TWO STAGE HYDRODESULFURIZATION PROCESS

Abstract: A process for hydrodesulfurizing naphtha feedstreams wherein the reactor inlet temperature is below the dew point of the feedstock at the reactor inlet so that the naphtha will completely vaporize within the catalyst bed. It is preferred to use a catalyst comprised of about 1 to about 10 wt.% MoO3, about 0.1 to about 5wt.%CoO supported on a suitable support material. They are also characterized as having an average medium pore diameter from about 60 ANGSTROM to 200 ANGSTROM , a Co/Mo atomic ratio of about 0.1 to about 1.0, a MoO3 surface concentration of about 0.5 x 10<-4> to about 3.0 x 10<-4>g MoO3/m<2>, and an average particle size of less than about 2.0mm in diameter.

Description: TWO STAGE HYDRODESULFURIZATION PROCESS FIELD OF THE INVENTION The present invention relates to a two stage process for hydrodesulfurizing naphtha feedstreams wherein the first stage contains a catalyst comprised of about 1 to about 10 wt.% M0O3, about 0.1 to about 5 wt.% CoO supported on a suitable support material. They are also characterized as having an average medium pore diameter from about 60 A to 200 A, a Co/Mo atomic ratio of about 0.1 to about 1.0, a M0O3 surface concentration of about 0.5 x 10 ~ 4 to about 3.0 x 10"4g M0O3/1T12, and an average particle size of less than about 2.0 mm in diameter; and the second stage contains a conventional hydrodesulfurization catalyst comprised of at least one Group VIII metal and at least one Group VI metal on an inorganic oxide support. BACKGROUND OF THE INVENTION Naphtha streams are primary products in any petroleum refinery in the United States. These streams are blended to makeup what is referred to in the industry as the "gasoline pool". One problem associated with such streams, especially those naphtha streams which are products of a cracking process, such as fluidized catalytic cracking and coking, is that they contain relatively high levels of undesirable sulfur. They also contain valuable olefins which contribute to the octane number of the resulting gasoline pool, and thus it is highly desirable not to saturate them to lower octane paraffins during processing. There is a continuing need for catalysts having ever improved properties with respect to the desulfurization of naphtha streams so that the sulfur level of such streams can be brought to the ever lower levels required by ever stricter governmental regulations. Research over the last couple of decades has resulted in a great many hydrodesulfurization catalysts and processes for desulfurizing naphtha feed streams, while attempting to keep olefin saturation at a minimum. While there are commercially successful naphtha hydrodesulfurization catalysts in use today, there is a continuing need for improved catalysts that are capable of combining optimum hydrodesulfurization with minimum hydrogenation of olefin. SUMMARY OF THE INVENTION In accordance with the present invention, there is provided a two stage process for hydrodesulfurizing a naphtha feedstock, which process comprises: i) reacting said feedstock in a first reaction stage under hydrodesulfurization conditions in contact with a catalyst is comprised of: (a) about 1 to 10 wt.% M0O3; and (b) about 0.1 to 5 wt.% CoO; and (c) a Co/Mo atomic ratio of about 0.1 to 1.0: and (d) a median pore diameter of about 60 A to 200 A; and (e) a M0O3 surface concentration in g M0O3/1T1- of about 0.5 x 10"4 to 3 x 10- 4 : and (f) an average particle size diameter of less than about 2.0 mm; and ii) passing the reaction product of the first stage to a second stage, also operated under hydrodesulfurization conditions, and in contact with a catalsyt comprised of at least one Group VIII metal selected from the group consisting of Co and Ni, and at least one Group VI metal selected from the group consisting of Mo and W. more preferably Mo. on an inorganic oxide support material. - J In a preferred embodiment of the present invention the catalyst has a metals sulfide edge plane area from about 800 to 2800 μmol oxygen/g M0O3 as measured by oxygen chemisorption. In another preferred embodiment of the present invention the Group VIII metal is Ni and the Group VI metal is Mo. In another preferred embodiment of the present invention, the process conditions of hydrodesulfurization are such that the inlet temperature of the feedstock to the reaction unit is below the dew point of the feedstock and 100% of the feedstock becomes vaporized in the catalyst bed. In other preferred embodiments of the present invention, the M0O3 surface concentration in g Moθ3/rn2 is about 0.75 x 10 ~ 4 to 2.5 x 10" ; the Co/Mo atomic ratio is from about 0.20 to 0.85: and the mean pore diameter is from about 75 A to about 175 A. BRIEF DESCRIPTION OF THE FIGURES Figure 1 is a plot of percent hydrodesulfurization versus percent olefin saturation for the examples presented in Example 1 1 hereof. Figure 2 is a bar chart showing relative volumetric activity for hydrodesulfurization for the catalyst systems of Example 1 1 herein wherein one catalyst system is a bed of only the catalyst of this invention, a second catalyst system is a bed composed of 87 vol.