SUPERHIGH TEMPERATURE AND PRESSURE STEAM TURBINE

Abstract: In a superhigh temperature and pressure steam turbine including a casing, blades in the casing receiving streams of steam jets for rotation, and a rotor shaft supporting the blades for rotation, wherein the casing includes an inner casing member having static blades secured thereto for guiding the streams of steam jets and an outer casing member enclosing the inner casing member, the rotor shaft is formed of an alloy consisting essentially, by weight, of less than 0.04% C, not more than 2% Mn, not more than 1.5% Si, 10-20% Cr, 20-30% Ni, 0.5-3% Mo, 0.5-3% Ti, 0.1-0.5% Al, 0.002-0.01% B and the balance Fe and inevitable impurities. The alloy has a microstructure in which a γ′ phase is precipitated in austenite matrix, whereby the rotor shaft has superior high temperature creep strength and excellent thermal fatigue resistant property.

Description: SUPERHIGH TEMPERATURE AND PRESSURE STEAM TEE INE BACKGROUND OF THE INVENTION This invention relates to novel steam turbines, and more particularly it deals with a superhigh temperature and pressure steam turbine operating at a steam temperature of 6000 to 6500C and under a steam pressure of 4000 to 50S psi which turbine is superior in thermal fatigue resistant property. Owing to petroleum shortage and a consequent rise in the price of petroleum, it has been taken to consideration to raise the temperature and pressure of steam used in generating plants so as to increase efficiency. In steam generating plants, it is now usual practice to operate the turbine under a steam condition of 5380 C, and the rotor shaft is formed of low alloy steel such as a Cr-Mo-V steel. However, in a high temperature and pressure generating plant in which the turbine is operated at a steam temperature of over 6000C and under a pressure of over 4000 psi, it has been revealed that the material now used is not fit for use from the point of view of strength because it is markedly low in creep rupture strength, thermal fatigue strength and strength at high temperatures. Meanwhile steam turbines operating at a main steam temperature of over 6000C are disclosed in "Transaction of the ASME", October 1960, for example. However, this type of steam turbines are low in thermal fatigue resistant prop-erWy3 and not suitable for use as steam turbines that on operate at peak load. More specifically, when a steam turbine is repeatedly started up and shut down, the starting-up and ceasing impose severe thermal fatigue conditions. Thus it becomes necessary to provide a steam turbine having a rotor and rotor blades having a fatigue life that can withstand this transitory condition, high strength at elevated temperature and high ductility at elevated temperature. Austenitic alloys are considered suitable from the point of view of strength as materials for the rotor and rotor blades operating under conditions of a steam pressure exceeding 4000 psi and a steam temperature in the range over 6000C. However, these alloys have the risks that, since various deposit phases are precipitated at high temperature, embrittlement thereof would be accelerated and their strength would be markedly lowered at elevated temperature. SUMMARY OF THE INVENTION An object of this invention is to provide a steam turbine including a turbine shaft having superior thermal fatigue resistant property at a main steam temperature of 6000 to 6500 C. Another object is to provide a superhigh temperature and pressure steam turbine of high reliability, particularly a steam turbine of the type described including a rotor shaft formed of austenitic forged steel having high strength at elevated temperature, high ductility at elevated temperature and low thermal embrittlement under the steam condition of a temperature range between 6000C and 6500 C. Still another object is to provide-a steam turbine having a rotor- shaft and rotor blades of high thermal fatigue resistant property under the steam condition of a temperature range between 6000 and 6500C. According to the invention, there is provided a superhigh temperature and pressure steam turbine comprising a casing, rotor blades in the casing receiving steam jet streams for rotation and a rotor shaft in the casing supporting the rotor blades for rotation, said casing including an inner casing member supporting static blades for guiding the steam jet and an outer casing member having a substantially spherical external shape enclosing the inner casing member, wherein the rotor shaft and the rotor blades are formed of austenitic steel having 1000 hour creep rupture strength of over 25 kg/mm2 at 6500C and have high thermal fatigue resistant strength. The blade sections of the-rotor shaft are preferably equidistantly located axially of the rotor shaft in the casing and are preferably unsymmetrical at the center position with respect to the axial direction. The outer casing member is preferably formed Qf Cr-Ni austenitic cast steel or Cr-Mo-V cast steel having a bainite structure. The inner casing member is preferably formed of Cr-Ni austenitic cast steel. The rotor shaft is made of austenitic forged steel consisting essentially by weight of less than 0.04% C , not more than 2% Mn, not more than 1.5% Si, 10-20% Cr, 20-30% Ni, 0.5-3% Mo, 0.5-3% Ti, 0.5-1% Al, 0.0020.01% B and the balance Fe and having a y' phase precipitated in the austenite matrix. Such rotor shaft has 1000 hour creep rupture strength of not less