Method of production of high-nitrogen ferritic heat-resisting steel

BACKGROUND OF THE INVENTION
1. Field of the Invention
This invention relates to a high-nitrogen ferritic heat-resisting steel, more particularly to a high-nitrogen ferritic heat-resisting steel containing chromium, and which is appropriate for use in a high-temperature, high-pressure environment, and to a method of producing the same.
2. Description of the Prior Art
Recent years have seen a marked increase in the temperatures and pressures under which thermal power plant boilers are required to operate. Some plans already call for operation at 566.degree. C. and 310 ata and it is expected that operation under conditions of 650.degree. C. and 350 ata will be implemented in the future. These are extremely severe conditions from the viewpoint of the boiler materials used.
At operating temperatures exceeding 550.degree. C., it has, from the viewpoints of oxidation resistance and high-temperature strength, been necessary to switch from ferritic 2.1/4Cr--1 Mo steel to high-grade austenitic steels such as 18-8 stainless steel. In other words, it has been necessary to adopt expensive materials with properties exceeding what is required.
Decades have been spent in search of steels for filling in the gap between 2.1/4Cr--1 Mo steel and austenitic stainless steel. Medium Cr (e.g. 9 Cr and 12 Cr) steel boiler pipes are made of heat-resisting steels that were developed against this background. They achieve high-temperature strength and creep rupture strength on a par with austenitic steels by use of a base metal composition which includes various alloying elements for precipitation hardening and solution hardening.
The creep rupture strength of a heat-resisting steel is governed by solution hardening in the case of short-term aging and by precipitation hardening in the case of long-term aging. This is because the solution-hardening elements initially present in solid solution in the steel for the most part precipitate as stable carbides such as M.sub.23 C.sub.6 during aging, and then when the aging is prolonged these precipitates coagulate and enlarge, with a resulting decrease in creep rupture strength.
Thus, with the aim of maintaining the creep rupture strength of heat-resisting steels at a high level, a considerable amount of research has been done for discovering ways for avoiding the precipitation of the solution hardening elements and maintaining them in solid solution for as long as possible.
For example, Japanese Patent Public Disclosures No. 63(1988)-89644, 61(1986)-231139 and 62(1987)-297435 disclose ferritic steels that achieve dramatically higher creep rupture strength than conventional Mo-containing ferritic heat-resisting steels by the use of W as a solution hardening element.
While the solution hardening by W in these steels may be more effective than by Mo, the precipitates are still fundamentally carbides of the M.sub.23 C.sub.6 type, so that it is not possible to avoid reduction of the creep rupture strength following prolonged aging.
Moreover, the use of ferritic heat-resisting steels at up to 650.degree. C. has been considered difficult because of their inferior high-temperature oxidation resistance as compared with austenitic heat-resisting steels. A particular problem with these steels is the pronounced degradation of high-temperature oxidation resistance that results from the precipitation of Cr in the form of coarse M.sub.23 C.sub.6 type precipitates at the grain boundaries.
The highest temperature for use of ferritic heat-resisting steel has therefore been considered to be 600.degree. C.
The need for heat-resisting steels capable of standing up under extremely severe conditions has grown more acute not only because of the increasingly severe operating conditions mentioned earlier but also because of plans to reduce operating costs by extending the period of continuous power plant operation from the current 100 thousand hours up to around 150 thousand hours.
Although ferritic heat-resisting steels are somewhat inferior to austenitic steels in high-temperature strength and anticorrosion property, they have a cost advantage. Furthermore, for reasons related to the difference in thermal expansion coefficient, among the various steam oxidation resistance properties they are particularly superior in scale defoliation resistance. For these reasons, they are attracting attention as a boiler material.
For the reasons set out above, however, it is clearly not possible with the currently available technology to develop ferritic heat-resisting steels that are capable of standing up for 150 thousand hours under operating conditions of 650.degree. C., 350 ata, that are low in price and that exhibit good steam oxidation resistance.
Through their research the inventors developed a high-nitrogen ferritic heat-resisting steel in which W is added in place of Mo as the main solution hardening element, thereby increasing the high-temperature strength, and nitrogen is forcibly added to the ferritic steel to a level of supersaturation, thereby causing dispersed precipitation of fine nitrides and carbo-nitrides which greatly delay the formation of M.sub.23 C.sub.6 precipitates that would otherwise consume large quantities of Cr acting as an oxidation resistance enhancer, and W acting as a solution hardening agent. The inventors found that this steel exhibits stable creep rupture strength, superior high-temperature oxidation resistance and superior low-temperature toughness, and is capable of being applied under conditions of 650.degree. C., 350 ata and 150 thousand hours of continuous operation.