% of the catalyst of this invention and 13 vol.% of the conventional catalyst KF-742: and a third catalyst system which is a bed composed of 74 vol.% of catalyst of this invention and 26 vol.% of the conventional catalvst KF-742. DETAILED DESCRIPTION OF THE INVENTION Naphtha feedstocks suitable for use in the present invention can comprise any one or more refinery streams boiling in the range from about 10°C to about 232°C, at atmospheric pressure. The naphtha feedstock generally contains cracked naphtha which usually comprises fluid catalytic cracking unit naphtha (FCC catalytic naphtha), coker naphtha, hydrocracker naphtha, resid hydrotreater naphtha, debutanized natural gasoline (DNG), and gasoline blending components from other sources wherein a naphtha boiling range stream can be produced. FCC catalytic naphtha and coker naphtha are generally more olefinic naphthas since they are products of catalytic and/or thermal cracking reactions. and are the more preferred streams for use in the present invention. The naphtha feedstock, preferably a cracked naphtha feedstock, generally contains not only paraffins, naphthenes, and aromatics, but also unsaturates, such as open-chain and cyclic olefins, dienes, and cyclic hydrocarbons with olefinic side chains. The cracked naphtha feedstock generally comprises an overall olefins concentration ranging as high as about 60 wt.%. more typically as high as about 50 wt.%. and most typically from about 5 wt.% to about 40 wt.%. The cracked naphtha feedstock can comprise a diene concentration of as much as 15 wt.%, but more typically ranges from about 0.02 wt.% to about 5 wt.% of the feedstock. High diene concentrations can result in a gasoline product with poor stability and color. The cracked naphtha feedstock sulfur content will generally range from about 0.05 wt.% to about 0.7 wt.% and more typically from about 0.07 wt.% to about 0.5 wt.% based on the total weight of the feedstock. Nitrogen content will generally range from about 5 wppm to about 500 wppm. and more typically from about 20 wppm to about 200 wppm. There are many hydrodesulfurization catalysts in the prior art that are similar to those used in the first stage of the present invention, but none can be characterized as having all of the unique properties, and thus the level of activity for hydrodesulfurization in combination with the relatively low olefin saturation, as those of the instant invention. For example, some conventional hydrodesulfurization catalysts typically contain M0O3 and CoO levels within the range of those instantly claimed. Other hydrodesulfurization catalysts have surface areas and pore diameters in the range of the instant catalysts. Only when all of the properties of the instant catalysts are present can such a high degree of hydrodesulfurization in combination with such low olefin saturation be met. The properties which are critical to the catalysts of the present invention include: (a) a M0O3 concentration of about 1 to 10 wt.%, preferably about 2 to 8 wt.%. and more preferably about 4 to 6 wt.%, based on the total weight of the catalyst: (b) a CoO concentration of about 0.1 to 5 wt.%, preferably about 0.5 to 4 wt.%, and more preferably about 1 to 3 wt.%, also based on the total weight of the catalyst: (c) a Co/Mo atomic ratio of about 0.1 to about 1.0, preferably from about 0.20 to about 0.80. more preferably from about 0.25 to about 0.72; (d) a median pore diameter of about 60 A to about 200 A, preferably from about 75 A to about 175 A, and more preferably from about 80 A to about 150 A; (e) a M0O3 surface concentration of about 0.5 x 10 ~ 4 to about 3 x 10 ~ 4 g. Moθ3/m-*-*, preferably about 0.75 x 10 ~ 4 to about 2.5 x 10 ~ 4, more preferably from about 1 x 10 ~ 4 to about 2 x 10"4; and (f) an average particle size diameter of less than 2.0 mm, preferably less than about 1.6 mm, more preferably less than about 1.4 mm. and most preferably as small as practical for a commercial hydrodesulfurization process unit. The most preferred catalysts will also have a high degree of metal sulfide edge plane area as measured by the Oxygen Chemisorption Test described in "Structure and Properties of Molybdenum Sulfide: Correlation of O2 Chemisorption with Hydrodesulfurization Activity". SJ. Tauster et al., Journal of Catalysis 63. pp 515-519 (1980). which is incorporated herein by reference. The Oxygen Chemisorption Test involves edge-plane area measurements made wherein pulses of oxygen are added to a carrier gas stream and thus rapidly traverse the catalyst bed. For example, the oxygen chemisorption will be from about 800 to 2,800, preferably from about 1,000 to 2,200. and more preferably from about 1.200 to 2.000 μmol oxygen/ gram M0O3. The terms hydrotreating and hydrodesulfurization are sometimes used interchangeably in this document. The catalysts for both the first and second