form of liquid water or in the form of steam produced by vaporization of liquid water in contact with the oil) enters the reaction zone as part of the flow of feedstock - 63 - which enters such zone. Although not wishing to be bound by any theory, it is. believed that the foregoing is advan¬ tageous in promoting dispersion of the feedstock. Also, the heat of vaporization of the water, which heat is absorbed from the catalyst, from the feedstock, or from both, causes the water to be a more efficient heat sink than steam alone. Preferably the weight ratio of liquid water to feed is about 0.04 to about 0.2 more preferably about 0.05 to about 0.15. Of course, the liquid water may be introduced into the process in the above described manner or in other ways, and in either event the introduction of liquid water may be accompanied by the introduction of additional amounts of water as steam into the same or different portions of the reaction zone or into the catalyst and/or feedstock. For example, the amount of additional steam may be in a weight ratio relative to feed in the range of about 0.01 to about 0.25, with the weight ratio of total H-O (as steam and liquid water) to feedstock being about 0.3 or less. The charging weight ratio of liquid water relative to steam in such combined use of liquid water and steam may for example range from about 15 which is presently pre¬ ferred, to about 0-2. Such ratio may be maintained at a predetermined level within such range or varied as neces¬ sary or desired to adjust or maintain heat balance. Other materials may be added to the reaction zone to per¬ form one or more of the above described functions. For example, the dehydrogenation-condcnsation activity of heavy metals may be inhibited by introducing hydrogen sulfide gas into the reaction zone- Hydrogen may be made available for hydrogen deficient carbo-metallic oil feedstocks by introducing into the reaction zone either a conventional hydrogen donor diluent such as a heavy naphtha or relative¬ ly low molecular weight carbon-hydrocarbon fragment contri- - 64 - butors, including for example: light paraffins; low mole¬ cular weight alcohols and other compounds which permit or favor intermolecular hydrogen transfer; and compounds that chemically combine to generate hydrogen in the reaction zone such as lay reaction of carbon monoxide with water, or with alcohols, or with olefins, or with other materials or mixtures of the foregoing. All of the above .mentioned additional materials (including water), alone or ir- -conjunction with each other or in con¬ junction with other materials, such as nitrogen or other inert gases, light hydrocarbons, and others, may perform any of the above-described functions for which they are suitable, including without limitation, acting as diluents to reduce feed partial pressure and/or as heat sinks to absorb excess heat present in the catalyst as received from the regeneration step. The foregoing is a discussion of some of the functions which can be performed by materials other than catalyst and carbo-metallic oil feedstock in¬ troduced into the reaction zone, and it should be under¬ stood that other materials may be added or other functions performed without departing from the spirit of the invention- The invention may be practiced in a wide variety of appara¬ tus. However, the preferred apparatus includes means for rapidly vaporizing as much feed as possible and efficiently admixing feed and catalyst (although not necessarily in that order) , for causing the resultant mixture to flow as a dilute suspension in a progressive flow mode, and for separating the catalyst from cracked products and any un- cracked or only partially cracked feed at the end of a pre¬ determined residence time or times, it being preferred that all or at least a substantial portion of the product should be abruptly separated from at least a portion of the catalyst. - 65 - For example, the apparatus may include, along its elongated reaction chamber, one or more points for introduction of carbo-metallic feed, one or more points for introduction of catalyst, one or more points for introduction of addi¬ tional material, one or more points for withdrawal of products and one or more points for withdrawal of catalyst. The means for introducing feed, catalyst and other material may range from oper pipes to sophisticated jets or spray nozzles, it being preferred to use means capable of break¬ ing up the liquid feed into fine droplets. Preferably, the catalyst, liquid water (when used) and fresh feed are brought together in an apparatus similar to that disclosed in U.S. Patent Application Serial No. 969,601 of George D. Myers, et al., filed December 14, 1978, the entire disclos¬ ure of which is hereby incorporated herein by reference. Accordingly to a particularly preferred embodiment based on a suggestion which is understood to have emanated from Mr. Stephen M. Kovach, the liquid water and carbo-metallic oil, prior to their introduction into the riser, are caused to pass through a propeller, apertured disc, or any ap¬ propriate high shear agitating means for forming a "homoge¬ nized mixture" containing finely divided droplets of oil and/or water with oil and/or water present as a continuous phase. It is preferred that the reaction chamber, or at least the major portion thereof, be more nearly vertical than hori¬ zontal and have a length to diameter ratio of at least about 10, more preferably about 20 or 25 or more. Use of a vertical riser type reactor is preferred. If tubular, the reactor can be of uniform diameter throughout or may be provided with a continuous orstep-wise increase in diameter along the reaction path to maintain or vary the velocity along the flow path. - 66 - In general, the charging means (for catalyst and feed) and the reactor configuration are such as to provide a relatively high velocity of flow and dilute suspension of catalyst. For example, the vapor or catalyst velocity in the riser will-be usually at least about 25 and more typically at least about 35 feet per second. This velocity may range up to about 55 or about 75 feet or about 100 feet per second or higher. The vapor velocity at the top of the reactor may be higher than that at the bottom and may for example be about 80 feet per second at the top and about 40 feet per second at the bottom. The velocity capa¬ bilities of the reactor will in general be sufficient to prevent substantial build-up of catalyst bed in the bottom or other portions of the riser, whereby the catalyst load¬ ing in the riser can be maintained below about 4 or 5 pounds, as for example about 0.5 pounds, and below about 2 pounds, as for example 0.8 pounds, per cubic foot, respec¬ tively, at the upstream (e.g., bottom) and downstream (e.g., top) ends of the riser. The progressive flow mode involves, for example, flowing of catalyst, feed and products as a stream in a positively controlled and maintained direction established by the elongated nature of the reaction zone. This is not to suggest however that there must be strictly linear flow. As is well known, turbulent flow and "slippage" of cata¬ lyst may occur to some extent especially in certain ranges of vapor velocity and some catalyst loadings, although it has been reported advisable to employ sufficiently low catalyst loadings to restrict slippage and back-mixing. Most preferably the reactor is one which abruptly separates a substantial portion or all of the vaporized cracked pro¬ ducts from the catalyst at one or more points along the riser, and preferably separates substantially all of the vaporized cracked products frcm the catalyst at the down¬ stream end of the riser. A preferred type of reactor em- bodies ballistic separation of the catalyst and products; that is, catalyst is projected in a direction established by the riser tube, and is caused to continue its motion in the general direction so established, while the products, having lesser momentum, are caused to make an abrupt change of direction, resulting in an abrupt, substantially instan¬ taneous separation of product from catalyst. In a preferred embodiment referred to as a vented riser, the riser tube is provided with a substantially unobstructed discharge opening at its downstream end for discharge of catalyst. An exit port in the side of the tube adjacent the downstream end receives the products. The discharge opening communicates with a catalyst flow path which extends to the usual stripper - and regenerator, while the exit port communicates with a product flow ' path which is substantially or entirely separated from the catalyst flow path and leads to separation means for separating the products from the relatively small portion of catalyst, if any, which manages to gain ' entry to the product exit port. Examples of a ballistic separation apparatus and techniques as above described, are found in U.S. Patents 4,066,533 and 4,070,159 to Myers, et al., the disclosures of which patents are hereby incorporated herein by reference in their entireties. The mode of catalyst/product separation presently deemed best for practicing the present invention is disclosed in a U.S. Patent Application Serial No. , filed simultaneously herewith in the names of Paul W. Walters, Roger M. Benslay, and Dwight F. Barger, entitled CARBO-METALLIC OIL CONVERSION WITH 3ALLISTIC SEPARATION. The ballistic separation step preferably includes at least a partial reversal of direction by the product vapors upon discharge from the riser tube; that is, the product vapors make a turn or change of direction which exceeds 90° at the riser tube outlet. This may be accomplished for example by providing an annu¬ lar cup-like member surrounding the riser tube at its upper end, the ratio of cross-sectional area of the ann lus of the cup-like member relative to the cross-sectional area of the m - 68 - riser tube outlet being low i.e., less than 1 and preferably less than about 0.6. Preferably the lip of the cup is slightly upstream of, or below the downstream end or top of the riser tube, and the cup is preferably concentric with the riser tube. By means of a product vapor line com¬ municating with the interior of the cup but not the interior of the riser tube, having its inlet positioned within the cup interior in a direction upstream of the riser tube out¬ let, product vapors emanating from the riser tube and enter¬ ing the cup by reversal of direction are transported away from the cup to auxiliary catalyst and product separation equipment downstream of the cup. Such an arrangement can produce a high degree of completion of the separation of catalyst from product vapors at the vented