There have been few papers published on research into high-nitrogen ferritic heat-resisting steels and the only known published report in this field is Ergebnisse der Werkstoff-Forschung, Band I, Verlag Schweizerische Akademieder Werkstoffwissenschaften "Thubal-Kain", Zurich, 1987, 161-180.
However, the research described in this report is limited to that in connection with ordinary heat-resisting steel and there is no mention of materials which can be used under such severe conditions as 650.degree. C., 350 ata and 150 thousand hours continuous operation.
SUMMARY OF THE INVENTION
An object of this invention is to provide a high-nitrogen ferritic heat-resisting steel which overcomes the shortcomings of the conventional heat-resisting steels, and particularly to provide such a steel capable of being used under severe operating conditions wherein the decrease in creep rupture strength following prolonged aging and the degradation of high-temperature oxidation resistance caused by precipitation of carbides are mitigated by adding nitrogen to supersaturation so as to precipitate fine nitrides and/or carbo-nitrides which delay the formation of carbides such as the M.sub.23 C.sub.6 precipitates seen in conventional steels.
Another object of the invention is to provide such a high-nitrogen ferritic heat-resisting steel imparted with superior high-temperature oxidation resistance and creep rupture strength by allowing nitrogen added to beyond the solution limit to precipitate in the form of nitrides and carbo-nitrides.
Another object of the invention is to provide a method of producing a high-nitrogen ferritic heat-resisting steel of the aforesaid type.
This invention was accomplished in the light of the aforesaid knowledge and, in one aspect, pertains substantially to a high-nitrogen ferritic heat-resisting steel comprising, in weight percent, 0.01-0.30% C, 0.02-0.80% Si, 0.20-1.00% Mn, 8.00-13.00% Cr, 0.50-3.00% W, 0.005-1.00% Mo, 0.05-0.50% V, 0.02-0.12% Nb and 0.10-0.50% N and being controlled to include not more than 0.050% P, not more than 0.010% S and not more than 0.020% 0, and optionally comprising (A) one or both of 0.01-1.00% Ta and 0.01-1.00% Hf and/or (B) one or both of 0.0005-0.10% Zr and 0.01-0.10% Ti, the balance being Fe and unavoidable impurities.
Another aspect of the invention pertains to a method of producing such a high-nitrogen ferritic heat-resisting steel wherein the steel components are melted and equilibrated in an atmosphere of a mixed gas of a prescribed nitrogen partial pressure or nitrogen gas and the resulting melt is thereafter cast or solidified in an atmosphere controlled to have a nitrogen partial pressure of not less than 1.0 ata and a total pressure of not less than 4.0 ata, with the relationship between the partial pressure p and the total pressure P.sub.t being
10.sup.P <P.sub.t.sup.0.37 +log.sub.10 6
thereby obtaining sound ingots free of blowholes.
The above and other features of the present invention will become apparent from the following description made with reference to the drawings.

BRIEF DESCRIPTION OF THE DRAWINGS
FIG. 1 is a perspective view of an ingot and the manner in which it is to be cut.
FIG. 2 is a graph showing the relationship between the steel nitrogen content and the weight percentage of the total of M.sub.23 C.sub.6 +M.sub.6 C+Cr.sub.2 N+Cr.sub.2 (C,N) among the precipitates in the steel accounted for by M.sub.23 C.sub.6 +M.sub.6 C, and the relationship between the steel nitrogen content and the weight percentage of the total of M.sub.23 C.sub.6 +M.sub.6 C+Cr.sub.2 N+Cr.sub.2 (C,N) among the precipitates in the steel accounted for by Cr.sub.2 N+Cr.sub.2 (C,N).
FIG. 3 is a graph showing conditions under which blowholes occur in the ingot in terms of the relationship between the total pressure and nitrogen partial pressure of the atmosphere during casting.
FIG. 4 is a perspective view showing the manner in which creep test pieces are taken from a pipe specimen and a rolled plate specimen.