stage reaction zones of the present invention are supported catalysts. Any suitable inorganic oxide support material may be used for the catalyst of the present invention. Non- limiting examples of suitable support materials include: alumina, silica, titania. calcium oxide, strontium oxide, barium oxide, carbons, zirconia, diatomaceous earth, lanthanide oxides including cerium oxide, lanthanum oxide, neodynium oxide, yttrium oxide, and praesodynium oxide; chromia, thorium oxide, urania, niobia, tantala, tin oxide, zinc oxide, and aluminum phosphate. Preferred are alumina, silica, and silica-alumina. More preferred is alumina. For the catalysts with a high degree of metal sulfide edge plane area of the present invention, magnesia can also be used. It is to be understood that the support material can contain small amount of contaminants, such as Fe. sulfates. silica, and various metal oxides which can be present during the preparation of the support material. These contaminants are present in the raw materials used to prepare the support and will preferably be present in amounts less than about 1 wt.%. based on the total weight of the support. It is more preferred that the support material be substantially free of such contaminants. It is an embodiment of the present invention that about 0 to 5 wt.%, preferably from about 0.5 to 4 wt.%. and more preferably from about 1 to 3 wt.%, of an additive be present in the support, which additive is selected from the group consisting of phosphorus and metals or metal oxides from Group IA (alkali metals) of the Periodic Table of the Elements. The hydrodesulfurization process of the present invention will typically begin with a cracked naphtha feedstock preheating step. That is. the chargestock is preheated in feed/effluent heat exchangers prior to entering a furnace for final preheating to a targeted reaction zone inlet temperature. The feedstock can be contacted with a hydrogen-containing stream prior to, during, and/or after preheating. The hydrogen-containing stream can also be added in the hydrodesulfurization reaction zone. The hydrogen stream can be pure hydrogen or can be in admixture with other components found in refinery hydrogen streams. It is preferred that the hydrogen-containing stream have little, if any, hydrogen sulfide. The hydrogen stream purity should be at least about 50% by volume hydrogen, preferably at least about 65% by volume hydrogen, and more preferably at least about 75% by volume hydrogen for best results. Each reaction stage can consist of one or more fixed bed reactors each of which can comprise a plurality of catalyst beds. Since some olefin saturation will take place, and olefin saturation and the desulfurization reaction are generally exothermic, consequently interstage cooling between fixed bed reactors, or between catalyst beds in the same reactor shell, can be employed. A portion of the heat generated from the hydrodesulfurization process can be recovered and where this heat recovery option is not available, cooling may be performed through cooling utilities such as cooling water or air. or through use of a hydrogen quench stream. In this manner, optimum reaction temperatures can be more easily maintained. The process of the present invention, for both stages, generally operates at a liquid hourly space velocity of from about 0.5 hr * to about 15 hr -- . preferably from about 0.5 hr ~ l to about 10 hr and most preferably from about 2 hr 1 to about 10 hr 1 . The most preferred mode of performing the hydrodesulfurization in the first reaction stage is to use a reactor inlet temperature below the dew point of the feedstock so that the naphtha fraction will not be completely vaporized at the reactor inlet. As the hydrodesulfurization reaction begins when the naphtha feed contacts the catalyst, some of the exothermic heat of reaction is absorbed by the endothermic heat of vaporization, thus achieving 100% vaporization within the bed (dry point operation). By transferring some of the heat of reaction to vaporization, the overall temperature rise across the reactor is moderated, thus reducing the overall extent of olefin hydrogenation with only small reductions in hydrodesulfurization. The degree of vaporization is defined by the ratio of the inlet dew point temperature (Trjp, R) of the naphtha feedstock to the reactor inlet temperature (Trjsj R), where R is the absolute temperature in degrees Rankine. The dew point temperatures can be calculated by computer software programs, such as Pro/II, available from Simulation Sciences Inc. In the present configuration, the Trjp/TjN ratio should be greater than or equal to 0.990. but less than the ratio at which dry point operation is not achieved within the catalyst bed. That is. the ratio extends up to the point at which the operation stays all mixed phase in the reactor. The ratio limit may vary somewhat depending on selected operating conditions. The 0.990 ratio is specified to account for uncertainties in the measurement of