riser tube out¬ let, so that the required amount of auxiliary catalyst sep¬ aration equipment such as cyclones is greatly reduced, with consequent large savings in capital investment and operat¬ ing cost. Preferred conditions for operation of the process are de¬ scribed below. Among these are feed, catalyst and reaction temperatures, reaction and feed pressures, residence time and levels of conversion, coke production and coke laydown on catalyst- In conventional FCC operations with VGO, the feedstock is customarily preheated, often to ' temperatures significantly higher than are required to make the feed sufficiently fluid for pumping and for introduction into the reactor. For example, preheat temperatures as high as about 700° or 800°F have been reported. But in our process as pres¬ ently practiced it is preferred to restrict preheating of the feed, so that the feed is capable of absorbing a larger amount of heat from the catalyst while the catalyst raises the feed to conversion temperature, at the same time mini¬ mizing utilization of external fuels to heat the feedstock. - 69 - Thus, where the nature of the feedstock permits, it may be fed at ambient temperature. Heavier stocks may be fed at preheat temperatures of up to about 600°F, typically about 200°F to about 500°F, but higher preheat temp¬ eratures are not necessarily excluded. The catalyst fed to the reactor may vary widely in temp¬ erature, forexample from about li00°to about 1600°F, more preferably about -1200° to about 1500°F and most pref- ^ erably about 1300° έb about 1400°F, with about 1325° to about 1375°F being considered optimum at present. As indicated previously, the conversion of the carbo- metallic oil to lower molecular weight products may be conducted at a temperature of about 900° to about 1400°F, measured at the reaction chamber outlet. The reaction temperature as measured at said outlet is more preferably maintained in the range of about 965° to about 1300°F, still more preferably about 975° to about 1200°F, and most preferably about 980° to about 1150°F. Depending upon the temperature selected and the properties of the feed, all of the feed may or may not vaporize in the riser. Although the pressure in the reactor may, as indicated above, range from about 10 to about 50 psia, preferred and more preferred pressure ranges are about 15 to about 45 and about 35 to about 45. n general,- the partial (or total) pressure of the feed may be in the range of about 3 to about 30, more preferably about 7 to about 25 and most preferably about 10 to about 17 psia. The feed partial pressure may be controlled or suppressed by the introduc¬ tion of gaseous (including vaporous) materials into the reactor, such as for instance the steam, water and other additional materials described above- The process " may for example be operated with the ratio of feed partial pressure relative to total pressure in the riser in the - 70 - range of about 0.2 to about 0.8, more typically about 0.3 to about 0.7 and still more typically about 0.4 to about 0.6, with the ratio of added gaseous material (which may include recycled gases and/or steam resulting from intro¬ duction of H-0 to the riser in the form of steam and/or liquid water) relative to ' -total pressure in the riser correspondingly ranging from about 0.8 to about 0.2, more- typically about Q.7 to about 0.3 and still more typically about 0.6 to about -.0.4. In the illustrative operations just described, the ratio of the partial pressure of the added gaseous material relative to the partial pressure of the feed may be in the range of about 0.25 to about 4.0, more typically about 0.4 to about 2.3 and still more typically about 0.7 to about 1.7. Although the residence time of feed and product vapors in the riser may be in the range of about 0.5 to about 10 seconds, as described above, preferred and more preferred values are about 0.5 to about 6 and about 1 to about 4 seconds, with about 1.5 to about 3.0 seconds currently being considered about optimum. For example, the process may be operated with a riser vapor residence time of about 2.5 seconds or less by introduction of copious amounts of gaseous materials into the riser, such amounts being suf¬ ficient to provide for example a partial pressure ratio of added gaseous materials relative to hydrocarbon feed of about 0-3 or mere. By way of further illustration, the process may be operated with said residence time being about 2 seconds or less, with the aforesaid ratio being in the range of about 1 to about 2. The combination of low feed partial pressure, very low residence time and ballistic separation of products from catalyst are con¬ sidered especially beneficial for the conversion cf carbo- metallic oils. Additional benefits may be obtained in the foregoing combination when there is a substantial partial " prossurf * - of added -gaseous material, esoeci.iliv H O - 71 - scribed above. Depending upon whether there is slippage between the cata¬ lyst and hydrocarbon vapors in the riser, the catalyst riser residence time may or may not be the same as that of the vapors. Thus, the ratio of average catalyst reac¬ tor residence time versus vapor reactor residence time, i.e., slippage, may be in the range of about 1 to about 5, more preferably about 1 to about 4 and most preferably about 1 to about 3, -with about 1 to about 2 currently be¬ ing considered optimum. In practice, there will usually be a small amount of slip¬ page, e.g., at least about 1.05 or 1.2. In an operating unit there may for example be a slippage of about 1.1 at the bottom of the riser and about 1.05 at the top. In certain types of known FCC units, there is a riser which discharges catalyst and product vapors together into an enlarged chamber, usually considered to be part of the reactor, in which the catalyst is disengaged from product and collected. Continued contact of catalyst, uncracked feed (if any) and cracked products in such enlarged chamber results in an overall catalyst feed contact time appreciably exceeding the riser tube residence times of the vapors and catalysts. When practicing the process , of the present in¬ vention with ballistic separation of catalyst and vapors at the downstream (e.g., upper) extremity of the riser, such as is taught in the above mentioned Myers, et al. , patents, the riser residence time and the catalyst contact time are substantially the same for a major portion of the feed and product vapors. It is consi d ered advantageous if the vapor riser residence time and vapor catalyst contact time are substantially the same for at least about 80%, more pref¬ erably at least about 90% and most preferably at least about 95% by volume of the total feed and product vapors - 72 - passing through the riser. By denying such vapors continued contact with catalyst in a catalyst disengagement and col¬ lection chamber one may avoid a tendency toward re-cracking and diminished selectivity- In general, the combination of catalyst to oil ratio, temp¬ eratures, pressures and residence times should be such as to effect a substantial conversion of the carbo-metallic oil feedstock. It is an advantage of the process that very - high levels of conversion can be attained in a single pass; for example the conversion may be in excess of 50% and may range to about 90% or higher. Preferably, the afore¬ mentioned conditions are maintained at levels sufficient to maintain conversion levels in the range of about 60 to about 90% and more preferably about 70 to about 85%. The foregoing conversion levels are calculated by sub¬ tracting from 100% the percentage obtained by dividing the liquid volume of fresh feed into 100 times the volume of liquid product boiling at and above 430°F (tbp, standard atmospheric pressure) . These substantial levels of conversion may and usually do result in relatively large yields of coke, such as for example about 4 to about 14% by weight based on fresh feed, more commonly about 6 to about 13% and most frequently about 10 to about 13%. The coke yield can more or less quantitatively eposit upon the catalyst. At contemplated catalyst to oil ratios, the resultant coke laydown may¬ be in excess of about 0.3, more commonly in excess of about 0.5 and very frequently in excess of about 1% of coke by weight, based on the weight of moisture free re¬ generated catalyst- Such coke laydown may range as high as about 2%, or about 3%, or even higher. In common with conventional FCC operations on VGO, the present process includes stripoin of spent catalyst afte - 73 - disengagement of the catalyst from product vapors- Persons skilled in the art are acquainted with appropriate strip¬ ping agents and conditions for stripping spent catalyst, but in some cases the present process may require some¬ what more severe conditions than are commonly employed. This may result, for example, from the use of a carbo- metallic oil having constituents which do not volatilize under the conditions prevailing in the reactor, which constituents deposit themselves at least in part on the ' catalyst. Such adsorbed, unvaporized material can be troublesome fromat least two standpoints. First, if the gases (including vapors) used to strip the catalyst can gain admission to a catalyst disengagement or collection chamber connected to the downstream end of the riser, and if there is an accumulation of catalyst in such chamber, vaporization of these unvaporized hydrocarbons in the stripper can be followed by adsorption on the bed of cata¬ lyst in the chamber. More particularly, as the catalyst in the stripper is stripped of adsorbed feed material, the resultant feed material vapors pass through the bed of catalyst accumulated in the catalyst collection and/or dis¬ engagement chamber and may deposit coke and/or condensed material on the catalyst in said bed- As the catalyst bearing such deposits moves from the bed and into the stripper and from thence to the regenerator, the condensed products can create a demand for more stripping capacity, while the coke can tend to increase regeneration temp¬ eratures and/or demand greater regeneration capacity- For the foregoing reasons, it is preferred to prevent or re¬ strict contact between stripping vapors and catalyst ac¬ cumulations in the catalyst disengagement or collection chamber. This may be done for example by preventing such accumulations from forming, e.g., with the exception of a quantity of catalyst which essentially drops out of circulation and may remain at the bottom of the disengage¬ ment and/or collection chamber, the catalyst that is in - 74 - circulation may be removed from said chamber promptly upon settling to the bottom