FIG. 5 is a graph showing the relationship between steel nitrogen content and extrapolated creep rupture strength at 650.degree. C., 150 thousand hours.
FIG. 6 is a graph showing an example of creep test results in terms of stress vs rupture time.
FIG. 7 is a graph showing the relationship between steel nitrogen content and Charpy impact absorption energy at 0.degree. C. following aging at 700.degree. C. for 10 thousand hours.
FIG. 8 is a graph showing the relationship between steel nitrogen content and the thickness of the oxidation scale formed on the surface of a test piece after oxidation at 650.degree. C. for 10 thousand hours.

DETAILED DESCRIPTION OF THE PREFERRED EMBODIMENT
The reasons for the limits placed on the components of the high-nitrogen ferritic heat-resisting steel in this invention will now be explained.
C is required for achieving strength. Adequate strength cannot be achieved at a C content of less than 0.01%, while at a C content exceeding 0.30% the steel is strongly affected by welding heat and undergoes hardening which becomes a cause for low-temperature cracking. The C content range is therefore set at 0.01-0.30%.
Si is important for achieving oxidation resistance and is also required as a deoxidizing agent. It is insufficient for these purposes at a content of less than 0.02%, whereas a content exceeding 0.80% reduces the creep rupture strength. The Si content range is therefore set at 0.02-0.80%.
Mn is required for deoxidation and also for achieving strength. It has to be added at at least 0.20% for adequately exhibiting its effect. When it exceeds 1.00% it may in some cases reduce creep rupture strength. The Mn content range is therefore set at 0.20-1.00%.
Cr is indispensable to oxidation resistance. It also contributes to increasing creep resistance by combining with N and finely precipitating in the base metal matrix in the form of Cr.sub.2 N, Cr.sub.2 (C,N) and the like. Its lower limit is set at 8.0% from the viewpoint of oxidation resistance. Its upper limit is set at 13.0% for maintaining the Cr equivalent value at a low level so as to realize a martensite phase texture.
W produces a marked increase in creep rupture strength by solution hardening. Its effect toward increasing creep rupture strength over long periods at high temperatures of 550.degree. C. and higher is particularly pronounced. Its upper limit is set at 3.00% because at contents higher than this level it precipitates in large quantities in the form of carbide and intermetallic compounds which sharply reduce the toughness of the base metal. The lower limit is set at 0.50% because it does not exhibit adequate solution hardening effect at lower levels.
Mo increases high-temperature strength through solution hardening. It does not exhibit adequate effect at a content of less than 0.005% and at a content higher than 1.00% it may, when added together with W, cause heavy precipitation of Mo.sub.2 C type oxides which markedly reduce base metal toughness. The Mo content range is therefore set at 0.005-1.00%.
V produces a marked increase in the high-temperature strength of the steel regardless of whether it forms precipitates or, like W, enters solid solution in the matrix. When it precipitates, the resulting VN serves as precipitation nuclei for Cr.sub.2 N and Cr.sub.2 (C,N), which has a pronounced effect toward promoting fine dispersion of the precipitates. It has no effect at below 0.05% and reduces toughness at higher than 0.50%. The V content range is therefore set at 0.05-0.50%.
Nb increases high-temperature strength by precipitating as NbN and Nb(C,N). Also, similarly to V, it promotes fine precipitate dispersion by forming precipitation nuclei for Cr.sub.2, Cr.sub.2 (C,N) and the like. The lower limit at which it manifests these effects is 0.02%. Its upper limit is set at 0.12% because when present at higher levels it reduces strength by causing precipitate coagulation and enlargement.
N dissolves in the matrix and also forms nitride and carbo-nitride precipitates. As the form of the precipitates is mainly Cr.sub.2 N and Cr.sub.2 (C,N), there is less precipitate-induced consumption of Cr and W than in the case of the M.sub.23 C.sub.6, M.sub.6 C and other such precipitates observed in conventional steels. N thus increases oxidation resistance and creep rupture strength. At least 0.10% is required for precipitation of nitrides and carbo-nitrides and suppressing precipitation of M.sub.23 C.sub.6, M.sub.6 C. The upper limit is set at 0.50% for preventing coagulation and enlargement of nitride and carbo-nitride precipitates by the presence of excessive nitrogen.