than 25 kg/mm2 and excellent thermal fatigue resistant property at 6500 C. The rotor shaft is preferably formed of austenitic forged steel consisting essentially by weight of 0.015-0.03% C, 0.5-1.5% Mn, 0.3-1% Si, 14-17% Cr, 24-28% Ni, 1-2% Mo, 1.5-2.5% Ti, 0.15-0.4% Al, 0.004 0.008 B and the balance Fe and having a y' phase precipitated in the austenite matrix. Further, it is preferred to add vanadium of 0.05-0.5 wt in the steel alloy of the rotor, and more preferably 0.2-0.3% vanadium is added. The rotor blades of the superhigh temperature and pressure turbine according to the invention consist essentially by weight of 0.01-0.1% C, not more than 1.5% Si, not more than 2% Mn, 10-20% Cr,¯20-30% Ni, 0.5-3% Mo, 1.5-3% Ti, 0.1-0.5% Al, 0.002-0.01% B and the balance Fe. Preferably the rotor blades consist essentially by weight of 0.04-0.7% C, 0.5-1.5 Mn, 0.3-1% Si, 14-17% Cr, 24-28% Ni, 1-2% Mo, 1.5-2.5% Ti, 0.15-0.4% Al, 0.004-0.008% B and the balance Fe and inevitable impurities. Further, it is preferred to add vanadium of 0.05-0.5 wt% in the steel alloy of the rotor blade, and more preferably 0.2-0.3% vanadium is added. The rotor shaft and the rotor blades of the superhigh temperature and pressure steam turbine according to the invention preferably have, with respect to the aforesaid chemical composition. the following Ni equivalent and Cr equivalent: Ni equivalent ENi (%) + ((30 x C (%))) + ((0.5 x Mn (%)))] = 23 - 29 Cr equivalent [Cr (%) + Mo (%) + ((1.5 x Si (%)))] = 12 - [(7/10 x Ni equivalent) +9] The reasons why the elements are limited to the respective ranges of values in the aforesaid composition are as follows: Carbon Strength at elevated temperature increases with an increase in C but a reduction in toughness and thermal embrittlement are accelerated with an increase in C. The carbon content in the material of the rotor shaft that increases strength at elevated temperature without reducing toughness nor thermal embrittlement is less than 0.04%, more preferably between 0.015 and 0.03%, and the carbon content of material of the rotor blades is 0.010.1%, preferably between 0.04 and 0.07 - Manganese This element is the most important deoxidizing component in production. However, when the elment fls too large in amount, toughness and oxidation reslstar:cc are adversely affected. Thus the amount is limitted to be not more than 2%, preferably between 0.5 and 1.5* Nickel This element is an important component for improving high temperature mechanical strength of the steel according to the invention, particularly creep rupture strength and thermal fatigue life thereof. More specifically, this element is conducive to formation of a stable austenite structure and increased high temperature strength. However, in view of its expensiveness and the high temperature ductility and yield strength of the steel being reduced when its amount is too high, the amount is limitted between 20 and 30%, preferably between 24 and 28%. Silicon Similarly to manganese, this element is a deoxidizing component necessary for production. When the amount is over 1.5%, however, the forgibility of the steel diminishes and its high temperature toughness is reduced. Thus the upper limit is 1.5 wt, preferably between 0.3 and 1%. Molybdenum This element improves creep rupture strength by strengthening the austenite matrix and forming a carbide. However, the steel has its high temperature ductility reduced and its workability deteriorates when the amount of the element is too large. Thus the amount is limitted between 0.5 and 3 wt%, preferably between 1 and 2%. Chromium This element is an important component for improving the high temperature oxidization property of the material according to the invention. As shown in Fig. 1 (b), no satisfactory effect is achieved if the amount is under 10%. When the amount is over 20%, embrittlement increases after prolonged holding at elevated temperature. The amount is thus preferably between 14 and 17%. Titanium Besides being used as a deoxidizing agent, this element has the effect of hardening alloys by the precipitation thereof pounds. However, when the amount exceeds 3%, the element reduces the ductility and toughness of the steel and accelerates notch deterioration. To increase the high temperature strength of the steel, it is necessary that the amount of this element be not less than 0.5%. Preferably the amount is between 1.5 and 2.5. Aluminium Aluminium is added as a deoxidizing agent in the amount of 0.1-0.5%. Preferably in 0.15-0.4 . This element is combined with titanium to cause precipitation of an intermetallic compound, to thereby increase high temperature -strength. However, when the amount is too great, it tends to reduce strength. Thus the amount thereof is limitted between 0.1-0.5. Boron This element has the effects of markedly strengthening grain boundary and providing hi tempers ductility. However, workability deteriorates when the amount is too large. Thus the amount is limitted between 0.002 and 0.01%, preferably between 0.004 and 0.008%. Vanadium This element is added to improve creep strength. When the amount thereof is below 0.05%, no satisfactory effect is achieved. When the amount is over 0.5%, however, ductility and toughness are both adversely affected. The amount is preferably between 0.2 and 0.3%. Nickel Equivalent Fig. 7a shows the relation between the nickel equivalent (% Ni + 30 x % C + 0.5 x &num; Mn) regarding an austenite heat resisting