of the chamber. Also, to minimize ' regeneration temperatures and demand for regeneration ca¬ pacity, it may be desirable to employ conditions of time, temperature and atmosphere in the stripper which are suf-- ficient to reduce potentially volatile hydrocarbon material borne by the stripped catalyst to about 10% or less by weight of the total carbon loading on the catalyst. Such stripping may for example include reheating of the cata- " * lyst, extensive stripping with steam, the use of gases hav¬ ing a temperature considered higher than normal for FCC/VGO operations, such as for instance flue gas from the regenera¬ tor, as well as other refinery stream gases such as hydro- treater off-gas (H-S containing) , hydrogen and others. For example, the stripper may be operated at a temperature of about 350°F using steam at a pressure of about 150 psig and a weight ratio of steam to catalyst of about 0.002 to about 0.003. On the other hand, the stripper may be operated at a temperature of about 1025°F or higher. Substantial conversion of carbo-metallic oils to lighter products in accordance with the invention tends to produce sufficiently large coke yields and coke laydown on cata¬ lyst to require some care in catalyst regeneration. In order to maintain adequate activity in zeolite and non- zeolite catalysts, it is desirable to regenerate the cata¬ lyst under conditions of time, temperature and atmosphere sufficient to reduce the percent by weight of carbon re¬ maining on the catalyst to about 0.25% or less, whether the catalyst bears a large heavy metals accumulation or not. Preferably this weight percentage is about 0.1% or less and more preferably about 0.05% or less, especially with zeo¬ lite catalysts. The amounts of coke which must therefore be burned off of the catalysts when processing carbo-metal¬ lic oils are usually substantially greater than would be the OMPI - 75 - case when cracking VGO. The term coke when used to describe the present invention, should be understood to include any residual unvaporized feed or cracking product, if any such material is present on the catalyst after stripping. Regeneration of catalyst, burning away of coke deposited on the catalyst during the conversion of the feed, may be performed at any suitable temperature in the range of about 1100° to about 1600°F, measured at the regenerator cata- ^_ lyst outlet. This 'emperature is preferably in the range of about 1200° to about 1500°F, more preferably about 1275° to about 1425°F and optimally about 1325°F to about 1375°F. The process has been operated, for example, with a flui¬ dized regenerator with the temperature of the catalyst dense phase in the range of about 1300° to about 1400°F. Regeneration is preferably conducted while maintaining the catalyst in one or more fluidized beds in one or more flui- dization chambers. Such fluidized bed operations are char¬ acterized, for instance, by one or more fluidized dense beds of ebulliating particles having a bed density of, for exam¬ ple, about 25 to about 50 pounds per cubic foot- Fluidiza- tion is maintained by passing gases, including combustion supporting gases, through the bed at a sufficient velocity to maintain the particles in a fluidized state but at a velocity which is sufficiently small to prevent substantial entrainment of particles in the ' gases. For example, the lineal velocity of the fluidizing gases may be in the range of about 0-2 to about 4 feet per second and preferably about 0.2 to about 3 feet per second. The average total resi¬ dence time of the particles in the one or more beds is sub¬ stantial, ranging for example from about 5 to about 30, more preferably about 5 to about 20 and still more preferably about 5 to about 10 minutes. From the foregoing, it may be readily seen that the fluidized bed regeneration of the present invention is readily distinσuishable from the - 76 - contact, low-density entrainment type regeneration which has been practiced in some FCC operations. When regenerating catalyst to very low levels of carbon on regenerated catalyst, e.g., about 0.1% or less or about 0.05% or less, based on the weight of regenerated catalyst, it is acceptable to burn off at least about the last 10% or at least about the last 5% by weight of coke (based on the total weight-of coke on the catalyst immediately prior to regeneration) in ~ contact with combustion producing gases containing excess oxygen. In this connection it is con¬ templated that some selected portion of the coke, ranging from all of the coke down to about the last 5 or 10% by weight, can be burned with excess oxygen. By excess oxy¬ gen is meant an amount in excess of the stoichiometric requirement for burning all .of the hydrogen to water, all of the carbon to carbon dioxide and all of the other com¬ bustible components, if any, which are present in the above- mentioned selected portion of the coke immediately prior to regeneration, to their highest stable state of.oxidation under the regenerator conditions. The gaseous products of combustion conducted in the presence of excess oxygen will normally include an appreciable amount of free oxygen. Such free oxygen, unless removed from the by-product gases or con¬ verted to some other form by a means or process other than regeneration, will normally manifest itself as free oxygen in the flue gas from the regenerator unit. In order to provide sufficient driving force to complete the combustion of the coke with excess oxygen, the amount of free oxygen will normally be not merely appreciable but substantial, i.e., there will be a concentration of at least about 2 mole percent of free oxygen in the total regeneration flue gas recovered from the entire, completed regeneration operation. While such technique is effective in attaining the desired low levels of carbon on regenerated catalyst, is has its limitations and difficulties as will become apparent from OMPI - 77 - Heat released by combustion of coke in the regenerator is absorbed by the catalyst and can be readily retained there¬ by until the regenerated catalyst is brought into contact with fresh feed. When processing carbo-metallic oils to the relatively high levels of conversion involved in the present invention, the amount of regenerator heat which is trans¬ mitted to fresh feed by way of recycling regenerated cata¬ lyst can substantially exceed the level of heat input which is appropriate in the riser for heating and vaporizing the feed and other materials, for supplying the endothermic heat of reaction for cracking, for making up the heat losses of the unit and so forth. Thus, in accordance with the in¬ vention, the amount of regenerator heat transmitted to fresh feed may be controlled, or restricted where necessary, within certain approximate ranges. The amount of heat so transmitted may for example be in the range of about 500 to about 1200, more particularly about 600 to about 900, and more particularly about 650 to about 850 BTUs per pound of fresh feed. The aforesaid ranges refer to the combined heat, in BTUs per pound of fresh feed, which is transmitted by the catalyst to the feed and reaction products (between the contacting of feed with the catalyst and the separation of product from catalyst) for supplying the heat of reaction (e.g. , for cracking) and the difference in enthalpy between the products and the fresh feed. Not included in the fore¬ going are the heat made available in the reactor by the ad¬ sorption of coke on the catalyst, nor the heat consumed by heating, vaporizing or reacting recycle streams and such added materials as water, steam naphtha and other hydrogen donors, flue gases and inert gases, or by radiation and other losses. One or a combination of techniques may be utilized in this invention for controlling or restricting the amount of regeneration heat transmitted via catalyst to fresh feed. ΓR - 78 - For example, one may add a combustion modifier to the crack¬ ing catalyst in order to reduce the temperature of combus¬ tion of coke to carbon dioxide and/or carbon monoxide in the regenerator. Moreover, one may remove heat from the catalyst through heat exchange means, including for example, heat exchangers (e.g., steam coils) built into the regenera¬ tor itself, whereby one may extract heat from the catalyst during regeneration. Heat exchangers can be built into cata¬ lyst transfer lines,_ such as for instance the catalyst re¬ turn line from the regenerator to the reactor, whereby heat may be removed from the catalyst after it is regenerated. The amount of heat imparted to the catalyst in the regen¬ erator may be restricted by reducing the amount of insula¬ tion on the regenerator to permit some heat loss to the surrounding atmosphere, especially if feeds of exceedingly high coking potential are planned for processing; in gen¬ eral, such loss of heat to the atmosphere is considered economically less desirable than certain of the other al¬ ternatives set forth herein. One may also inject cooling fluids into portions of the regenerator other than those oc¬ cupied by the dense bed, for example water and/or steam, whereby the amount of inert gas available in the regenerator for heat absorption and removal is increased. Another suitable and preferred technique for controlling or restricting the heat transmitted to fresh feed via recycled regenerated catalyst involves- maintaining a specified ratio between the carbon dioxide and carbon monoxide formed in the regenerator while such gases are in heat exchange con¬ tact or relationship with catalyst undergoing regeneration. In general, all or a major portion by weight of the coke present on the catalyst immediately prior to regeneration is removed in at least one combustion zone in which the afore¬ said ratio is controlled as described below. More particu¬ larly, a least the major portion more preferably at least about 65 and more preferably at least about 30% by weight - 79 - of the coke on the catalyst is removed in a combustion zone in which the molar ratio of CO_ to CO is maintained at a level substantially below 5, e.g., about 4 or less. Look¬ ing at the CO-/CO relationship from the inverse standpoint, it is preferred that the CO/CO- molar ratio should be at least about 0.25 and preferably at least about 0.3 and still more preferably about 1 or more or even 1.5 or more. While persons skilled in the art are aware of techniques for inhibiting the burning of CO to CO-, it has been suggested - that the mole ratio of CO:CO_ should be kept less than 0.2 when regenerating catalyst with large heavy metal accumula¬ tions resulting from the processing of carbo-metallic oils, in this connection see for example