P, S and O are present in the steel according to this invention as impurities. P and S hinder the achievement of the purpose of the invention by lowering strength, while 0 has the adverse effect of forming oxides which reduce toughness. The upper limits on these elements is therefore set at 0.050%, 0.010% and 0.020%, respectively.
The basic components of the steel according to this invention (aside from Fe) are as set out above. Depending on the purpose to which the steel is to be put, however, it may additionally contain (A) one or both of 0.01-1.00% Ta and 0.01-1.00% Hf and/or (B) one or both of 0.0005-0.10% Zr and 0.01-0.10% Ti.
At low concentrations Ta and Hf act as deoxidizing agents. At high concentrations they form fine high melting point nitrides and carbo-nitrides and, as such, increase toughness by decreasing the austenite grain size. In addition, they also reduce the degree to which Cr and W dissolve in precipitates and by this effect enhance the effect of supersaturation with nitrogen. Neither element exhibits any effect at less than 0.01%. When either is present at greater than 1.00%, it reduces toughness by causing enlargement of nitride and carbo-nitride precipitates. The content range of each of these elements is therefore set at 0.01-1.00%.
Acting to govern the deoxidation equilibrium in the steel, Zr suppresses the formation of oxides by markedly reducing the amount of oxygen activity. In addition, its strong affinity for N promotes precipitation of fine nitrides and carbo-nitrides which increase creep rupture strength and high-temperature oxidation resistance. When present at less than 0.0005% it does not provide an adequate effect of governing the deoxidation equilibrium, and when present at greater than 0.10% it results in heavy precipitation of coarse ZrN and ZrC which markedly reduce the toughness of the base metal. The Zr content range is therefore set at 0.0005-0.10%.
Ti raises the effect of excess nitrogen by precipitating in the form of nitrides and carbo-nitrides. At a content of less than 0.01% it has no effect, while at a content of over 0.10% it results in precipitation of coarse nitrides and carbo-nitrides which reduce toughness. The Ti content range is therefore set at 0.01-0.10%.
The aforesaid alloying components can be added individually or in combinations.
The object of this invention is to provide a ferritic heat-resisting steel that is superior in creep rupture strength and high-temperature oxidation resistance. Depending on the purpose of use it can be produced by various methods and be subjected to various types of heat treatment. These methods and treatments in no way diminish the effect of the invention.
However, in view of the need to supersaturate the steel with nitrogen, it is necessary during casting to raise the pressure of the atmosphere to not less than 4.0 ata and to control the nitrogen partial pressure to not less than 1.0 ata. As an auxiliary gas to be mixed with the nitrogen gas it is appropriate to use an inert gas such as Ar, Ne, Xe or Kr. These casting conditions were determined by the following experiment.
Steel of a chemical composition aside from nitrogen as indicated in claims 1-4 was melted in an induction heating furnace installed in a chamber that could be pressurized up to 150 ata. A mixed gas of argon and nitrogen having a prescribed nitrogen partial pressure was introduced into the furnace and maintained at a pressure which was varied from test to test. After the nitrogen and molten metal had reached chemical equilibrium, the molten metal was cast into a mold that had been installed in the chamber beforehand, whereby there was obtained a 5-ton ingot.
The ingot was cut vertically as shown in FIG. 1 and the ingot 1 was visually examined for the presence of blowholes.
Following this examination, a part of the ingot was placed in a furnace and maintained at 1180.degree. C. for 1 hour and then forged into a plate measuring 50 mm in thickness, 750 mm in width and 4,000 mm in length.
This plate was subjected to solution treatment at 1100.degree. C. for 1 hour and to tempering at 760.degree. C. for 3 hours. The steel was then chemically analyzed and the dispersion state and morphology of the nitrides and carbo-nitrides were investigated by observation with an optical microscope, an electron microscope, X-ray diffraction and electron beam diffraction, whereby the chemical structure was determined.
Among the precipitates present within the as-heat-treated steel, FIG. 2 shows how the proportion of the precipitates in the steel accounted for by M.sub.23 C.sub.6 type carbides and M.sub.6 C type carbides, and the proportion thereof accounted for by Cr.sub.2 N type nitrides and carbo-nitrides, vary with nitrogen concentration. At a nitrogen concentration of 0.1%, nitrides and carbo-nitrides account for the majority of the precipitates in the steel, while at a nitrogen concentration of 0.15%, substantially 100% of the precipitates are nitrides and carbo-nitrides with virtually no carbides present whatsoever. Thus, for the effect of this invention to be adequately manifested it is necessary for the nitrogen concentration of the steel to be not less than 0.1%.