steel now in use and the 1000 hour creep rupture strength obtained at 6500 C. As shown, an increase in the nickel equivalent is accompanied by an improvement in creep rupture strength. This relation tends to be saturated with the nickel equivalent being about 35%. If the 1000 hour creep rupture strength at 6500C used as a target is made to agree with the scatter band value of 26-34 kg/mm2 (1000 hour creep rupture strength at 5500C) now used for the currently used material, then the optimum value of the nickel equivalent is between 23 and 29%. Chromium Equivalent Chromium equivalent is 12 < (% Cr equivalent) # 7/10 x (% nickel equivalent) + 9. Fig. 7b shows the relation between the chromium content and the increment for high temperature oxidation. Fig. 7b shows that the chromium content should be not less than 12% if its addition is to have any effect in oxidization resistance at elevated temperature. Fig. 7c shows the result obtained with the relation shown in Fig. etb and the optimum range of the aforesaid nickel equivalent as inserted in Shefla's diagram. In Fig. 7c, if the upper limit of the chromium equivalent is set corresponding to the nickel equivalent on condition that a stable austenite structure is obtained, then the value is 7/10 x (% nickel equivalent) + 9 (see Fig. 7c) according to Shefla's diagram. The hatching in Fig. 7c indicates the nickel equivalent and chromium equivalent as limited by the invention. Additional and other objects, features and advantages of the invention will become apparent from the description set forth hereinafter when considered in conjunction with the accompanying drawings. For producing the alloys noised in the present invention, it is preferred to effect melting by use of argon-oxygen blowing decarburization process or vacuum decarburization process. BRIEF DESCRIPTION OF THE DRAWINGS Fig. 1 is a schematic view of one example of the superhigh temperature and pressure steam turbine according to the invention; Fig. 2 is a diagrammatic representation showing a relation between absorbed energy and the amount of C in the material according to the invention; Fig. 3 is a diagrammatic representation of the working stress caused in the rotor shaft according to the operation pattern of the steam turbine now in use; Fig. 4a is a notional view of the turbine rotor surface temperature-strain (stress) pattern of the steam turbine in actual use; Fig. 4b is a view showing a model of a high temperature low cycle fatigue pattern simulating the thermal fatigue operation pattern of Fig. 4a which model is a strain-holding type; Fig. 4c is another model of the fatigue pattern similar to Fig. 4b in which model the strain-holding time is removed; ; Fig. 5 is a diagrammatic representation of the results of high temperature low cycle fatigue tests cone ducted on the materials according to the invention and material of the prior art; Fig. 6 is a diagrammatic representation of the influence of born exerted on the high temperature low cycle fatigue life; Fig. 7a is a diagrammatic representation of the relation between creep rupture strength and nickel equivalent; Fig. 7b is a diagrammatic representation of the relation between high temperature oxidization increment and the amount of chromium; Fig. 7c is a Shefla's diagram; Fig. 8 is a diagram showing the 103 hour creep rupture strength of the material according to the invention and the material of the prior art as extrapolated by the Rallson-Mirror process; ; Fig. 9 is a diagrammatic representation of the high temperature low cycle fatigue of the material according to the invention and the material of the prior art; and Fig. 10 is a microscopic photograph of the specimen structure. DESCRIPTION OF THE PREFERRED EMBODIMENT Fig. 1 is a sectional view showing the essential portions of one embodiment of the superhigh temperature and pressure steam turbine in conformity with the invention, in which steam is introduced through a main steam line 1 into the turbine and is jetted in a predetermined direction by static blades 3 attached to an inner casing member 2 to thereby rotate rotor blades 5 mounted on a rotor shaft 4. After doing work, the steam flows through a gap between an outer casing member 6 and the inner casing member 2 and then is exhausted through a cooled steam outlet port 7, an exhaust outlet port 8 and an auxiliary exhaust outlet port 9. The exhausted steam is forwarded to a next steam turbine operating at a lower temperature. 10 is the center of each bearing of th rotor shaft 4. 11 and 12 are a gland and a intermediate gland leak outlet port respectively. 13 is a nozzle box Arrows indicate the direction of flow of the steam. The embodiment of the invention of the aforesaid construction will be described in detail with reference to the inner casing member 2 and the outer casing member 6 formed of Cr-Ni austenite cast steel and Cr-Ni austenite forged steel, respectively. Example 1 Table 1 shows the chemical composition of alloys used in experiments. Each of the alloys used in the present invention is prepared by the steps of vacuum are melting, forging, solid-solution treatment of holding it at 9800C for one hour with water-cooling thereafter, and aging treatment of holding at 7200C for 16 hours with air-cooling being effected thereafter, while each of the conventional alloys for comparison is prepared by the steps of vacuum are melting, forging and succeeding necessary treatments shown hereinbelow. The alloys used in the present invention has a microstructure in which a y' phase is precipitated in the austenite matrix. Conventional Cr-Mo-V steel serving as a conparative material was cooled by air-blowing after heating at 9700C for 15 hours, and then reheated at 67o0C for 48 hours before being cooled in the furnace. 