U.S. Patent 4,162,213 to Zrinscak, Sr., et al. In this invention, however, CO pro¬ duction is increased while catalyst is regenerated to about 0.1% carbon or less, and preferably to about 0.05% carbon or less. Moreover, according to a preferred method of carry¬ ing out the invention the sub-process of regeneration, as a whole, may be carried out to the above-mentioned low levels of carbon on regenerated catalyst with a deficiency of oxy¬ gen; more specifically, the total oxygen supplied to the one or more stages of regeneration can be and preferably is less than the stoichio etric amount which would be required to burn all hydrogen in the coke to H_0 and to burn all car¬ bon in the coke to CO-. If the coke includes other combusti¬ bles, the aforementioned stoichiometric amount can b'e ad¬ justed to include the amount of oxygen required to burn them. Still another particularly preferred technique for control¬ ling or restricting the regeneration heat imparted to fresh feed via recycled catalyst involves the diversion of a por¬ tion of the heat borne by recycled catalyst to added material introduced into the reactor, such as the water, steam, naphth other hydrogen donors, flue gases, inert gases, and other gaseous or vaporizable materials which may be introduced in¬ to the reactor. - 80 - The larger the amount of coke which must be burned from a given weight of catalyst, the greater the potential for ex¬ posing the catalyst to excessive temperatures. Many other¬ wise desirable and useful cracking catalysts are particularly susceptible to deactivation at high temperatures, and among these are quite a few of the costly molecular sieve or zeo¬ lite types of catalyst. The crystal structures of zeolites and the pore structures of the catalyst carriers generally are somewhat susceptible to thermal and/or hydrothermal de¬ gradation. The us<.-of such catalysts in catalytic conver¬ sion processes for carbo-metallic feeds creates a need for regeneration techniques which will not destroy the catalyst by exposure to highly severe temperatures and steaming. Such need can be met by a multi-stage regeneration process which includes conveying spent catalyst into a first re¬ generation zone and introducing oxidizing gas thereto. The amount of oxidizing gas that enters said first zone and the concentration of oxygen or oxygen bearing gas therein are sufficient for only partially effecting the desired conver¬ sion of coke on the catalyst to carbon oxide gases. The partially regenerated catalyst is then removed from the first regeneration zone and is conveyed to a second regenera¬ tion zone. Oxidizing gas is introduced into the second re¬ generation zone to provide a higher concentration of oxygen or oxygen-containing gas than in the first zone, to complete the removal of carbon to the desired level. The regenera¬ ted catalyst may then be removed from the second zone and recycled to the reactor for contact with fresh feed. An example of such multi-stage regeneration process is described in U.S. Patent Application Serial No. 969,602 of George D- Myers, et al- , filed December 14, 1978, the entire disclosure of which is hereby incorporated herein by reference. Another example may be found in U.S. Patent 2,938,739. Multi-stage regeneration offers the possibility of combin¬ ing oxygen deficient regeneration with the control of the OMPI - 81 - CO:CO- molar ratio- Thus, about 50% or more, more prefer¬ ably about 65% to about 95%, and more preferably about 80% to about 95% by weight of the coke on the catalyst immedi¬ ately prior to. regeneration may be removed in one or more stages of regeneration in which the molar ratio of CO:C0 2 is controlled in the manner described above. In combination with the foregoing, the last 5% or more, or 10% or more by weight of the coke originally present, up to the entire amount of coke remaining after the preceding stage or stages, can be removed in a subsequent stage of regeneration in which more oxygen is present. Such process is susceptible of operation in such a manner that the total flue gas recovered from the entire, completed regeneration operation contains little or no excess oxygen, i.e., on the order of about 0.2 mole percent or less, or as low as about 0.1 mole percent or less, which is substantially less than the 2 mole percent which has been suggested elsewhere. Thus, multi-stage re¬ generation is particularly beneficial in that it provides another convenient technique for restricting regeneration heat transmitted to fresh feed via regenerated catalyst and/or reducing the potential for thermal deactivation, while simul¬ taneously affording an opportunity to reduce the carbon level on regenerated catalyst to those very low percentages (e.g., about 0.1% or less) which particularly enhance cata¬ lyst activity. For example, a two-stage regeneration process may be carried out with the first stage burning about 80% of the coke at a bed temperature of about 1300°F to produce CO and CO- in a molar ratio of CO/CO- of about 1 and the second stage burning about 20% of the coke at a bed temperature of about 1350°F to produce substantially all CO- mixed with free oxygen. Use of the gases from the second stage as combus¬ tion supporting gases for the first stage, along with ad¬ ditional air introduced into the first stage bed, results in an overall CO to C0 2 ratio of about 0-6, with a catalyst residence time of about 5 to 15 minutes total in the two - 82 - zones- Moreover, where the regeneration conditions are subst tially more severe in the first zone than in the second zone (e.g., higher zone or localized temperatures and/or more severe steaming conditions), that part of the regeneration sequence which involves the most severe con¬ ditions is performed while there is still an appreciable amount of coke on the catalyst. Such operation may provide some protection of the catalyst from the more severe condi¬ tions. A particularly preferred embodiment of the invention is two-stage fluidized regeneration at a maximum tempera¬ ture of about 1400 F with a reduced temperature of at least about 10 or 20°F in the dense phase of the first stage as compared to the dense phase of the second stage, and with re¬ duction of carbon on catalyst to about 0.05% or less or even about 0.025% or less by weight in the second zone. In fact, catalyst can readily be regenerated to carbon levels as low as 0.01% by this technique, even though the carbon on catalyst prior to regeneration is as much as about 1%. In most circumstances, it will be important to insure that no adsorbed oxygen containing gases are carried into the riser by recycled catalyst. Thus, whenever such action is considered necessary, the catalyst discharged from the re¬ generator may be stripped with appropriate stripping gases to remove oxygen containing gases. Such stripping may for in¬ stance be conducted at relatively high temperatures, for example about 1350° to about 1370°F, using steam, nitrogen or other inert gas as the stripping gas(es). The use of nitrogen and other inert gases is beneficial from the stand¬ point of avoiding a tendency toward hydrcthcr al catalyst deactivation which may result from the use of stea . The following comments and discussion relating to metals management, carbon management and heat management may be of assistance in obtaining best results when operating the in¬ vention. Since these remarks are for the most part directed - 83 - to what is considered the best mode of operation, it should be apparent that the invention is not limited to the particu¬ lar modes of operation discussed below. Moreover, since cer¬ tain of these comments are necessarily based on theoretical considerations, there is no intention to be bound by any such theory, whether expressed herein or implicit in the opera¬ ting suggestions set forth hereinafter. Although discussod separately below, it is readily apparent that metals manage:.snt, carbon management and heat manage¬ ment are interrelated and interdependent subjects both in theory and practice. While co.ke yield and coke laydown on catalyst are primarily the result of the relatively large quantities of coke precursors found in carbo-metallic oils, the production of coke is exacerbated by high metals accumu¬ lations, which can also significantly affect catalyst per¬ formance. Moreover, the degree of success experienced in metal management and carbon management will have a direct influence on the extent to which heat management is neces¬ sary. Moreover, some of the steps taken in support of metals management have proved very helpful in respect to carbon and heat managment. As noted previously the presence of a large heavy metals ac¬ cumulation on the catalyst tends to aggravate the problem of dehydrogenation and aromatic condensation, resulting in in¬ creased production of gases and coke for a feedstock of a given Ramsbcttom carbon value- The introduction of substan¬ tial quantities of H_0 into the reactor, either in the form of steam or liquid water, appears highly beneficial from the standpoint of promoting steam reforming reactions- This is of assistance in maintaining the desired selectivity. Also, a unit design in which system components and residence times are selected to reduce the ratio of catalvst reactor - 84 - residence time relative to catalyst regenerator residence time will tend to reduce the ratio of the times during which the catalyst is respectively under reduction conditions and oxidation conditions. This too can assist in maintaining desired levels of selectivity. Whether the metals content of the catalyst is being managed successfully may be observed by monitoring the total hydro¬ gen plus methane produced in the- reactor and/or the ratio of hydrogen to methane thus produced. In general, it is considered that the hydrogen to methane mole ratio should be less than about 1 and preferably about 0.6 or less, with about 0.4 or less being considered about optimum. In actual practice the hydrogen to methane ratio may range from about 0.5 to about 1.5 and average about 0.8 to about 1. Careful carbon management can improve both selectivity (the ability to maximize production of valuable products) , and heat productivity. In general, the techniques of metals con¬ trol described above are also of assistance in carbon manage¬ ment. The usefulness of water addition in respect to carbon management has already been spelled out in considerable de¬ tail in that part of the specification which relates to ad¬ ded materials for introduction into the reaction zone. In general, those techniques which improve dispersion of the feed in the reaction zone should also prove helpful, these