The graph of FIG. 3 shows how the state of blowhole occurrence varies depending on the relationship between the total and nitrogen partial pressure of the atmosphere. For achieving a nitrogen concentration of 0.1% or higher it is necessary to use a total pressure of not less than 4.0 ata. Equilibrium calculation based on Sievert's law shows that the nitrogen partial pressure in this case is not less than 1.0 ata.
Moreover, where for controlling the amount of nitride and carbo-nitride precipitation the nitrogen partial pressure p is maintained at 1.0-6.0 ata (nitrogen concentration within the steel of approximately 0.5 wt.%), it becomes necessary to vary the total pressure P.sub.t between 4.0 and about 100 ata, the actual value selected depending on the nitrogen partial pressure. Namely, it is necessary to use a total pressure falling above the broken line representing the boundary pressure in FIG. 3.
When the boundary line of FIG. 3 is determined experimentally it is found to lie at
10.sup.P =P.sub.t.sup.0.37 +log.sub.10 6
meaning that the steel according to this invention can be obtained by selecting an atmosphere of a pressure and composition meeting the condition of the inequality
10.sup.P <P.sub.t.sup.0.37 +log.sub.10 6.
It is therefore necessary to use furnace equipment enabling pressure and atmosphere control. Without such equipment, it is difficult to produce the steel of the present invention.
There are no limitations whatever on the melting method. Based on the chemical composition of the steel and cost considerations, it suffices to select from among processes using a converter, an induction heating furnace, an arc melting furnace or an electric furnace.
The situation regarding refining is similar. Insofar as the atmosphere is controlled to a total pressure of not less than 4.0 ata and a nitrogen partial pressure of not less than 1.0 ata, it is both possible and effective to use a ladle furnace, an electro-slag remelting furnace or a zone melting furnace.
After casting under a pressurized atmosphere of a total pressure of not less than 4.0 ata and a nitrogen partial pressure of not less than 1.0 ata, it is possible to process the steel into a billet, bloom or plate by casting or hot rolling. Since the steel of this invention includes finely dispersed nitrides and carbo-nitrides, it is superior to conventional ferritic heat-resisting steels in hot-workability. This is also one reason for employing nitrides and carbo-nitrides obtained by adding nitrogen to beyond the solution limit.
For processing the steel into products, it is possible to first process it into a round or rectangular billet and then form it into a seamless pipe or tube by hot extrusion or any of various seamless rolling methods. Otherwise it can be formed into a sheet by hot and cold rolling and then made into a welded tube by electric resistance welding. Alternatively, it can be processed into a welded pipe or tube by use of TIG, MIG, SAW, LASER and EB welding, individually or in combination. Moreover, it is possible to expand the size range of products to which the present invention can be applied by following any of the aforesaid processes by hot or warm stretch reduction or sizing.
The steel according to the invention can also be provided in the form of a plate or sheet. The plate or sheet can, in its hot-rolled state or after whatever heat treatment is found necessary, be provided as a heat-resisting material in various shapes, without any influence on the effects provided by the invention.
The pipe, tube, plate, sheet and variously shaped heat-resisting materials referred to above can, in accordance with their purpose and application, be subjected to various heat treatments, and it is important for them to be so treated for realizing the full effect of the invention.
While the production process ordinarily involves normalizing (solution heat treatment)+tempering, it is also possible and useful additionally to carry out one or a combination of two or more of quenching, tempering and normalizing. It is also possible, without influencing the effects of the present invention in any way, to repeatedly carry out one or more of the aforesaid processes to whatever degree is necessary for adequately bringing out the steel properties.
The aforesaid processes can be appropriately selected and applied to the manufacture of the steel according to the invention.
WORKING EXAMPLES
The steels indicated in Tables 1-4, each having a composition according to one of claims 1-4, were separately melted in amounts of 5 tons each in an induction heating furnace provided with pressurizing equipment. The resulting melt was cleaned by ladle furnace processing (under bubbling with a gas of the same composition as the atmosphere) for reducing its impurity content, whereafter the atmosphere was regulated using a mixed gas of nitrogen and argon so as to satisfy the conditions of the inequality shown above. The melt was then cast into a mold and processed into a round billet, part of which was hot extruded to obtain a tube 60 mm in diameter and 10 mm in wall thickness and the remainder of which was subjected to seamless rolling to obtain a pipe 380 mm in diameter and 50 mm in wall thickness. The tube and pipe were subjected to a single normalization at 1100.degree. C. for 1 hour and were then tempered at 760.degree. C. for 3 hours.