12 Cr steel also serving as another comparative material was cooled by spraying of water in atomized particles after heating at 10500C for 24 hours, and then subjected to tempering at 6500C for 20 hours. These steel alloys were subjected to V-notch Charpy impact tests and creep rupture tests. Fig. 2 shows the results of impact tests conducted on the influences of the amount of C on thermal embrittlement by heating at 6500C for 1500 hours. The results show that, whereas absorbed energy of non-heat treated blanks is substantially constant irrespective of the amount of C, the absorbed energy reduces as the amount of C increases in the material heated at 6500C for 1500 hours, showing a marked thermal embrittlement in material with high C content. The values of absorbed energy at 200 C for 12 Cr steel and Cr-Mo-V steel which are now in use for producing rotors are specified as not less than 1.1 kg - m and 0.69 kg - m respectively. Particularly, in a case where the amount of C is not more than 0.03% by weight, the absorbed energy becomes not less than 1.5 kg - m, that is, superior thermal embrit tlement resistant property can be obtained. The thermal embrittlement resistant property of each alloy used as a material of the turbine shaft in the present invention is larger than those of the conventional 12 Cr steel and Cr-Mo-V steel. In the rotor shaft material for the steam turbine according to the invention, intracrystalline rupture (white triangle) prevailed when the material had a C ccntent of below 0.04 wt%. However, when the C content had a value not less than 0.04 wt, the rupture form has transferred to a grain boundary rupture type (black triangle). The results of analysis have shown that this change in rupture type is accounted as the deterioration of the grain boundary due to precipitation of the Mx type and M23C6 type carbides in the grain boundary. Thus, to diminish thermal embrittlement in interrelation with thermal fatigue, the amount of C is limitted to be less than 0.04%, preferably between 0.015 and 0.03% in the material for rotor shafts according to the invention. Table 1 EMI15.1 <SEP> Chemical <SEP> Composition <SEP> (wt%) <tb> <SEP> C <SEP> Si <SEP> Mn <SEP> Ni <SEP> Cr <SEP> Mo <SEP> V <SEP> Al <SEP> Ti <SEP> B <SEP> Fe <tb> Inven- <SEP> No. <SEP> 1 <SEP> 0.03 <SEP> 0.70 <SEP> 1.35 <SEP> 25.78 <SEP> 15.92 <SEP> 1.23 <SEP> 0.29 <SEP> 0.14 <SEP> 2.23 <SEP> 0.0055 <SEP> Bal. <tb> tive <SEP> No. <SEP> 2 <SEP> 0.02 <SEP> 0.69 <SEP> 1.21 <SEP> 25.98 <SEP> 15.79 <SEP> 1.24 <SEP> 0.31 <SEP> 0.14 <SEP> 2.36 <SEP> 0.0057 <SEP> " <tb> steel <SEP> No. <SEP> 3 <SEP> 0.040 <SEP> 0.70 <SEP> 1.30 <SEP> 25.80 <SEP> 15.84 <SEP> 1.25 <SEP> 0.30 <SEP> 0.15 <SEP> 2.11 <SEP> 0.0049 <SEP> " <tb> <SEP> No. <SEP> 4 <SEP> 0.048 <SEP> 0.74 <SEP> 1.35 <SEP> 25.75 <SEP> 15.86 <SEP> 1.25 <SEP> 0.32 <SEP> 0.15 <SEP> 2.98 <SEP> 0.0050 <SEP> " <tb> Steel <SEP> 12 <SEP> Cr <SEP> 0.16 <SEP> 0.40 <SEP> 0.71 <SEP> 0.51 <SEP> 10.73 <SEP> 0.98 <SEP> 0.21 <SEP> - <SEP> - <SEP> - <SEP> " <tb> of <SEP> Cr The <SEP> Mo-V <SEP> 0.28 <SEP> 0.26 <SEP> 0.78 <SEP> 0.36 <SEP> 1.16 <SEP> 1.30 <SEP> 0.25 <SEP> - <SEP> - <SEP> - <SEP> " <tb> Prior <tb> Art <tb> Fig. 3 shows an operation pattern of the severest condition for conventional steam turbines that is operated at a steam temperature of 5660C, that is, the starting-up and shutting-down of the turbine is repeated every 12 hours. When this operation pattern is applied to the superhigh temperature and pressure steam turbine according to the invention, the rotor shaft would be subjected to harsh low cycle fatigue due to high stress at the time of startup and shutdown as shown. Particularly the rotor shaft, unlike the rotor blades, would be subjected to harsh low cycle fatigue due to the combined actions of thermal stress and centrifugal stress because a rise in temperature is gradual in the rotor. Also, it would be subjected to creep due to centrifugal forces in steadystate operation. In Fig. 3, working stress represents thermal stress combined with centrifugal stress Table 2 shows the results of tension tests, creep rupture tests and low cycle fatigue tests conducted on the steel according to the invention at 6500C and on the steel of the prior art at 5500C. It will be seen in the table that the material according to the invention is. equal to or higher than the Cr-Mo-V steel in tensile strength and 0.2% yield strength, and that the rate of elongation thereof is 1.5 to 1.75 times as high as in the Cr-Mo-V steel. Creep rupture strength is 1.1 to 1.20 times as high in the material according to the invention as in the Cr-Mo-V steel and low cycle fatigue is equal to or slightly higher in the former than in the latter in spite of the difference of test temperature. The results of the low cycle fatigue tests represent the number of repetition continued until rupture occurs at a strain rate of 0.1%/second and strain amounts of 1.0% and 0.65% without holding strain (, that is, in the same manner as shown in Fig. 4c). Table 2 EMI18.1 Items <SEP> of <SEP> Tests <SEP> Prior <SEP> art <SEP> Invention <tb> <SEP> Cr-Mo-V <SEP> 12 <SEP> Cr <SEP> No. <SEP> 1 <SEP> No. <SEP> 