include for instance the use of fogging or misting devices to assist in dispersing the feed. Catalyst to oil ratio is also a factor in heat management. In. common with prior FCC practice on VGO, the reactor temp¬ erature may be controlled in the practice of the present in¬ vention by respectively increasing or decreasing the flow of hot regenerated catalyst to the reactor in response to de¬ creases and increases in reactor temperature, typically the - 85 - outlet temperature in the case of a riser type reactor- Where the automatic controller for catalyst introduction is set to maintain an excessive catalyst to oil ratio, one can expect unnecessarily large rates of carbon production and heat release, relative to the weight of fresh feed charged to the reaction zone- Relatively high reactor temperatures are also beneficial from the standpoint of carbon management. Such higher temp- eratures foster more, complete vaporization of feed and dis¬ engagement of product from catalyst. Carbon management can also be facilitated by suitable re¬ striction of the total pressure in the reactor and the par¬ tial pressure of the feed. In general, at a given level of conversion, relatively small decreases in the aforementioned pressures can substantially reduce coke production. This may be due to the fact that restricting total pressure tends to enhance vaporization of high boiling components of the feed, encourage cracking and facilitate disengagement of both un¬ converted feed and higher boiling cracked products from the catalyst. It may be of assistance in this regard to restrict the pressure drop of equipment downstream of and in communi¬ cation with the reactor. But if it is desired or necessary to operate the system at higher total pressure, such as for instance because of operating limitations (e.g-, pressure drop in downstream equipment) the above described benefits may be obtained by restricting the feed partial pressure. Suitable ranges for total reactor pressure and feed partial pressure have been set forth above, and in general it is desirable to attempt to minimize the pressure within these ranges. The abrupt separation of catalyst from product vapors and unconverted feed (if any) is also of great assistance. It is for this reasons that the so-called vented riser apparatus and technique disclosed in U.S. Patents 4,070,159 and - 86 - 4,066,533 to George D. Myers, et al., is the preferred type o apparatus for conducting this process. . For similar reasons, it is beneficial to reduce insofar as possible the elapsed time between separation of catalyst from product vapors and the commencement of stripping. The vented riser and prompt stripping tend to reduce the opportunity for coking of un¬ converted feed and higher boiling cracked products adsorbed on the catalyst. A particularly desirable mode of operation from the stand¬ point of carbon management is to operate the process in the vented riser using a hydrogen donor if necessary, while main¬ taining the feed partial pressure and total reactor pressure as low as possible, and incorporating relatively large amounts of water, steam and if desired, other diluents, which provide the numerous benefits discussed in greater detail above. Moreover, when liquid water, steam, hydrogen donors, hydrogen and other gaseous or vaporizable materials are fed to the reaction zone, the feeding of these materials pro¬ vides an opportunity for exercising additional control over catalyst to oil ratio. Thus, for example, the practice of - increasing or decreasing the catalyst to oil ratio for a given amount of decrease or increase in reactor temperature may be reduced or eliminated by substituting either appro¬ priate reduction or increase in the charging ratios of the water, steam and other gaseous or vaporizable material, or an appropriate reduction or increase in the ratio of water to steam and/or other gaseous materials introduced into the reaction zone. Heat management includes measures taken to control the amount of heat released in various parts of the process and/or for dealing successfully with such heat as may be released. Un¬ like conventional FCC practic using VGO, wherein it is usu¬ ally a problem to generate sufficient heat during regenera- - 87 - tion to heat balance the reactor, the processing of carbo- metallic oils generally produces so much heat as to require careful management thereof. Heat management can be facilitated by various techniques as¬ sociated with the materials introduced into the reactor. Thus, heat absorption by feed can be maximized by minimum preheating of feed, it being necessary only that the feed temperature be h5.gh enough so that it is sufficiently fluid for successful punn ng and dispersion in the reactor. When the catalyst is maintained in a highly active state with the suppression of coking (metals control) , so as to achieve higher conversion, the resultant higher conversion and greater selectivity can increase the heat absorption of the reaction. In general, higher reactor temperatures promote catalyst conversion activity in the face of more refractory and higher boiling constituents with high coking potentials. While the " rate of catalyst deactivation may thus be increased, the higher temperature of operation tends to offset this loss in activity. Higher temperatures in the reactor also contribute to enhancement of octane number, thus offset¬ ting the octane depressant effect of high carbon la own. Other techniques for absorbing heat have also been discussed above in connection with the introduction of water, steam, and other gaseous or vaporizable materials into the reactor. As noted above, the invention can be practiced in the above- described mode and in many others. An illustrative, nor.- « limiting example is described by the accompanying schematic diagrams in the figure and by the description of this figure which follows. Referring in detail to Fig.2 of the drawings, petroleum feedstock i s introduced into the lever end of riser reactor 2 chr ugh inlet line 1, at which point it is mixed with hot regenerated catalyst coming from regenerator 9 through lines 26, 5, 65 and 66 and a stripping vessel 14 and a reducing vessel 60. * * - 88 - The feedstock is catalytically cracked in passing up riser 2 and the product vapors are ballistically separated from catalyst particles in vessel 3. Riser 2 is of the vented type having an open upper end 40 surrounded by a cup-like member 42 which preferably stops just below the upper end 40 of the riser so that the lip of the cup is slightly up¬ stream of the open riser tube as shown in Fig. 2. A pair of product vapor lines 44, 46 communicate with the interior of the cup so as to discharge product vapors entering the cup from the vapor space of vessel 3. The cup forms an annulus 47 around and concentric to the upper end of the riser tube- The transverse cross-sectional area of annulus 47 is pref¬ erably less than, more preferably about 60% or less of, the transverse cross-sectional area of riser tube 2. This structure causes product vapors to undergo a complete re¬ versal in their direction of flow after they are discharged from the riser tube but before they leave the vapor space of vessel 3. The product vapors then make a further turn or change in direction of about 90° as they enter product lines 44 and 46. The product vapors then enter cyclone separators 48, 50 having overhead conduits 52, 54, respectively, which convey the vapors to line 4 through a common header 56. The amount of particle carry over with this flow reversal struc¬ ture may be reduced by a factor of about 5 or more relative to carry over with the basic vented riser arrangement described in U.S. Patents 4,066,533 and 4,070,159- Due to this reduction in carry over, cyclone separators 48 ' and 50 may comprise only a single cyclone stage instead of having multiple stages as usually required to prevent excessive carry over of catalyst fines into the overhead vapor line in prior vented riser applications. ΓORE OMP - 89 - The catalyst, contaminated with coke, is removed from sep¬ arator vessel 3 and passed into stripper 19 through line 7. Stripped catalyst is introduced into bed 23 in upper zone 10 of regenerator 9 through line 36. The rate of flow of catalyst into .zone 10 is controlled by valve 8. Makeup catalyst, whether virgin or used, is introduced through lines 30 and 31 into solids feeder 33 and then through line 32. Oxidizing gas, such as air, is introduced into zone 10 through line 21. A portion of the coke on the catalyst is burned in zone 10 and the partially regenerated catalyst flows downwardly through conduit 18 into lower regeneration zone 25. An oxidizing gas, such as air, is introduced into regenera¬ tion zone 25 through line 11. The oxidizing gas flows through gas distribution plate 15 and thus into the bed 16 of catalyst particles. This mixture passes upwardly through the bed 16 of coke-contaminated catalyst particles, flui- dizing it as well as reacting with the coke, and passes through perforated plate 17 into the bed of catalyst parti¬ cles in zone 10. The perforations in the plate 17 are large enough so that the upwardly flowing gas readily passes therethrough into zone 10. During regeneration of the catalyst the pressure difference between the upper and lower.zones prevents cata¬ lyst particles from passing downwardly through the plate. Gases within the regenerator comprising combustion products, nitrogen and possibly additives for combustion control, such as steam and/or chlorine, are separated from suspended cata¬ lyst particles by a separator (not shown) and then pass out of the regenerator through line 24. Regenerated catalyst is removed from zone 25 through conduit 26 for return to riser 2 through the stripper 14, the rate of removal being controlled by valve 6. - 90 - A stripping gas such as steam is introduced into stripper 19 through line 20 to remove volatiles from the catalyst. The volatiles pass from the stripper through line 7 into vessel 3 and then out through line 4. Similarly a stripper gas, such as steam is introduced into stripper 14 through line 12 to remove absorbed nitrogen from the regenerated catalyst before it is returned to the reactor 2. The stripped gases' pass through line 26 into the regenerator 9. While this invention may be used with single stage regenera¬ tors, or with multiple stage regenerators having cocurrent instead of countercurrent flow, it is especially useful in a regenerator of the type shown which is well-suited for producing gases having a high ratio of CO to CO-. In a preferred method of carrying out this invention in a countercurrent flow pattern, ' as