the inlet temperature including variance in the location of the temperature measurement and uncertainties in the calculation of the actual dew point; however, the naphtha feedstock should not be completely vaporized at the reactor inlet. The metals of the catalyst for both reaction stages of the present invention can be deposited or incorporated upon the support by any suitable conventional means, such as by impregnation employing heat-decomposable salts of the Group VIB and VIII metals or other methods known to those skilled in the art such as ion-exchange, with impregnation methods being preferred. Suitable aqueous impregnation solutions include, but are not limited to cobalt nitrate, ammonium molybdate, nickel nitrate, and ammonium meta-tungstate. Impregnation of the hydrogenation metals on the catalyst support using the above aqueous impregnation solutions can be performed using incipient wetness techniques. The catalyst support is precalcined and the amount of water to be added to just wet all of the support is determined. The aqueous impregnation solutions are added such that the aqueous solution contains the total amount of hydrogenation component metal(s) to be deposited on the given mass of support. Impregnation can be performed for each metal separately, including an intervening drying step between impregnations, or as a single co- impregnation step. The saturated support can then be separated, drained, and dried in preparation for calcination. Calcination generally is performed at a temperature of from about 250°C to about 650°C, or more preferably from about 425°C to about 600°C. Hydrodesulfurization of the naphtha feedstocks of the present invention for both reaction stages may be performed under the following conditions: Conditions Broad Preferred Temp (°C) 230-370 260-355 Total Press (psig) 200-800 200-500 H 2 Feed Rate SCF/B' 200-5000 1500-3000 H, Purity v% 50-100 65-100 LHSV 2 0.5-15 0.5-10 ' Standard Cubic Feed per Barrel 2 Liquid Hourly Space Velocity Reaction pressures and hydrogen circulation rates below these ranees can result in higher catalyst deactivation rates resulting in less effective selective hydrotreating. Excessively high reaction pressures increase energy and equipment costs and provide diminishing marginal benefits. The following examples are presented to illustrate the invention and should not be considered limiting in any way. Example 1 A solution was prepared by dissolving 8.590 g. of citric acid in 15 ml of deionized water to which 2.840 g. of cobalt carbonate was added. The resulting solution was heated to a boil then held there until the solution was clear. The heated solution was then cooled to about room temperature and 6.533 g. of ammonium heptamolybdate was added. After the solution became clear, the solution was diluted to 73.3 ml with deionized water. 1 18.2 g. of a transitional alumina extrudate which contained 84.6 wt.% solids and the remainder adsorbed water was added to the solution and agitated for several minutes to wet all of the particles. The transitional alumina extrudate was in cylindrical form with an average diameter of 1/16 inch, a median pore diameter as measured by mercury intrusion of 87 A, a surface area of about 270 nv-Vg. and a pore volume of about 0.60 cm^/g. After the particles were wetted, the solution was air dried under a hood overnight in an evaporation dish after which it was dried at about 120°C for four hours and then calcined at 455°C for two hours in air. The resulting catalyst is Catalyst A, which is used in Example 3 below. Example 2 Isothermal, upflow, all-vapor phase runs were made using a small fixed-bed unit with an intermediate cat naphtha (ICN) feedstock. The naphtha was found to have a 80-155°C boiling range (5% and 95% distillation boiling points), 740 wppm total sulfur, and 46 bromine number. The olefin saturation in this and all examples herein was determined by using the bromine number test (ASTM 1 159). A series of 5 wt.% M0O3 catalysts supported on alumina were prepared such that the atomic mole ratio of cobalt to molybdenum varied from 0.0 to 0.86 (0.0-2.4 wt.% CoO was added). The M0O3 surface concentrations for these catalysts were between 1.0 and 2.0x10"^ g Moθ3/m2, the average particle diameters were 1/32 inch, and the median pore diameters were 75-76 A as measured by mercury intrusion on the fresh catalysts in oxidized form. Each catalyst was sulfided in situ with a 10% H2S/H2 gas blend at 370-400°C for 8 hr and cooled to 250°C before the introduction of the naphtha feedstock. For the tests, the reactor conditions were 275°C, 1000 SCF/B, 100% hydrogen treat gas. 200 psig total inlet pressure and constant space velocity. Table I below lists the selectivity factors (xlO) and the Co/Mo atomic mole ratios. The selectivity factor has been described previously in US Patent 4.149,965 and is defined as the ratio of the hydrodesulfurization rate constant to the olefin hydrogenation rate constant: Selectivity Factor = — Vs ~ p~ Vs " f Ln [ B∑L (Br n where Sf, Sp are the feed and product sulfur levels, respectively and Brf and Brp are the feed and product bromine number levels, respectively. Table 1 shows that there is a maximum in selectivity when the Co/Mo mole ratio is greater than 0.0 and less than 0.86. TABLE I Co/Mo Mole Ratio Selectivity Factor (xlO) 0.00 2.8 0.20 5.5 0.43 6.2 0.86 4.8 Example 3 Isothermal, upflow, all-vapor phase pilot plant runs were made on an ICN feedstock (70-163°C, 775 wppm total sulfur, 49.2 bromine number) at 274°C. 200 psig total inlet pressure, treat gas to oil of 2000 SCF/B. 100% hydrogen treat gas and constant LHSV. Three catalysts were tested under these conditions: (1) Catalyst A, which was prepared according to Example 1 herein, is a 5.2 wt.