2 <SEP> Cr-Mo-V <tb> <SEP> Steel <SEP> Steel <SEP> Steel <tb> High <SEP> Tensile <SEP> strength <SEP> 77.3 <SEP> - <SEP> 86.5 <SEP> 85.4 <SEP> 1.11 <tb> temp- <SEP> (kg/mmê) <tb> rature <SEP> Yield <SEP> strenght <SEP> 59.8 <SEP> - <SEP> 66.6 <SEP> 68.1 <SEP> 1.11-1.14 <tb> tension <SEP> (kg/mmê) <tb> <SEP> Elongation <SEP> 14 <SEP> - <SEP> 24.5 <SEP> 21.2 <SEP> 1.51-1.75 <tb> <SEP> (%) <tb> <SEP> Reduction <SEP> of <SEP> 40 <SEP> - <SEP> 43.0 <SEP> 32.2 <SEP> 0.81-1.08 <tb> <SEP> Area <SEP> (%) <tb> Creep <SEP> 1000 <SEP> Hour <SEP> strength <SEP> 27 <SEP> 32 <SEP> 32 <SEP> 34 <SEP> 1.19-1.26 <tb> rutpure <SEP> (kg/mm2) <tb> <SEP> 2000 <SEP> Hour <SEP> strength <SEP> 25 <SEP> 330 <SEP> 29 <SEP> 30 <SEP> 1.16-1.20 <tb> <SEP> (kg/mm2) <tb> High <SEP> = <SEP> 1.0% <SEP> 700 <SEP> - <SEP> 770 <SEP> 639 <SEP> 0.91-1.10 <tb> tempera- <SEP> (Times) <tb> ture <SEP> = <SEP> 0.65% <SEP> 3000 <SEP> - <SEP> 3520 <SEP> 3110 <SEP> 1.04-1.17 <tb> low <SEP> cycle <SEP> (Times) <tb> fatigue <tb> From the foregoing, it will be appreciated that the material according te the invention which is used at a temperature of 6500C me--ts requirements regarding mechanical strength requited in the case of Cr-Mo-V steel used at present at 5500C. Thus it has been made clear that the material described above can be used for forming the rotor shaft of a superhighp temperature and pressure steam turbine operating a at a steam temperature of 6000-6500C and under a steam pressure of 4000-5000 psi. Example 2 Table 3 shows i chemical composition (wt%) of materials for forming the rotor blades used in the superhigh temperature and pressure steam turbine according to the invention. Each material has been obtained by performing vacuum arc melting, forging, and grain size regulation into a range C ASTM G.S. 2.5 - 4 was effected by holding it at 10500C tDr 3 hours. Then each material was water--cooled to room temperature in the same manner as in Example 1 after hanng been subjected to solid solution treatment of holding it at-8990C for 2 hours. Then, each material was subjected aging treatments of two steps, i.e*, first step was the holding it at 7600C for ;6 hours with air-cooling thereafter and the second step was the holding at 7180C for 6 hours with air-cooling thereafter. The blanks obtained by processing the materials through the aforesaid treatments had a micro structure having a y' phase precipitated in the austenite matrix. The blanks were machined to provide test pieces of predetermined dimensions. Generally, the blades of a steam turbine are directly subjected to the jetted steam, so that their temperatures rise relatively quickly after the steam turbine is actuated and becomes equal to that of steam. Meanwhile a rise in the temperature of the rotor shaft is relatively slow after the commencement of actuation of the steam turbine because it has a high thermal capacity and austenite steel has a low thermal conductivity. Thus the relatively large difference in temperature between the blades and rotor shaft exists for a substantial period of time. Because of this, the working stress (thermal stress plus centrifugal stress) to which the rotor shaft is subjected is very high at starting-up or ceasing (or when transferring to idling) as shown in Fig. 3, with the result that the thermal fatigue suffered by the blades is relatively lower than that suffered by the rotor shaft. Thus the amount of C for the materials of the blades is limitted between 0.01 and 0.1%, preferably between 0.04 and 0.07. Fig. ha shows a conceptual pattern of a relation between temperature and strain (stress) to which the surface of the rotor is subjected in the steam turbine of superhigh temperature and pressure according to the invention having the blades referred to hereinabove and the rotor shaft described by referring to Example 1. To assess the thermal fatigue life experimentarily, the operation conditions shown in Fig. 4a were converted to a trapezoidal strain cycle (constant temperature) with strain-holding (Fig. 4b), and a tension-compression triangular wave form (constant temperature) without strain-holding (Fig. 4c). The aforesaid conversion has been made on the basis of the hypothesis that there is a correlation between a thermal fatigue phenomenon (varying temperature) and a low cycle fatigue phenomenon (constant temperature). Fig. 5 is a diagram showing the results of high temperature low cycle fatigue tests conducted by controlling strain of gauge length at a strain rate of 0.1%/sec and at a temperature of 6500C. As shown, it will be seen that the materials of the invention containing 0.002-0.008% B has about twice as long service life as a conventional material containing no B in a low cycle region having a strain range of 0.5-1.2%, indicating that the addition of B has the effect of improving thermal fatigue resistant property. Table 3 EMI22.1 <SEP> Speci- <SEP> Chemical <SEP> Composition <SEP> (%) <tb> <SEP> men <tb> <SEP> No. <SEP> C <SEP> Si <SEP> Mn <SEP> Cr <SEP> Ni <SEP> Mo <SEP> V <SEP> Ti <SEP> B <SEP> Fe <SEP> Al <tb> Present <SEP> 5 <SEP> 0.04 <SEP> 0.44 <SEP> 1.41 <SEP> 15.05 <SEP> 25.56 <SEP> 1.37 <SEP> 0.31 <SEP> 0.17 <SEP> 0.008 <SEP> Bal. <SEP> 0.30 <tb> inven- <SEP> 6 <SEP> 0.04 <SEP> 0.44 <SEP> 1.41 <SEP> 15.05 <SEP> 25.56 <SEP> 1.37 <SEP> 0.31 <SEP> 2.17 <SEP> 0.006 <SEP> " <SEP> 0.30 <tb> tion <SEP> 7 <SEP> 0.04 <SEP> 0.44 <SEP> 1.41 <SEP> 15.05 <SEP> 25.56 <SEP> 1.37 <SEP> 0.31 <SEP> 2.17 <SEP> 0.004 <SEP> " <SEP> 0.30 <tb> <SEP> 8 <SEP> 0.04 <SEP> 0.52 <SEP> 1.29 <SEP> 14.64 <SEP> 26.44 <SEP> 1.40 <SEP> 0.28 <SEP> 2.11 <SEP> 0.010 <SEP> " <SEP> 0.26 <tb> <SEP> 9 <SEP> 0.05 <SEP> 0.84 <SEP> 1.50 <SEP> 14.70 <SEP> 26.30 <SEP> 1.10 <SEP> 0.12 <SEP> 2.11 <SEP> 0.028 <SEP> " <SEP> 0.30 <tb> Prior <SEP> 0.058 <SEP> 0.23 <SEP> 1.27 <SEP> 14.70 <SEP> 26.12 <SEP> 1.40 <SEP> 0.32 <SEP> 2.23 <SEP> - <SEP> " <SEP> 0.27 <tb> art <tb> Fg. 6 shows the influences exerted on fatigue life by the amount of B at a temperature of 6500C and a strain speed of 0.1%/sec in a strain region of 1.0%. As shown, fatigue life has a peak in the vicinity of 0.006% B and is about twice as long as that of material contain ing B in an amount outside the range of the invention. From the foregoing, it will be appreciated that the blades for steam turbines according to the invention has superior thermal fatigue resistant property and a prolonged service life. Example 3 Materials were subjected to vacuum arc melting, forging and regulating of grain size under the same conditions as described in Example 1. Then the materials were subjected to solid solution treatment and aging under the heat treating conditions shown in Table 7, and machines to produce materials for blades and rotor shafts. The materials Nos. 10 and 11 are those used for producing blades, and the materials Nos. 12 and 13 are those used for producing rotor shafts. Tables--5 and 6 show the results of creep rupture tests and fatigue tests conducted on these materials, respectively. As shown in Fig. 4a, the strain and stress caused on the surfaces of the rotors when a steam turbine is operated are such that transient compressive (tensile) strain due to thermal stress occurs at the time of starting-up (or ceasing) at a point A, and tensile stress acts due to centrifugal forces when the operation proceeds to a steadystate condition, so that the operation condition becomes such state as shown at points B and C in the steadystate. Therefore the strain cycle was assessed experimentally from low cycle fatigue based on the triangular waves for the starting-up and ceasing and from creep rupture strength for steadystate operation. Table 4 EMI25.1 Tested <SEP> Chemical <SEP> composition <SEP> (wt%) <tb> materials <SEP> C <SEP> Si <SEP> Mn <SEP> Cr <SEP> Ni <SEP> Mo <SEP> V <SEP> Ti <SEP> B <SEP> Fe <SEP> Al <tb> Inven- <SEP> No. <SEP> 10 <SEP> 0.04 <SEP> 0.44 <SEP> 1.41 <SEP> 15.05 <SEP> 25.56 <SEP> 1.37 <SEP> 0.31 <SEP> 2.17 <SEP> 0.004 <SEP> Bal. <SEP> 0.30 <tb> tion <SEP> No. <SEP> 11 <SEP> 0.042 <SEP> 0.70 <SEP> 1.45 <SEP> 15.92 <SEP> 25.78 <SEP> 1.23 <SEP> 0.29 <SEP> 2.23 <SEP> 0.0055 <SEP> " <SEP> 0.14 <tb> <SEP> No. <SEP> 12 <SEP> 0.020 <SEP> 0.69 <SEP> 1.21 <SEP> 15.79 <SEP> 25.98 <SEP> 1.24 <SEP> 0.31 <SEP> 2.36 <SEP> 0.0057 <SEP> " <SEP> 0.14 <tb> <SEP> No. <SEP> 13 <SEP> 0.036 <SEP> 0.55 <SEP> 1.15 <SEP> 14.15 <SEP> 26.22 <SEP> 1.32 <SEP> 0.31 <SEP> 2.32 <SEP> 0.0082 <SEP> " <SEP> 0.25 <tb> Conven- <SEP> Crtional <SEP> Mo-V <SEP> 0.28 <SEP> 0.26 <SEP> 0.73 <SEP> 1.16 <SEP> 0.36 <SEP> 1.30 <SEP> 0.25 <SEP> - <SEP> - <SEP> - <SEP> mate- <SEP> steel <tb> rial <tb> Table 5 EMI26.1 Types <SEP> of <SEP> Rallson-mirror <SEP> parameter <SEP> (C <SEP> = <SEP> 20) <tb> steel <SEP> alloy <SEP> Stress <tb> <SEP> 43 <SEP> kg/mmê <SEP> 40 <SEP> 33 <SEP> 30 <SEP> 27 <SEP> 23 <SEP> 15 <SEP> 12 <tb> No. <SEP> 11 <SEP> - <SEP> 37.2 <SEP> 38.2 <SEP> - <SEP> 38.9 <SEP> - <SEP> - <SEP> No. <SEP> 12 <SEP> 37.3 <SEP> - <SEP> 38.5 <SEP> - <SEP> 39.1 <SEP> - <SEP> - <SEP> No. <SEP> 13 <SEP> - <SEP> 36.9 <SEP> 38.1 <SEP> 38.4 <SEP> 38.3 <SEP> 39.4 <SEP> 40.6 <SEP> 41.7 <tb> Table 6 EMI27.1 Types <SEP> of <SEP> Temperature <SEP> Strain <SEP> speed <SEP> Fatigue <SEP> life <SEP> times <tb> steel <SEP> alloy <SEP> ( C) <SEP> % <SEP> sec <SEP> Strain <SEP> range <SEP> = <SEP> 1.0 <SEP> % <SEP> 0.65% <tb> No. <SEP> 11 <SEP> 650 <SEP> 0.1 <SEP> 800 <SEP> 3600 <tb> No. <SEP> 12 <SEP> 650 <SEP> 0.1 <SEP> 700 <SEP> 3200 <tb> Table 7 EMI27.2 Heat <SEP> treatment <SEP> Solid <SEP> solution <SEP> treatment <SEP> Aging <tb> <SEP> A <SEP> 760 <SEP> C <SEP> x <SEP> 16 <SEP> h#A#C <tb> (Applied <SEP> to <SEP> No. <SEP> 10) <SEP> 900 <SEP> C <SEP> x <SEP> 2 <SEP> h#W#Q <SEP> +720 <SEP> C <SEP> x <SEP> 6 <SEP> h#A#C <tb> <SEP> B <tb> (Applied <SEP> to <SEP> No. <SEP> 11) <SEP> 980 <SEP> C <SEP> x <SEP> 1 <SEP> h#W#Q <SEP> 720 <SEP> C <SEP> x <SEP> 16 <SEP> h#A#C <tb> Fig. 8 shows the results of extrapolation 't;?' the creep rupture strength of 105 hours conducted by the Rollson-Mirror process. According to this relation, t materials Nos. 10, 11 , 12 and 13 covered by the claims of the invention have strength of about 133 MPa at 6500C which is similar to mean creep rupture strength of 127 MPa of the conventional Cr-Mo-V steel tested at 5500C for comparison. Fig. 9 shows the results of high temperature low cycle fatigue tests effected by controlling strain of gauge length, at a strain rate of 0.1%/sec. The results show that in the entire strain range the fatigue life of the materials according to the present invention at 6500C is equal to or longer than that of the Cr-Mo-V steel at 5500C. Fig. 10 is a microscopic photograph at 2 magnification 1000x of the No. 1 alloy having a microstructure in which a y' phase is precipitated in the austenite matrix. The alloy according to the invention has high temperature strength required of the materials for the blades and the rotor operating at a steam