in the apparatus of Fig. 2, the amount of oxidizing gas and catalyst are controlled so that the amount of oxidizing gas passing into zone 25 is greater than that required to convert all the coke on the catalyst in this zone to carbon dioxide, and the amount of oxidizing gas passing upwardly from zone 25 into zone 10 together with the oxidizing gas added to zone 10 from line 21 is insufficient to convert all the coke in zone 10 to carbon dioxide. Zone 10 therefore will contain some CO. In prior art conversion processes, the regenerated catalyst is usually fed directly from the regenerated catalyst standpipe 5 into the bottom of the riser 2 where it is immediately mixed with the feed. In the present invention, a separate catalyst reducing vessel 60 is provided to treat the regenerated cata¬ lyst with a reducing gas supplied to the vessel through a sup¬ ply line 61 containing an inlet valve 62. Excess reducing gas and/or products of the reducing reaction are discharged throug an overhead vent line 63 containing an outlet valve 64. It is preferable to provide a sufficient rate of re d ucing throu h - 91 - intimate contact between the particulate catalyst and the redu ing gas. After contact with the reducing gas, the fluidized catalyst flows over into a reduced catalyst standpipe 65 which has an upper leg 66 containing a slide valve 67 and a lower le 68 containing a slide valve 69. The section of riser between lower leg 68 and upper leg 66 comprises a reducing zone 70 nea the bottom of -riser 2 to which reducing gas may be supplied by a line 71 having a riser inlet valve 72. A supply header 74 i -connected both to line 61 and 71 and may also be used to suppl both reducing gas and additional lift! gases to the bottom of •the riser through line 71. Riser reducing zone 70 may be used alone to reduce regenerated catalyst fed to the riser or in combination with the reducing vessel 60 as a supplemental reducing zone to further treat re¬ generated catalyst contacted initially with the reducing gas i vessel 60. Although line 12 to stripper 14 is usually employe to introduce a stripping medium into the stripper, it is also contemplated by the invention that thisline may be.usedto supply carbon monoxide to the stripper vessel 14 for purposes of redu ing regenerated catalyst in stripper 14 and ' in upstream regen¬ erated catalyst standpipe 26. For this purpose, a portion of the flue gas discharged through line 24 from the upper zone 10 of the regenerator may be cooled, compressed and recycled to line 12- as a source of reducing gas for reducing catalyst in the regenerated catalyst standpipe and/or stripper. A particularly preferred embodiment is described in Fig. 3 where reference numeral 80 identifies a feed.control valve in feedstock supply pipe 82. Supply pipe 83 (when used) in¬ troduces liquid water and/or an additive solution into the feed. Heat exchanger 81 in supply pipe 82 acts as a feed preheater, whereby preheated feed material may be delivered to a feed line 84 near the bottom of a riser reactor 90. Catalyst is delivered to the reactor through catalyst stand- pipe 86, the flow of catalyst being regulated by a control valve 87 and suitable automatic control equipment (not shown) with which persons skilled in the art of designing and op¬ erating riser type cracking units are familiar. - 92 - A reducing zone 91 is provided in the bottom section of the rise between the outlet of regenerated catalyst standpipe 36 and the feed inlet 84. Reducing gas is introduced into this zone throug a line 85 which may be connected to line 150 which contains hy¬ drogen and possibly methane and other reducing gases separated from liquid product by the receiver 142 discussed below. If ad¬ ditional lift gas is need, some of the water and/or feed from lines 82 and 83 may be introduced into the bottom of the riser through an alternate feedline 38. Some or all of the water in line 83 may be provided by the water discharge line 148 contain¬ ing water separated frrm product liquid and gases- by receiver 142~. The reactor is equipped with a disengagement vessel 92 simi¬ lar to the disengagement vessel 3 of the reactor shown in Fig. 2. Catalyst departs disengagement vessel 92 through stripper 94. Spent catalyst passes from stripper 94 to re ¬ generator 101 via spent catalyst transfer pipe 97 having a slide valve 98 for controlling flow. Regenerator 101 is divided into upper chamber 102 and lower chamber 103 by a divider panel 104 intermediate the upper and lower ends of the regenerator vessel. The spent catalyst from transfer pi ** *e 97 enters upper chamber 102 in which the catalyst is partially regenerated. A funnel-like collector 106 having a bias-cut upper edge receives partially regen¬ erated catalyst from the upper surface of the dense phase of catalyst in upper chamber 102 and delivers it, via drop leg 107 having an outlet 110, beneath the upper surface of the dense phase of catalyst in lower chamber 103. Instead of internal catalyst drop leg 107, one may use an external drop leg. Valve moans in such ex¬ ternal drop leg can control the residence time and flow rate in and between the upper and lower chambers. Make up cata¬ lyst and/or catalyst or regenerator additives may be added to the upp-rrr chamber 102 and/or the lower chamber 103 i EX, - 93 - through addition lines 99 and 100 respectively. Air is supplied to the regenerator through an air supply pipe 113. A portion of the air travels through a branch supply pipe 114 to bayonet 115 which extends upwardly into the in¬ terior of plenum 111 along its central axis. Catalyst in - chamber 103 has access to the space within plenum 111 be- ' tween its walls and bayonet 115. A smaller bayonet (not shown) in the aforementioned space fluffs the catalyst and urges it upwardly toward a horizontally arranged ring dis- - tributor (not shown) adjacent the open top of plenum 111 where it opens into chamber 103. The remainder of the air passing through air supply pipe 113 may be heated in air heater 117 (at least during start-up with VGO) and is then introduced into inlet 118 of the ring distributor, which may be provided with holes, nozzles or other apertures which produce an upward flow of gas to fluidize the partially re¬ generated catalyst in chamber 103. The air in chamber 103 completes the regeneration of the par¬ tially regenerated catalyst received via drop leg 107. The amount of air supplied is sufficient so that the resultant combustion gases are still able to support combustion upon reaching the top of chamber 103 and entering chamber 102. Drop leg. 107 extends through an enlarged aperture in panel 104, to which is secured a gas distributor 120 which is con¬ centric with and surrounds a drop leg. Combustion support¬ ing gases from chamber 103, which have been partially de¬ pleted, are introduced via gas distributor 120 into upper regenerator chamber 102 where they contact incoming coked catalyst from coked catalyst transfer pipe 97- Apertured probes 121 in gas distributor 120 assist in achieving a uni¬ form distribution of the partially depleted combustion sup¬ porting gas into upper chamber 102. Supplemental air or cooling fluids may be introduced into upper chamber 102 * through a supply pipe 122, which may also discharge through gas distributor 120. - 94 - Fully regenerated catalyst with less than about 0.25% carbon, preferably less than about 0.1% and more preferably less than about 0.05%, is discharged from lower regenerator chamber 103 through regenerated catalyst stripper 128, whose outlet feeds into catalyst standpipe 86. Thus, regenerated catalyst is returned to riser 91 for contact with additional fresh feed. The division of the regenerator into upper and lower regenera tion chambers 102 and 103 not only smooths out variations in catalyst regenerator residence time but is also uniquely of assistance in restricting the quantity of regeneration heat which is imparted to the fresh feed while yielding a regen¬ erated catalyst with low levels of coke for return to the riser. Because of the arrangement of the regenerator, coked catalyst from transfer line 97, with a relatively high loading of carbon, contacts in chamber 102 combustion supporting gases which have already been at least partially depleted of oxy¬ gen by the burning of carbon from partially regenerated cata¬ lyst in lower chamber 102. Because of this, it is possible to control both the combustion of carbon and the quantity of carbon dioxide produced in upper regeneration chamber 102. A though regenerating gas introduced through air supply pipe 113 and branch conduit 114 may contain relatively large quantities of oxygen, the partially regenerated catalyst which is con¬ tacts in lower chamber 103 has already had a major portion of its carbon removed. The high oxygen concentration and temp¬ erature in chamber 103 combine to rapidly remove the remain¬ ing carbon in the catalyst, thereby achieving a clean, regen¬ erated catalyst with a minimum of heat release. Thus, here again, the combustion temperature and the ratio of CO-, to CO in the lower chamber are readily controlled. The regenera¬ tion off gases are discharged from upper chamber 102 via gas pipe 123, regulator valve 124, catalyst fines trap 125 and outlet 126. OMH - 95 - The vapor products from disengagement vessel 92 may be process in any convenient manner such as by discharge through vapor li 131 to fractionator 132. Fractionator 132 includes a bottoms outlet 133, side outlet 134, flush oil stripper 135, and stripper bottom line 136 connected to pump 137 for discharging flush oil. Overhead product from stipper 135 returns to frac¬ tionator 132.via line 138. The main overhead discharge line 139 of the fractionator is co nected to an overhead receiver 142 having a bottoms line 143- feeding into pump 144 for discharging gasoline product. A por tion of this product may be returned to the fractionator via recirculation line 145, the flow being controlled by valve 146 The receiver 142 also includes a water receiver 147 and a wate discharge line 148. The gas outlet 150 of the overhead receiv discharges a stream which is mainly below-.C,, but containing some C_, C β and C_ material. If desired, the C 5 and above material in the gas stream may be separated by compression, cooling and fractionation, and recycled to receiver 142. The oxidizing gas, such as air, introduced into regeneration zone 103 through line 114 may be mixed with a cooling spray of water from a conduit 109. The mixture of oxidizing gas and atomized water flows through bayonet 115 and thus into the lower bed of catalyst particles. The apertures in distributor 120 are large enough so that