% M0O3 and 1.5 wt.% CoO on an alumina support with a 87 A median pore diameter and 1/16 inch particle diameter (of this invention); (2) Catalyst B which is a 8.2 wt.% M0O3 and 2.4 wt.% CoO on an alumina support with a 85 A median pore diameter and 1/16 inch particle diameter; and (3) Catalyst C which is a commercial RT-2 catalyst that contained about 12 wt.% M0O3 and 4 wt.% CoO (67 A median pore diameter and 1/16 inch particle diameter). The Co/Mo mole ratios for all three catalysts ranged from 0.55 to 0.63. A fourth catalyst. Catalyst D, was also tested but the catalyst was first run with a heavy cat naphtha feed (1757 wppm total sulfur and 29.7 bromine number) for a period of 24 days before switching to the above ICN feedstock and conditions. Catalyst D w as a commercial KF-742 catalyst with about 15 wt.% M0O3. 4 wt.% CoO. 72 A median pore diameter and 1.3 mm particle diameter. All catalysts were sulfided in situ with a 10% H2S/H2 gas blend at 37TC for 15 hr and cooled to 93°C before the introduction of the initial naphtha feedstock. After the introduction of the ICN feedstock, the catalysts were given 4-1 1 davs to line-out. Table II shows the selectivity factor (xl O) as a function of the M0O3 surface concentration. Catalyst A. which is a catalyst of this invention, shows a clear enhancement in selectivity when the M0O3 surface concentration is less than 2.9x10 ~ 4 g MoO3/m2. For the same catalysts, the treat gas to oil ratio was changed to 1000 SCF/B after the completion of the balances at 2000 SCF/B. Again, Catalyst A shows a clear enhancement in selectivity when the M0O3 surface concentration is less than 2.9x10" 4 g M0O3/1Η 2 . TABLE II Treat Gas Ratio Total Days Surface Selectivity Catalyst SCF/B on Oil Concentration Factor (xlO) g MoO 3 /m 2 A 2000 1 1 1.9 x IO- 4 6.2 B 2000 11 2.9 x IO- 4 4.6 C 2000 11 4.0 x lO- 4 4.5 D 2000 28 5.5 x lO' 4 3.9 A 1000 25 1.9 x lO" 4 5.2 B 1000 25 2.9 x lO "4 4.3 C 1000 25 4.0 x lO" 4 4.5 D 1000 40 5.5 x lO" 4 4.5 Example 4 The temperature response of three low-metal catalysts was investigated with an ICN feedstock (71-167°C, 922 wppm total sulfur. 58 bromine number) at 200 psig total inlet pressure. 1000 SCF/B treat gas to oil ratio, 100% hydrogen and 260-288°C. The runs were done in isothermal, upflow reactors in all-vapor phase operation. The catalysts were prepared in the laboratory with M0O3 contents ranging from 3.2-5.2 wt.% and CoO contents ranging from 0.9-1.5 wt.%. Three different alumina supports were used that varied significantly in the median pore diameters. The supports w ill be referred to as Support X which had a 58 A median pore diameter (MPD). Support Y which had a 87A MPD. and Support Z which had a 131 A MPD. The average particle diameters of the catalysts were all less than 1/16 inch so as to isolate the effect of pore diameter with temperature. Each catalyst was sulfided in situ with a 10%) H2S/H2 gas blend at 371 °C for 15 hr and cooled to 93 °C before the introduction of the ICN feedstock. The catalysts and the hydrodesulfurization (HDS) results as a function of temperature are reported in Table III below. TABLE III Catalyst Wt.% Wt.% Particle Median Pore Relative Number MoO 3 CoO Support Dia., inch Diameter. A LHSY Temρ.°C %HDS 1 4.9 1.4 X 1/20 58 1 260 74.0 1 274 90.0 1 288 91.8 5.2 1.5 Y 1/32 87 1.75 260 75.7 1.75 274 86.2 1.75 288 95.8 .2 0.9 1/20 131 1 260 72.6 1 274 87.6 1 288 96.0 For both Catalysts 2 and 3. the %HDS increased in a uniform trend from 260 to 288°C. However, for Catalyst 1 , only a small increase was observed from 274 to 288°C indicating a HDS diffusion limitation due to the small average pore size of 58A. Therefore, catalysts of the present invention must have median pore diameters greater than 58 A at moderate operating temperatures. Example 5 Isothermal, upflow. all-vapor phase pilot plant runs were made on a heavy cat naphtha (HCN) feedstock (72-228°C. 2075 wppm total sulfur. 