In addition, a 50 ton ingot was cast and forged into a slab which was hot rolled into 25 mm and 50 mm thick plates.
As shown in FIG. 4, creep test pieces 6 measuring 6 mm in diameter were taken along the axial direction 4 of the pipe or tube 3 and along the rolling direction 5 of the plates and subjected to creep test measurement at 650.degree. C. Based on the data obtained, a linear extrapolation was made for estimating the creep rupture strength at 150 thousand hours. A creep rupture strength of 15.0 kg/mm.sup.2 was used as the creep rupture strength evaluation reference value. The creep rupture strength at 650.degree. C., 150 thousand hours is hereinafter defined as the linearly extrapolated value at 150 thousand hours on the creep rupture strength vs rupture time graph.
Toughness was evaluated through an accelerated evaluation test in which aging was carried out at 700.degree. C. for 10 thousand hours. JIS No. 4 tension test pieces were cut from the aged steel and evaluated for impact absorption energy. Assuming a water pressure test at 0.degree. C., the toughness evaluation reference value was set at 5.0 kgf.m.
High-temperature oxidation resistance was evaluated by suspending a 25 mm.times.25 mm.times.5 mm test piece cut from the steel in 650.degree. C. atmospheric air in a furnace for 10 thousand hours and then cutting the test piece parallel to the direction of growth of the scale and measuring the oxidation scale thickness.
The 650.degree. C., 150 thousand hour creep rupture strength, the Charpy impact absorption energy at 0.degree. C. after aging at 700.degree. C. for 10 thousand hours and the oxidation scale thickness after oxidation at 650.degree. C. for 10 thousand hours are shown in Tables 1 to 4, respectively.
For comparison, steels of compositions not falling within any of the claims to 4 were melted, processed and tested in the same way as described above. Their chemical compositions and the evaluation results are shown in Table 5.
FIG. 5 shows the relationship between the nitrogen content of the steels and the extrapolated creep rupture strength at 650.degree. C., 150 thousand hours. It will be noted that the creep rupture strength attains high values exceeding 15 kg/mm.sup.2 at a steel nitrogen content of 0.1% or higher but falls below 15 kg/mm.sup.2 and fails to satisfy the evaluation reference value that was set at a steel nitrogen content of less than 0.1%.
FIG. 6 shows the results of the creep test in terms of stress vs rupture time. A good linear relationship can be noted between stress and rupture time at a steel nitrogen content of not less than 0.1%. On the other hand, when the steel nitrogen content falls below 0.1%, the relationship between stress and rupture time exhibits a pronounced decline in creep rupture strength with increasing time lapse. That is to say, linearity is not maintained. This is because W and the other solution hardening elements precipitate as carbides whose coagulation and enlargement degrades the creep rupture strength property of the base metal. In contrast, at a nitrogen content of 0.1% or higher, fine nitrides and carbo-nitrides are preferentially precipitated so that the formation of carbides is greatly delayed, and since this suppresses the dissolution of the solution hardening elements into carbides, a high creep rupture strength was maintained in the long-term creep test.
FIG. 7 shows the relationship between Charpy impact absorption energy at 0.degree. C. following aging at 700.degree. C. for 10 thousand hours and steel nitrogen content. When the steel nitrogen content falls within the range of 0.1-0.5%, the impact absorption energy exceeds 3.0 kgf.m. In contrast, when it falls below 0.1%, there is little or no suppression of grain growth by residual high melting point nitrides during solution treatment and, as a result, the impact absorption energy decreases, and when it exceeds 0.5%, the impact absorption energy is reduced by heavy nitride precipitation.
FIG. 8 shows the relationship between the thickness of the oxidation scale formed on the surface of a test piece after oxidation at 650.degree. C. for 10 thousand hours and the steel nitrogen content. Although the oxidation scale thickness is between 400 and 800 .mu.m when the steel nitrogen content falls below 0.1%, it decreases to 250 .mu.m or less when the steel nitrogen content is 0.1% or higher.