the upwardly flowing gas readily passes therethrough into zone 102. However, the perforations are sized so that the pressure difference between the upper and lower zones prevents cata¬ lyst particles from passing downwardly through the distributor The bayonet 115 and distributor are similarly sized. Gases exiting the regenerator comprise combustion products, nitro¬ gen, steam formed by combustion reactions and/or from vaporiz¬ ing water added to the regenerator, and oxides of sulfur and other trace elements. These gases are separated from suspende catalyst particles by a cyclone separator (not shown) and t Jϊ - 96 - pass out of the regenerator through discharge conduit 123. While this invention may be used with single stage regenerato or with multiple stage regenerators which have basically con¬ current instead of countercurrent flow between combustion gas and catalyst, it is especially useful in regenerators of the type shown in Figs. 2 and.3, which have countercurrent flow and are well-suited for producing combustion product gases having a low ratio of CO- to CO, which helps lower regenera¬ tion temperatures in the presence of high carbon levels.. - 97 - Examples 1-4 These examples describe tests illustrating the effectiveness of the steam reforming reaction provided by the invention- The testing apparatus was comprised of a Vicor r ' eaction tube having an inside diameter of about 22 millmeters and including a pre¬ heating zone and a reaction zone heated by a surrounding fur¬ nace- A- bed comprised of 20 grams of unpacked test catalyst was supported for contact with a vaporous feed and water mix¬ ture in a reaction zone extending along the reaction tube or about 3 inches.-. During performance of the tests, the catalyst bed was maintained at a temperature of about 950°F and a vap¬ orous mixture of * n-heptane and water was first passed through the preheating zone where it was preheated to about 950°F before passing throu the catalyst bed in the reaction, zone. The n-heptane was fed into the reaction tube at an addition rate of 6.5 milliliters per hour and premixed with water upstream of the preheating zone at a mole ratio of about 14:1. This provided a contact time between the reactant mixture and the catalyst bed of about 2 seconds or less. After passing through the reaction zone, the resulting mixture of feed, water and product was passed through a condensing zone to separate liquid condensate from gaseous products. Two types of catalyst materials were used in the tests. Ex¬ amples 1 and 2 employed a Super DX catalyst available from the Davison Division of W. R. Grace and Co. This catalyst had a surface area of about 89 square meters per gram and a pore volume of about 0.25 cc/gm, and was pretreated so as to contain about 300 ppm of deposited vanadium and about 19,000 ppm of deposited nickel. The catalyst employed in Examples 3 and 4 was comprised of microspheres of calcined kaolin clay having a surface area of about 8 square meters per gram and a pore volume of about 0.10 cc/gm, and was pretreated so as to contain about 25,400 ppm of deposited vanadium and about 5,200 ppm of deposited nickel. Although the particulate material of Examples 3 and 4 is referredto here as a "catalyst", it is substantially an inert material exhibiting in its virgin state a icroactivity of less than 20, preferably about 10. - 98 - After being introduced into the test apparatus but before performance of the test, the catalysts of Examples 1 and 3 were treated with an oxidizing medium comprised of passing air over the catalyst at about 950°F until the exiting gas was substantially free of carbon oxides (at leasu 1 hour) . The catalysts of Examples 2 and 4 were similarly treated with a reducing medium comprised of passing one liter of hydrogen over the catalyst at about 950°F. This amount of hydrogen was sufficient to reduce only about 60 percent of the vana¬ dium pentoxide found on the catalyst of Example 4. The re- suits of the steam reforming tests with n-heptane and water _. passed over the catalysts of Examples 1-4 are set forth in Tables I and II. With reference to Table I, the rate of conversion of feed to product in Examples 1, 3 and 4 was sufficiently slow that about 19.5 milliliters of feed had to be passed over the cata¬ lyst during a 3 hour period in order to obtain a measurable amount of product. To ensure that all of theproduct was re¬ covered, these runs also employed either a helium or a nitro¬ gen purge to sweep the reaction system of product after com¬ pletion of the conversion reaction. The volume of purge gas used was that required to make up a total gas volume of about 1 liter in a gaseous product collecting system downstream of the liquid product condensing section. These runs provided both a gaseous product and a liquid condensate comprised of unreacted water, unreacted feed and a relatively small amount of liquid product. Contrary to Examples 1, 3 and 4, the conver¬ sion reaction of Example 2 was so rapid and complete that the capacity of the gaseous product collecting system was filled within a 10 minute reaction period and no significant amount of liquid condensate was produced. The volume percent of feed converted to product during each of these examples is given on the second line of Table II. In addition to the amount of feed converted to product, Table II shows the percentage of product provided by five of the principal reaction mechanisms that can occur in riser crackj. - 99 namely, thermal cracking reactions, catalytic cracking reactio due to acid sites on the catalyst (acid cracking) , metal dehy¬ drogenation reactions, metal steam reforming reactions, and methane forming reactions. This table also gives the rate of conversion by each of these ' reaction mechanisms. As readily apparent from a comparison of the data in Examples 1 and 2, re¬ duced nickel relative to oxidized nickel on a conversion cata¬ lyst gives a much higher rate and level of conversion, and a significant proportion of the conversion with reduced nickel is due to metal steam reforming reactions. Thus, a volume percent conversion of 96.6, of which 32.1 percent was provided be metal steam reforming, was realized in Example 2 as compared to a volume percent conversion of 7.6, of which 0.3 percent was provided by metal steam reforming, real±ze& ' -in Example 1. An even more dramatic illustration of the metal steam reforming reaction of thepresent invention is provided by a comparison between Examples 1 and 2 of the metal steam reforming conver¬ sion rate and the acid cracking conversion rate.. These rates increased in Example 2 relative to Example 1 by factors of abou 1200 and about 6-6 respectively. While the level of conversion increased, the amount of coke deposited on the catalyst de¬ creased by a factor of about 3 with the reduced catalyst of Example 2 as compared with the oxidized catalyst of Example 1. The amount of excess hydrogen generated by the metal steam re¬ forming reaction is also significant in that this hydrogen can be separated from the vapor product stream of a conversion pro¬ cess and recycled as a source of reducing gas for the oxidized nickel on regenerated catalyst. A comparison of the hydrogen data in Table I shows that the reduced conversion catalyst of Example 2 produced about 36 times more hydrogen per weight of feed converted than did the oxidized conversion catalyst of Example 1. Examples 3 and 4 are included to illustrate the adverse effects of high vanadium to nickel ratios on the metal steam refoj - 100 - reaction. Thus, while significant steam reforming would be expected at a nickel level of 5200 ppm, the presence of vana¬ dium at a weight ratio to nickel of almost 5:1 interferes with this reaction. With reference to Table II, metal dehydrogena¬ tion reactions predominate over steam reforming reactions in both Examples " 3 and 4. In addition, the presence of vanadium pentoxide on the oxidized catalyst caused certain abnormalitie as indicated by the footnotes to this table. For example, the mole percentage of product from metal dehydrogenation is be¬ lieved to be low because some of the hydrogen was consumed in reducing vanadium p.entoxide to vanadium trioxide. The weight percent hydrogen based on weight of feed converted as given fo Example 3 in Table I is similarly low. On the other hand, the mole percentage of product from metal steam reforming is be¬ lieved to be high due to the generation of carbon oxides by carbon reduction of vanadium pentoxide to vanadium trioxide- This latter conclusion is consistent with the way in which steam reforming values are determined. Calculation of the amo of metal steam reforming is based on the amount of carbon oxid produced during the conversion process. The metal steam refor ing reactions producing carbon oxides are illustrated by equa¬ tions (1) and- (2) given previously in this specification. It i nevertheless quite significant that the amount of coke produced decreased by a factor of more than 2 with the catalyst of Ex¬ ample 4 having reduced nickel as compared to the catalyst-of Exam¬ ple 3 having oxidized nickel as shown in Table I. OMPΪ 101 - TABLE I STF.ΛM REFORMING OF n-IIEPTANE ACCORDING TO EXAMPLES 1-4 Example No. 1 2 3 4 Catalyst Super DX Super DX Kaolin Kaolin Preconditioninc 1 oxidized reduced oxidized reduced Reaction Time 3 hours @ 10 min. 3 hours 3 hours Composition of gas product (%) by GC analysis: N 2 ' 0.85 7.97 72.41 64.54 «2 16.36 60.92 8.64 20.92 c l 3.89 1.22 0.74 1.31 C2 1.68 0.14 0.63 0.99 C2 = 2.38 0.04 0.97 1.27 C3 18.75 0.71 0.27 0.54 C3 = 24.08 0.70 1.80 2.22 i-C4 11.47 0.67 0.15 0.14 n-C4 3.82 0.29 0.10 0.21 ' l+iC4~ " *■' ; 4.77 0.31 0.72 - 0.S-7 tr-C 1.77 .0.10 0.18 0.22 cisC " = 1.20 0.07 0.12 0.15 1,3C S 0.04 iCs 0.48 0.02 0.03 nC 5 0.16 — — >C 5 6.05 4.58 6.14 4.48 02 0.40 0.12 1.00 0.45 CO 0.69 14.87 1.31 0.54 C0 2 0.50 7.28 4.06 0.62 Gas Product 150 1200 1000 1000 Amount, ml He purge N 2 purge N 2 purge Liquid product none amount, ml 8 observed 9 9 .Composition of : liquid product (%) : nC 94.01 98.64 93.44 Benzene 0.05 0.12 0.16 Toluene 0.43 0.39 0.62 Xylenes 0.22 0.03 0.03 Wgt.% coke based on wgt. feed con¬ verted 1.70 0.55 6.96 3-35 Wgt.% H 2 based on wgt. feed converted 0.18 6.50 2.17' 4.62 Wgt.% H 2 based on total feed wgt. 0.014 6.28 0.05 0.12 Se -102- TABLE II STEAM REFORMING OF n-HEPTANE ACCORDING TO EXAMPLES 1-4 Example No. 1 2 3 4 Vol.