33.9 bromine number) using the three catalysts listed in Table IV below. The two low-metal CoMo catalysts were made with aluminas that had median pore diameters of 87 A (Support Y) and 131 A (Support Z) as measured by mercury intrusion on the fresh catalysts in the oxidized form. The third catalyst used was a high-activity, commercial catalyst (KF-752) with a median pore diameter of 77 A. In order to monitor the performance of the high-activity catalyst at levels similar to the low-metals catalysts, less volume of the high-activity catalyst was loaded into its reactor (by a factor of 4.7). This resulted in the very high space velocities used for this catalyst. Each catalyst was sulfided in situ with a 10% H2S/H2 gas blend at 370°C for 15 hr and cooled to 93°C before the introduction of the HCN feedstock. The catalysts were first allowed to line-out for 10 days at the base condition of 296°C, 800 SCF/B and 325 psig total inlet pressure. After this period, the temperature was increased to 338°C and the space velocity was increased by a factor of 2 for each catalyst. Data was taken after one day on oil (Case I). After 8 days, the conditions were switched back to the base conditions. After 4 days, the conditions were changed to 354°C and 300 SCF/B: again data was taken after one day on oil (Case II). Table IV shows the %HDS results for the three catalysts. TABLE IV Commercial Low-Metal Low-Metal High Catalyst on Catalyst on Description Activity Catalvst Support Y Support Z Wt.% M0O 3 20.5 5.2 Wt.% CoO 4.9 1.5 0.9 Median Pore Diameter. A 77 87 131 Base LHSV* 4.7 1 1 Base Temperature, °C 296 296 296 Base %HDS 89.2% 97.6% 89.4% Case I LHSV* 9.3 2 Case I Temperature, °C 337 337 337 Case I %HDS 89.9% 99.7% 97.0% Case II LHSV* 4.7 1 1 Case II Temperature, °C 354 354 354 Case II %HDS 63.8% 97.5% 89.9% * Space velocities on a relative basis. A comparison of the Base Case to Case I shows that the high- activity catalyst had the smallest increase in HDS level. Comparing the Base Case with Case II shows that there was a dramatic decrease in FIDS level for the high-activity catalyst whereas the HDS levels for each low-metal catalyst remained approximately constant. Both Cases I and II indicate that there is a significant HDS diffusion limitation for the high-activity catalyst with the HCN feedstock at temperatures greater than 337°C. Therefore, the median pore diameter should be greater than about 77 A for higher temperature operations. Example 6 Isothermal, upflow. all-vapor phase pilot plant runs were made using two very similar HCN feedstocks with 72-228°C boiling range. 1760 (Feed L) to 2075 (Feed H) wppm total sulfur, and 29.7 (Feed L) to 33.2 (Feed H) bromine number. A laboratory-prepared low-metal catalyst and a commercially- produced low-metal, catalyst were compared to the commercial catalysts RT-2 and KF-742. The low-metal catalysts were 1.3 mm asymmetric quadrilobes with 84-87 A median pore diameters and consisted of 4.2 wt.% M0O3 and 1.2- 1.3 wt.% CoO on alumina. Commercial RT-2 was a 1/16 inch extrudate with 67 A median pore diameter and about 12 wt.% M0O3 and 4 wt.% CoO. The KF-742 commercial catalyst was a 1.3 mm quadrilobe with a 72 A median pore diameter and about 15 wt.% M0O3 and 4 wt.% CoO. Each catalyst was sulfided in situ with a 10% H2S/H2 gas blend at 371 °C for 15 hr and cooled to 93°C before the introduction of the naphtha feedstock. For the tests, the reactor conditions were 302°C, 1000 SCF/B, 80% hydrogen/20% methane treat gas and 325 psig total inlet pressure. The space velocities were adjusted such that HDS levels between 96 and 99% were obtained. Table V below summarizes the HDS and olefin hydrogenation (OH) levels along with the calculated selectivity factors. The selectivity factors show that the low-metal catalysts are the most selective for HDS. TABLE V HCN LHSV Selectivity Catalyst Feed (relative) %HDS %OH Factor (x 10) Commercial RT-2 L 2.8 96.8 45.6 2.93 Commercial KF-742 L 6.4 97.8 48.9 3.17 Lab Low-Metal Catalvst H 1 99.2 58.5 3.54 Commercial Low-Metal Catalyst H 1 99.1 57.0 3.57 Example 7 Isothermal, upflow. all-vapor phase pilot plant runs were made on a HCN feedstock (85-237°C. 1760 wppm sulfur. 29.7 bromine number) at 288°C. 325 psig total inlet pressure, treat gas to oil of 1000 SCF/B. 80% hydrogen 20% methane treat gas and constant LHSV. A laboratory-prepared catalyst containing 5.2 wt.% M0O3 and 1.5 wt.% CoO on an alumina support with a 87 A median pore diameter was compared to a high-activity commercial CoMo catalyst, KF-742. Both catalysts were sulfided in situ with a 10% H2S/H2 gas blend at 371 °C for 15 hr and cooled to 93 °C before the introduction of the HCN feedstock. A comparison at constant conditions shows that the low-metal catalyst can achieve a sulfur removal level close to 90% while providing significantly less olefin hydrogenation (see Table VI). TABLE VI Wt.% Wt.% % Olefin Catalyst M0O3 CoO %HDS Hydrogenation Low-Metal Catalyst 5.2 1.5 87.7 28.9 Commercial KF-742 15 4 99.6 85.4 Example 8 Isothermal, upflow, all-vapor phase pilot plant runs were made on an ICN feedstock (71- 166°C. 978 wppm total sulfur. 