Reference is now made to the comparison steels shown in Table 5. Nos. 161 and 162 are examples in which insufficient steel nitrogen content resulted in a low extrapolated creep rupture strength at 650.degree. C., 150 thousand hours, and also poor high-temperature oxidation resistance. Nos. 163 and 164 are examples in which excessive steel nitrogen content caused heavy precipitation of coarse nitrides and carbo-nitrides, resulting in a Charpy impact absorption energy at 0.degree. C. after aging at 700.degree. C. for 10 thousand hours of not more than 3.0 kgf.m. No. 165 is an example in which a low W concentration resulted in a low creep rupture strength owing to insufficient solution hardening, notwithstanding that the steel nitrogen content fell within the range of the invention. No. 166 is an example in which heavy precipitation of coarse ZrN caused by a Zr concentration in excess of 0.1% resulted in a Charpy impact absorption energy at 0.degree. C. after aging at 700.degree. C. for 10 thousand hours of less than 3.0 kgf.m. Nos. 167, 168 and 169 are examples similar to the case of No. 166 except that the elements present in excess were Ta, Hf and Ti, respectively. As a result, heavy precipitation of coarse TaN, HfN and TiN resulted in a Charpy impact absorption energy at 0.degree. C. after aging at 700.degree. C. for 10 thousand hours of less than 3.0 kgf.m. No. 170 is an example in which the nitrogen partial pressure was 2.2 ata and the total pressure was 2.5 ata, values not satisfying the inequality set forth above, so that many large blowholes formed in the ingot, making it impossible to obtain either a sound ingot or a plate, and leading to a reduction in both the extrapolated creep rupture strength at 650.degree. C., 150 thousand hours and the Charpy impact absorption energy at 0.degree. C. after aging at 700.degree. C. for 10 thousand hours.
TABLE 1__________________________________________________________________________(Wt. %) Invention Steels CS kg/ VE TONo. C Si Mn P S Nb V Cr Mo W Zr Ta Hf Ti N O mm.sup.2 kgf .multidot. .mu.m__________________________________________________________________________ 1 0.018 0.682 0.885 0.034 0.009 0.058 0.215 11.98 0.922 0.850 -- -- -- -- 0.255 0.019 19.9 4.67 176 2 0.131 0.796 0.532 0.029 0.002 0.074 0.490 8.77 0.961 1.024 -- -- -- -- 0.104 0.010 16.0 13.9 117 3 0.255 0.685 0.935 0.014 0.009 0.046 0.382 11.45 0.421 2.157 -- -- -- -- 0.143 0.004 17.3 12.8 206 4 0.011 0.499 0.249 0.019 0.009 0.094 0.432 11.00 0.985 2.256 -- -- -- -- 0.250 0.007 21.0 4.24 1755 0.035 0.387 0.626 0.029 0.007 5 0.269 8.36 0.350 1.752 -- -- -- -- 0.301 0.003 23.5 4.40 198 6 0.088 0.491 0.213 0.013 0.002 0.037 0.202 9.46 0.193 1.124 -- -- -- -- 0.170 0.014 17.0 16.0 230 7 0.226 0.566 0.756 0.038 0.008 0.072 0.091 12.71 0.698 0.829 -- -- -- -- 0.329 0.016 23.4 7.19 226 8 0.074 0.763 0.813 0.012 0.009 0.105 0.470 9.07 0.563 2.597 -- -- -- -- 0.259 0.012 24.2 14.8 135 9 0.110 0.056 0.530 