% Feed Con¬ verted to Product 7.6 96.6 2.3 2.6 Mole Percentage of Product Converted by Each Mechanism: Thermal Cracking 0.4 0.5 2.9 3.6 Acid Cracking 97.5 50.0 55.0 42.4 Metal Dehydro¬ genation 1.5 15.7 31.0 * 50.0 Metal Steam Reforming 0.3 32.0 9.8** 1.9 Methane Forming 0.3 1.8 1.3 2.1 Total 100.0 100.0 100.0 100.0 Rate of Conversion by Each Mechanism ( mjnute x 10 ~ ) : Thermal Cracking 2 38 5 7 Acid Cracking 578 3,840 98 86 Matal Dehydro¬ genation 9 1,210 56.0* 101 Metal Steam Reforming 2 2,420 18** 4 Methane Forming 2 140 2 4 Total 593 7,648 179 203 * This abnormality is due to hydrogen consumed to reduced vana¬ dium pentoxide according to the following reaction: V 2°5 + 2H 2 → V 2°3 + 2H 2° ** This abnormality is due to carbon reduction of vanadium pentox ide according to the following reaction in which [C] represents a general source of carbon: V 2 0 5 + 2[C] --> V 2 0 3 + 2CO - 103 - Having thus described actual tests, the following Example is offered to illustrate practice of the invention in more detai " Example 5 A carbo-metallic feed at a temperature of about 450°F is intr duced at a rate of about 2070 pounds per hour into the bottom zone of a vented riser reactor where it is mixed with steam, liquid water and a zeolite catalyst at a temperature of. about 1275°F. The catalyst to oil ratio by weight is about 11:1. The carbo-metallic feed has a heavy metal content of about 5 ■ parts per million nickel equivalents which is comprised of a- bout 4 ppm nickel and about 5 ppm vanadium. This feed has a sulfur content of about one percent and a Conradson carbon co tent of about 7 percent. About 85 percent of the feed boils above 650°F and about 20 percent of the feed boils above 1025 The liquid water and steam are injected into the riser at a r of about 120 and 400 pounds per hour respectively to provide mole ratio of water to feed of about 4. The temperature at ' t riser outlet is about 1000°F and the pressure within theriser about 40 psia. The partial pressure of feed and steam are about 8 psia and about 32 psia respectively. Within the riser about 75 volume percent of the feed is conve to fractions boiling at a temperature less than 430°F and abo 55 volume percent of the feed is converted to gasoline. The catalyst containing about 1 percent by weight of coke and about 0.01 weight percent sulfur is removed from the reactor and introduced into a stripper where it is contacted with ste at a temperature of about 1000°F to remove volatiles adsorbed onto the catalyst- The stripped catalyst is introduced into the upper zone of a two-zone regenerator as shown in Fig. 1 a a rate of 23,000 pounds per hour. Each -zone contains about 4000 pounds of catalyst for a total catalyst inventory of abo 8000 pounds. Air is introduced into the lower zone at a rate of about 1400 pounds per hour. The lower zone produces 85 pounds of CO- per hour and no measurable amount of - 104 - at a temperature of about 1340°F. Air is introduced into the upper zone at a rate of about 1200 pounds per hour together with flue gases from the lower zone. The upper zone produces 540 pounds of CO- per hour and 112 pounds of CO per hour, and it is at a temperature of about 1330°F. The regenerator flue gases contain 3400 ppm sulfur oxides and CO- and CO in a iole ratio of 3.6. The catalyst removed from the lower zone and recycled to the reactor riser contains a- bout 0.03 percent coke by weight. and about 10,000 ppm nickel equivalents of which about 8,000 ppm is nickel and about 10,0 ppm is vanadium. A hydrogen treatment vessel is provided between the regenerator and t riser as shown in Fig. 2 to reduce nickel oxide on the regen¬ erated catalyst before it is contacted with fresh feed and water. A relatively pure hydrogen atmosphere is maintained in the hydrogen treatment vessel and hydrogen is consumed at the rate of about 6 pounds per hour in reducing about 182 pou of nickel per hour from its oxide form (NiO) to elemental nickel (Ni) . During the conversion, the amount of coke pro¬ duced is about one-half or less and the amount of hydrogen produced is about 30 times or more of the respective amounts of coke and hydrogen that are produced in the ab¬ sence of reduction of the nickel on the catalyst and steam reforming in the riser.

Claims: - 105 - Claims What is claimed is: 1. A process for economically converting carbo-metallic oils to liquid fuel products in a system comprising a pro¬ gressive-flow reactor and a catalyst regenerator comprising: a. providing a converter feed containing 650°F÷ material, said 650°F+ material being characterized by a carbon residu on pyrolysis of ?t least about 1 and by containing at least about 4 parts per million of Nickel Equivalents of heavy metal(s), said heavy metal(s) including nickel? b. bringing said converter feed together with particulate cracking catalyst to form a stream comprising a suspension of said catalyst in said feed and causing the resultant stream to flow through a progressive flow type reactor havin an elongated conversion zone for a predetermined vapor riser residence time in the range of about 0.5 to about 10 seconds ' at a temperature of about 900 to about 1400°F and under a pressure of about 10 to about 50 pounds per square inch ab¬ solute sufficient for causing a conversion per pass in the range of about 50% to about 90% while depositing at least a portion of said heavy metal(s) on the catalyst and produc¬ ing coke on the catalyst in amounts in the range of about 0.3 to about 3% by weight; c. separating spent, coke-laden catalyst from the stream of hydrocarbons formed by vaporized feed and resultant crack ing products; d. maintaining, in one or more regeneration zones, one or more fluidized catalyst regeneration beds comprising spent catalyst undergoing regeneration by combustion of the coke with oxygen on the spent catalyst, and sunolying addition'1„ - 106 - spent catalyst to one or more of such fluidized regeneration bed or beds; e. retaining said catalyst particles in said regeneration zone or zones in contact with a flow of said combustion-sup¬ porting gas under conditions of temperature, atmosphere and average total residence time in said zone or zones sufficien for combustion of the coke on the catalyst and for reducing the level of carbon on the catalyst to about 0.25% by weight or less, while forming gaseous combustion product gases com- prising CO and/or C0-, said regenerated catalyst being char-- acterized by a deposited nickel content in at least a par¬ tially oxidized state; f. contacting said regenerated catalyst with a reducing gas under reducing conditions sufficient to reduce at least a portion of said oxidized nickel to a reduced state; g. recycling the regenerated catalyst with said deposits of reduced nickel to the reactor conversion zone for contact with fresh feed; and h. introducing water into said reactor conversion zone so as to form a mixture of water with said suspension of catalyst feed, the amount of water introduced into said reactor conve sion zone and the amount of reduced nickel on said recycled catalyst being sufficient to provide a steam reforming reac¬ tion in said reactor conversion zone so that hydrogen defi¬ cient components of said converter feed are converted to pro¬ ducts having higher hydrogen to carbon ratios and the amount of said converter feed converted to coke is reduced. - REA - 107 - 2. The process according to claim 1 in which said regenerate catalyst contains deposited nickel in an amount of at least 2000 ppm. 3. The process according to claim 1 in which said regenerate catalyst contains deposited nickel in an amount of at least 30.00 ppm. 4. The process according to claim 1 in which said regenerate catalyst contains deposited nickel in an -amount of at least 6000 ppm. - 5. The process according to claim 1 in which said regenerate catalyst contains deposited nickel in the range of 7000 to 20,000 ppm. 6. The process of claim 1 in which the ratio of the partial pressure of water to the partial pressure of feed in said re¬ actor conversion zone is about 14 or less. 7. The process of claim 1 in which the ' ratio of the partial pressure of water to the partial pressure of feed in said re¬ actor conversion zone is about 7 or less- 8. The process of claim 1 in which the ratio of the partial pressure of water to the partial pressure of feed in said re¬ actor conversion zone is about 4 or less. 9. The process of claim 1 in which the ratio of the partial pressure of water to the partial pressure of feed in said re¬ actor conversion zone is in the range of from about 3 to abou 4. 10. The process of claim 1 in which said heavy metals also in clude vanadium and the weight ratio of vanadium to nickel is less than about 3.0. - J E, - QQ - 11. The process of claim 10 in which the weight ratio of va dium to nickel is about 2.0 or less. 12. The process of claim 10 in which the weight ratio of va dium to nickel is about 1.0 or less. 13. The process of claim 1 in which said cracking catalyst has a surface area of at least 40 square meters per gram and total pore volume of at least 0.2 cc/gm. 14. The process of_claim 1 in which said cracking catalyst _ has a surface area of at least 80 square meters per gram and total pore volume of at least 0.3 cc/gm. 15. The process of claim 1 in which said cracking catalyst has a surface area in the range from about 80 to about 250 square meters per gram and a.-.total pore volume of at least 0.5 cc/gm. 16. The process of claim 1 in which liquid water, steam, or combination of liquid water and steam is introduced into said conversion zone in a mole ratio relative to feed from about 2:1 to about 14:1. 17. The process of claim 1 in which the level of carbon on t catalyst is reduced to about 0.1 percent or less in said re¬ generation zone or zones. 18. The process of claim 1 in which the nickel content of sai recycled catalyst is in the range of about 0.5 to about 2.5 weigh percent based on weight of catalyst. 19. The process of claim 1 in which the nickel content of sai recycled catalyst is in the range of about 2.0 to about 3.0 weight percent based on weight of catalyst. 20. The process of claim 1 in which the temperature of cataly leaving said conversion zone is between about 900°F and a^^. 1200°F. Q MP - 109 - 21. The process of claim 1 in which the temperature of cataly leaving said conversion zone is at a temperature in the range of about 1000°F to about 1100°F. 22. The process of claim 1 in which said vapor riser residenc time is in the range of about 0.5 to about 3 seconds. 23. The process of claim 1 in which said vapor riser residenc time is in the range of about 1.0 to about 2.0 seconds. "$ f E MPI

Inventors: HETTINGER WILLIAM P JR, KOVACH STEPHEN M, MYERS GEORGE D, ZANDONA OLIVER J
Applicants: ASHLAND OIL INC, HETTINGER WILLIAM P JR, KOVACH STEPHEN M, MYERS GEORGE D, ZANDONA OLIVER J
Application year: 1981
Main classification: C10G11
IPC codes: C10G11, C10G47