49.7 bromine number, 49.1 API, 29 wppm total nitrogen) at 274°C. 200 psig total inlet pressure, 1000 SCF/B. 100% hydrogen treat gas and constant LHSV. Table VII shows a summary of the catalysts that were tested. Both Supports a and b were alumina. Each catalyst was sulfided in situ with a 10% H2S/H2 gas blend at 371 °C for 15 hr and cooled to 93 °C before the introduction of the ICN feedstock. After the introduction of the ICN feedstock, the catalysts were given 10-1 1 days to line- out. TABLE VII Edge Co/Mo Median Surface Plane Area Selective M0O3 CoO P Atomic Pore DiaConcentration Particle μmol O-1 Factor Catalyst Support wt.% wt.% wt.% Ratio meter. A g MoO m- Size. A g MoO- (x l O) E a 4.2 1.2 - 0.55 87 1.49 x l O **4 1 .3 mm 761 5.1 F a 6.1 1.5 - 0.47 87 1.99 x lO "4 1.3 mm 1885 5.0 G b 5.0 1.5 - 0.57 84 1.74 x l O **4 1 /16 in 2560 5.2 H b 5.0 1.7 0.53 0.64 84 1.78 x l O "4 1 /16 in 1348 5.3 Figure 1 hereof shows a plot of the HDS relative activity versus the metal sulfide edge plane area for the catalysts described in Table VII above. The relative HDS activity was calculated for each catalyst based on a weight M0O3 basis using 1.33 order kinetics and then normalized to the value for the commercial Catalyst E (which was given the value of 100). Since the selectivitλ factors in Table VII are approximately constant, it is apparent that obtaining metals dispersions higher than about 800 and lower than about 2800 μmol 02 g M0O3 results in catalysts that have higher HDS activity per weight of M0O3 than the base Catalyst E yet retain the same high selectivity. The HDS activity per weight of M0O3 appears to be maximized between about 1200 and 2000 μmol 02 g M0O3. Example 9 A FICN feedstock (99-232°C. 2200 wppm sulfur. 21.1 bromine number) was processed in a commercial hydrotreating unit with a fixed bed of a new commercial catalyst of this invention ( 1.3 mm asymmetric quadrilobe. 4.2 wt.% M0O3. 1.2 wt.% CoO. alumina support with 87 A median pore diameter). The catalyst was sulfided prior to hydrotreating the HCN feedstock according to a standard commercial practice. Table VIII below summarizes two conditions. Condition A is a case in which the reactor inlet temperature was greater than the calculated inlet dew point temperature whereas Condition B is a case where the reactor inlet temperature was lower than the calculated dew point. From Conditions A to B. the dew point at the inlet changed as a result of increasing the space velocity by a factor of 2.3 and increasing the reactor pressure 45 psig with the hydrogen flowrate approximately constant. The temperature rise for Condition B shows that the product at the reactor outlet was completely vaporized, i.e.. the operation went through the dry point in the reactor bed. TABLE VIII Gas to Oil Inlet Reactor Condiratio Temp.. Inlet Dew ΛTemp, T DP /T IN %OlefinH Selectivity RON MON tion # SCF/B °C Point. °C °C ( /R) %HDS ydro Factor (x 10) Loss Loss A 2000 374 249 46 0.954 97 83 1.0 4.5 1 9 B 950 277 285 7.2 1.015 93 33 2.7 1 .0 0.3 Table VIII shows that the HDS levels for the two conditions were close while the olefin hydrogenation was significantly different (83% for Condition A versus 33% for Condition B). This corresponds to a factor of 2.7 increase in the selectivity factor for Condition B versus Condition A. The large olefin hydrogenation reduction resulted in significant octane savings of 3.5 RON and 1.6 MON while the HDS level was maintained at greater than 90%. Note that the road octane loss. (ΔRON+ΔMON)/2. was only 0.65 at 93% HDS. Significant hydrogen consumption savings were also realized from the lower olefin hydrogenation level. Example 10 A HCN feedstock (99-232°C, 2200 wppm sulfur. 21.1 bromine number) was processed in a commercial hydrotreating unit with a fixed bed of a new commercial catalyst of this invention (1.3 mm asymmetric quadrilobe, 4.2 wt.% M0O3, 1.2 wt.% CoO, alumina support with 87 A median pore diameter). The catalyst was sulfided prior to hydrotreating the HCN feedstock according to a standard commercial practice. Table IX below summarizes ten conditions that were run over two months in the commercial unit. The total reactor pressure during this time was 280-350 psig while the LHSV varied by a factor of 2.85 over a base level. Table IX also lists the %>HDS and %OH which are values that were averaged over the period at each condition. TABLE IX Inlet Dew- Condition Gas to Oil Inlet Temp. Point Temp. T DP /T IN Selectivity Number Ratio, SCF/B °c (T, N ) °C (T DP ) (R/R) %HDS %OH Factor (x 10) 1 2000 263 249 0.974 94 75 0.9 2 2000 274 249 0.954 97 83 1.0 1500 274 263 0.980 97 68 1.5 4 1500 269 264 0.990 97 58 2.0 5 1450 266 268 1.005 93 42 2.0 6 1000 274 282 1.015 93 45 1 .8 7 820 288 296 1.015 93 46 1.8 8 950 277 285 1.015 93 33 2.7 9 760 291 293 1.005 95 38 2.8 10 890 279 288 1.015 95 34 3.2 Conditions 1-3 above are at Trjp/Tjxj ratios below 0.990 and show low selectivity values of 1.5 or less. Conditions 4- 10 are at Tj)p/Tj sj ratios of 0.990 and greater and show selectivity values of 1.8 to 3.2. These data show that for a variety of commercial unit conditions using a catalyst of this invention, high selectivity values are obtained as long as the Trj)p/Tj \ f ratio is greater than or equal to 0.990. Example 11 A sample of catalyst of this invention and a conventional catalyst was used for this example. The catalyst of this invention was comprised of 4.2 wt.