temperature of 6000-6500C and is suitable for use as materials for the rotor blades and the rotor. Example 4 Alloys having chemical compositions shown in Table 8 were produced in the same manner as Example 1. Table 8 EMI29.1 <SEP> C <SEP> Mn <SEP> Si <SEP> Cr <SEP> Ni <SEP> Mo <SEP> V <SEP> Fe <SEP> Ti <SEP> Al <SEP> B <SEP> S <SEP> P <tb> No. <SEP> 14 <SEP> 0.038 <SEP> 1.30 <SEP> 0.38 <SEP> 15.04 <SEP> 26.00 <SEP> 1.21 <SEP> 0.32 <SEP> Bal <SEP> 1.95 <SEP> 0.23 <SEP> 0.0039 <SEP> 0.0001 <SEP> 0.003 <tb> No. <SEP> 15 <SEP> 0.037 <SEP> 1.32 <SEP> 0.36 <SEP> 15.04 <SEP> 26.17 <SEP> 1.18 <SEP> 0.29 <SEP> Bal <SEP> 1.61 <SEP> 0.19 <SEP> 0.0035 <SEP> 0.001 <SEP> 0.003 <tb> No. <SEP> 16 <SEP> 0.021 <SEP> 1.30 <SEP> 0.36 <SEP> 15.13 <SEP> 26.08 <SEP> 1.19 <SEP> 0.31 <SEP> Bal <SEP> 2.01 <SEP> 0.22 <SEP> 0.0043 <SEP> 0.001 <SEP> 0.003 <tb> No. <SEP> 17 <SEP> 0.020 <SEP> 1.28 <SEP> 0.36 <SEP> 14.72 <SEP> 25.96 <SEP> 1.27 <SEP> 0.30 <SEP> Bal <SEP> 1.66 <SEP> 0.20 <SEP> 0.0045 <SEP> 0.001 <SEP> 0.003 <tb> Figs. 11 and 12 show a relation between J ç rY temperature and tensile strength and another relat between aging temperature and creep rupture time at ç regarding the above-described alloys of the present invention, respectively. As apparent from Figs. 11 and 12, low aging temperature not more than 7400C is preferred for obtaining improved creep rupture strength and tensile strength. Further, the amount of carbon does not cause much influence regarding the enhancement of mechanical strength, however, the lower the amounts carbon and titanium in the alloys, the higher the elongation and reduction of area thereof become. Example 5 Table 9 shows the chemical composition of the rotor shaft 4 of the superhigh temperature and pressure steam turbine according to the invention. Raw materials for constituting the aforesaid composition were subjected to vacuum induction melting under a vacuum of 10 3 to produce electrodes of about 1000 mm in diameter. The electrodes were remelted by an electro-slag-remelting process (ESR) by use of flux consisting of CaF2 of 55%, A1203 of 35% and TiO2 of 10% and cast into columnar ingots. The ingots were diffusionannealed at a temperature of 11000-15000C and forged at a temperature below 10500C to produce a columnar blank of 850 mm in diameter and 6000 mm in length. The blank was held for 3 hours at a temperature of 10500C to control the grain size into a range of ASTM G.S. 2.5-4 while rotating the blank at a rate of 3 times per one minute. Table 9 EMI32.1 <SEP> C <SEP> Mn <SEP> Si <SEP> Cr <SEP> Ni <SEP> Mo <SEP> V <SEP> Ti <SEP> Al <SEP> B <SEP> S <SEP> P <SEP> Fe <tb> No. <SEP> 18 <SEP> 0.020 <SEP> 1.25 <SEP> 0.35 <SEP> 14.90 <SEP> 26.03 <SEP> 1.25 <SEP> 0.30 <SEP> 1.63 <SEP> 0.20 <SEP> 0.0043 <SEP> 0.001 <SEP> 0.003 <SEP> Bal. <tb> After subjecting the blank to solution treatment by holding same at a temperature in the range between 900 and 10000C for 1 hour, they were water-cooled by jetting water thereagainst while vertically holding and rotating it at a rate of three revolutions per-minute to room temperature. Thereafter, the blank was held at a temperature between 7000 and 7300C for 16 hours to effect aging while rotating it in the same manner, to provide a microstructure in which a y' phase is precipitated in austenite matrix. The blank was then machined to obtain a rotor shaft having predetermined dimensions shown in Fig. 13. Specimens for experiments were taken from the left hand end of the rotor shaft as shown in Fig. 13 and were subjected to the tests of tensile strength and creep rupture strength, with the result that there were obtained strength and elongation both substantially similar to those of the specimen No. 17 described above. Example 6 Table 10 shows the chemical composition (wt%) of a blade used in the superhigh temperature and pressure steam turbine of the present invention. Table 10 EMI34.1 <SEP> C <SEP> Si <SEP> Mn <SEP> Ni <SEP> Cr <SEP> Mo <SEP> V <SEP> Al <SEP> Ti <SEP> B <SEP> Fe <tb> No. <SEP> 19 <SEP> 0.031 <SEP> 0.65 <SEP> 1.25 <SEP> 25.81 <SEP> 16.00 <SEP> 1.21 <SEP> 0.30 <SEP> 0.15 <SEP> 2.25 <SEP> 0.0056 <SEP> Bal. <tb> Raw materials for constituting this chemical composition were subjected to vacuum induction melting to produce electrode (600 mm in diameter) for ESR. The electrodes were remelted by ESR process by use of flux consisting of CaFe of-50%, Cao of 25%, TiO2 of 15%and Al2O3 of 10%, and the molten metal was cast into blanks. Then, each of the blanks was heat-treated to control the grain size thereof. After that, there was effected the solution heat treatment of holding the blank at 8990C for 2 hours and of water-cooling thereafter. Then, the blank was subjected to aging treatment of two steps, i.e., in the first step the blank was held at 7600C for 16 hours with air-cooling being effected thereafter and in the second step the blank was held at 7180C for 6 hours with air-cooling thereafter, so that there was obtained a blank having microstructure in which y' phase is precipitated in austenite matrix. Such blank was subjected to mechanical working to obtain the blade having predetermined dimensions. Specimens were picked from the blade, which specimens were subjected to the test of evaluating tensile strength, creep rupture strength and high temperature lower circle fatigue resistant property, with the result that there were obtained values in a degree approximately similar to those of the specimen No. 1 shown in Table 2.