% M0O3, 1.2 wt.% CoO, on an alumina support having a median pore diameter of about 87A. The conventional catalyst was a catalyst designated KF- 742 and available from Akzo Nobel, and was comprised of about 15 wt.% M0O3, 4 wt.% CoO on an alumina support having a median pore diameter of about 72A. Both catalysts were tested in a 1.3 mm asymmetric quadrilobe size. Each catalyst was sulfided in situ with a 10%> H2S/H2 gas blend for approximately 16 hrs at two holding temperatures, 232°C and 371°C. and cooled to 93°C before introduction of naphtha feed. All tests were preformed in isothermal, upflow, all vapor phase pilot units. The two stacked bed tests and the full charge of RT-225 and KF-742 were tested with a Baton Rouge heavy cat naphtha feed having a 72-246°C boiling range, 2321 wppm total sulfur, and 23.5 bromine number. Two stacked bed volume percent loadings were compared, 87/13 and 74/26, of RT-225 (inlet)/KF-742 (outlet). All tests were performed at reactor conditions of 260/277/293°C, 2600 scf/b, 100%o hydrogen treat gas and 300 psig total inlet pressure. Space velocity was held constant at 6.5 LHSV, Figure 1 plots %HDS versus %>OS from the four runs. Selectivity is shown directly by plotting percent HDS versus the percent olefin saturation. Figure 1 show equivalent selectivity for the stacked beds when compared with RT-225. And significantly improved selectivity for the stacked beds versus KF-742 alone. Equivalent selectivity means that the catalysts will give similar olefin saturation at a constant HDS level. An example taken from Figure 1 shows both the stacked beds and RT-225 are saturating about 28% olefins at 95%o HDS while KF-742 saturates approximately 35%. Figure 2 shows stacked catalyst beds containing RT-225 and KF- 742 with significant HDS activity improvements over the reference case of a 100% RT-225 loaded reactor. The relative volumetric activity for the 87 vol.% RT-225/13 vol. KF-742 stacked bed was 180 and for the 74 vol.% RT-225/26 vol.% KF-742 stacked bed 200. KF-742 was added as the second (outlet) catalyst in a stacked bed configuration with HDS selective RT-225 in the inlet, to increase the overall HDS performance of the catalyst system.

Claims: CLAIMS: 1. A two stage process for hydrodesulfurizing a naphtha feedstock, which process comprises: i) reacting said feedstock in a first reaction stage under hydrodesulfurization conditions in contact with a catalyst is comprised of: (a) about 1 to 10 wt.% M0O3; and (b) about 0.1 to 5 wt.% CoO; and (c) a Co/Mo atomic ratio of about 0.1 to 1.0; and (d) a median pore diameter of about 60 A to 200 A; and (e) a M0O3 surface concentration in g Moθ3/m2 of about 0.5 x lO" 4 to 3 x 10-4; and (g) an average particle size diameter of less than about 2.0 mm; and ii) passing the reaction product of the first stage to a second stage, also operated under hydrodesulfurization conditions in contact with a catalsyt comprised of at least one Group VIII metal selected from the group consisting of Co and Ni, and at least one Group VI metal selected from the group consisting of Mo and W. more preferably Mo. on an inorganic oxide support material. 2. The process of claim 1 wherein the amount of M0O3 is from about 2 to 8 wt.%. and the amount of CoO is from about 0.5 to 4 wt.%, and the inorganic support material is selected from the group consisting of alumina, silica, and silica-alumina. 3. The process of claim 2 where the Co/Mo atomic ratio is from about 0.20 to about 0.80 and the median pore diameter is from about 75 A to about 175 A. 4. The process of claim 3 wherein the catalyst has a metal sulfide edge plane area of from about 800 to 2800 μmol oxygen/g M0O3 as measured by oxygen chemisorption and the M0O3 surface concentration is from about 0.75 x l0- 4 to about 2.5 x 10 "4. 5. The process of claim 4 wherein the process unit is operated such that the inlet temperature of the feedstock to the reaction unit is below the dew- point of the feedstock and 100% of the feedstock becomes vaporized in the catalyst bed. 6. The process of claim 5 wherein the amount of M0O3 is from about 4 to 6 wt.%, and the amount of CoO is from about 1 to 3 wt.%, and the inorganic support material is selected from the group consisting of alumina, silica, and silica-alumina. 7. The process of claim 6 where the Co/Mo atomic ratio is from about 0.25 to about 0.72 and the median pore diameter is from about 80 A to about 150 A. 8. The process of claim 7 wherein the M0O3 surface concentration is from about l x lO" 4 to about 2 x 10 _4 g MoO3/m 2 .

Inventors: BRIGNAC GARLAND BARRY, COKER JOHN CALVIN, KAUFMAN JEFFREY LAWRENCE, BRIGNAC, GARLAND, BARRY, COKER, JOHN, CALVIN, KAUFMAN, JEFFREY, LAWRENCE
Applicants: EXXON RESEARCH ENGINEERING CO, EXXON RESEARCH AND ENGINEERING COMPANY
Application year: 1999
Main classification: C01G45
IPC codes: B01J23, B01J35, C10G45, C10G65