Claims: CLAIMS 1. A superhgh temperature and pressure steam turbine comprising a casing, blades in said casing receiving streams of steam jets for rotation, and a rotor shaft supporting said blades for rotation, said casing including an inner casing member having static blades secured thereto for guiding the streams of steam jets, and an outer casing member enclosing said inner casing member; said rotor shaft being made of an alloy consisting essentially, by weight, of less than 0.0% C, not more than 2% Mn, not more than 1.5% Si, 10-20% Cr, 20-30% Ni, 0.5-3% Mo, 0.5-3% Ti, 0.1-0.5% Al, 0.002-0.01% B and the balance Fe and inevitable impurities and having a microstructure in which a y' phase is precipitated in austenite matrix. 2. A superhigh temperature and pressure steam turbine comprising a casing, blades in said casing receiving streams of steam jets for rotation, and a rotor shaft supporting said blades for rotation; said casing including an inner casing member having static blades secured thereto for guiding the streams of steam jets, and an outer casing member enclosing said.inner casing member; said rotor shaft being made of an alloy consisting essentially, by weight, of less than 0.04% C, not more than 2% Mn, not more than 1.5% Si, 10-20% Cr, 20-30% Ni, 0.5-3% Mo, 0.5-3% Ti, 0.1-0.5% Al, 0.002-0.01% B and the balance Fe and inevitable impurities and having a microstructure in which a y' phase is precipitated in austenite matrix, and said blades being made of an alloy consisting essentially, by weight, of 0.01-0.1% C, not more than 1.5% Si, not more than 2% Mn, 10-20% Cr, 20-305 Ni, O.5-3% Mo, 1.5-3% Ti, 0.1-0.59 Al, 0.002-0.01% B and the balance Fe and inevitable umpurities and having a microstructure in which a y' phase is precipitated in austenite matrix, 3. A superhigh temperature and pressure steam turbine comprising a casing, blades in said casing receiving streams of steam jets for rotation, and a rotor shaft supporting said blades for rotation, said casing including an inner casing member having static blades secured thereto for guiding the streams of steam jets, and an outer casing member enclosing said inner casing member; said rotor shaft being made of an alloy consisting essentially, by weight, of less than 0.04% C, not more than 2% Mn, not more than 1.5% Si, 10-20% Cr, 20-30% Ni, 0.5-3% Mo, 0.5-3% Ti, 0.1-0.5% Al, 0.002-0.01% B and the balance Fe and inevitable impurities, and the Ni equivalent of said alloy is: Ni equivalent [Ni(%) + {(30 x C(%) + (0.5 x Mn(%))] = 23 - 29; and the Cr equivalent thereof is: Cr equivalent [Cr(%) + Mo(%) + (1.5 x Si(%)}] EMI38.1 <tb> = <SEP> 12 <SEP> - <SEP> [(7/10 <SEP> x <SEP> Ni <SEP> equivalent) <SEP> + <tb> and the alloy being austenitic forged steel having a microstructure with a y' phase precipitated in austenite matrix, 4. A superhigh temperature and pressure steam turbine as claimed in any one of claims 1-3, wherein said rotor shaft is formed of an alloy consisting essentially, by weight, of 0.015-0.03 % C, 0.5-1.5% Mn, 0.3-1% Si, 14-17% Cr, 24-28% Ni, 1-2% Mo, 1.5-2.5% Ti, 0.15-0.4 Al, 0.004-0.008% B, 0.05-0.5% V and the balance Fe and inevitable impurities. 5. A superhigh temperature and pressure steam turbine as claimed in claim 2, wherein said blades are formed of an alloy consisting essentially, by weight, of 0.04-0.07% C, 0.5-1.5% Mn, 0.3-1% Si, 14-17% Cr, 24-28% Ni, 1-2% Mo, 1.5-2.5% Ti, 0.15-0.4% Al, 0.0040.008% B, 0.05-0.5% V and the balance Fe and inevitable impurities. 6. A superhigh-temperature and pressure steam turbine as claimed in any one of claims 1-3, wherein said rotor shaft has 1000 hour creep rupture strength of 26-34 kgYmm2 at 6500C. 7. A superhigh temperature and pressure steam turbine as claimed in any one of claims 1-3, wherein said stream of steam jets have a temperature in a range between 6000 and 6500C and the steam pressure is in a range between 4000 and 5000 psi.

Inventors: IIJIMA, KATSUMI, KIRIHARA, SEISHIN, SUKEKAWA, MASAYUKI, YAMADA, NORIO
Applicants: HITACHI, LTD.
Application year: 1982
Main classification: C22C38
IPC codes: F01D5, C22C38