0.022 0.002 0.057 0.302 12.02 0.479 0.656 -- -- -- -- 0.430 0.015 21.7 6.95 21210 0.250 0.151 0.857 0.016 0.003 0.096 0.116 12.42 0.617 2.967 -- -- -- -- 0.117 0.009 22.6 14.2 11311 0.260 0.418 0.748 0.021 0.004 0.041 0.452 11.29 0.686 2.505 0.0429 -- -- -- 0.400 0.018 23.7 4.09 23612 0.046 0.599 0.739 0.024 0.006 0.061 0.263 11.94 0.846 0.961 0.0253 -- -- -- 0.146 0.015 17.1 14.2 16313 0.098 0.465 0.593 0.033 0.008 0.025 0.312 12.92 0.306 2.574 0.0249 -- -- -- 0.435 0.007 24.5 5.48 22114 0.183 0.560 0.469 0.017 0.001 0.101 0.238 12.70 0.257 1.592 0.0595 -- -- -- 0.149 0.012 17.7 8.16 13815 0.062 0.615 0.891 0.021 0.006 0.057 0.340 12.06 0.365 2.174 0.0488 -- -- -- 0.349 0.018 23.8 11.0 16616 0.224 0.791 0.425 0.034 0.006 0.113 0.483 12.05 0.827 2.318 0.0113 -- -- -- 0.118 0.018 24.5 16.6 18417 0.146 0.458 0.829 0.023 0.002 0.038 0.080 8.63 0.346 1.264 0.0155 -- -- -- 0.129 0.016 16.7 13.6 22118 0.171 0.531 0.633 0.035 0.006 0.050 0.331 12.67 0.584 1.931 0.0299 -- -- -- 0.256 0.015 22.3 4.85 23019 0.065 0.385 0.401 0.019 0.001 0.117 0.431 12.63 0.749 2.345 0.0735 -- -- -- 0.178 0.009 18.2 13.5 16220 0.169 0.161 0.275 0.041 0.007 0.110 0.233 9.43 0.515 1.688 0.0166 -- -- -- 0.365 0.011 21.3 7.73 12221 0.250 0.394 0.807 0.010 0.002 0.096 0.269 11.51 0.570 1.668 -- 0.014 -- -- 0.293 0.015 18.4 3.71 21322 0.072 0.070 0.554 0.032 0.008 0.094 0.405 12.37 0.116 1.542 -- 0.346 -- -- 0.442 0.016 21.4 11.3 16423 0.126 0.110 0.459 0.035 0.002 0.021 0.270 10.37 0.319 1.731 -- 0.645 -- -- 0.484 0.017 22.0 11.8 22424 0.023 0.257 0.268 0.047 0.010 0.100 0.175 11.45 0.878 1.502 -- 0.443 -- -- 0.488 0.011 22.5 15.3 20125 0.118 0.292 0.545 0.035 0.009 0.097 0.432 11.62 0.986 1.305 -- 0.146 -- -- 0.138 0.004 19.4 3.31 19626 0.028 0.343 0.627 0.046 0.002 0.081 0.224 9.26 0.330 2.857 -- 0.356 -- -- 0.104 0.016 19.8 13.3 16427 0.240 0.568 0.675 0.029 0.001 0.072 0.085 10.36 0.591 1.629 -- 0.074 -- -- 0.468 0.005 15.5 13.0 13028 0.229 0.721 0.837 0.030 0.010 0.086 0.327 8.33 0.465 1.848 -- 0.372 -- -- 0.297 0.011 18.3 12.0 12429 0.050 0.546 0.848 0.038 0.004 0.095 0.354 11.53 0.619 2.724 -- 0.034 -- -- 0.465 0.011 15.2 5.99 25030 0.047 0.599 0.883 0.019 0.008 0.116 0.256 8.56 0.269 2.234 -- 0.247 -- -- 0.458 0.007 17.9 4.49 23431 0.274 0.224 0.265 0.021 0.001 0.067 0.335 10.15 0.076 0.809 0.0179 0.129 -- -- 0.138 0.011 18.5 3.06 17932 0.059 0.358 0.757 0.032 0.003 0.067 0.452 12.38 0.237 2.678 0.0490 0.376 -- -- 0.384 0.010 18.6 11.3 11433 0.181 0.371 0.509 0.019 0.001 0.086 0.250 8.67 0.445 0.876 0.0223 0.251 -- -- 0.273 0.016 20.1 11.1 21734 0.262 0.399 0.868 0.029 0.002 0.043 0.253 9.91 0.378 0.786 0.0571 0.459 -- -- 0.477 0.005 20.3 12.1 14335 0.214 0.216 0.397 0.011 0.003 0.106 0.102 12.12 0.740 1.685 0.0217 0.012 -- -- 0.479 0.007 20.8 16.7 14436 0.088 0.739 0.842 0.031 0.007 0.044 0.111 8.72 0.216 1.550 0.0349 0.220 -- -- 0.350 0.018 23.5 6.79 24837 0.086 0.551 0.737 0.018 0.004 0.025 0.126 8.08 0.972 2.042 0.0139 0.135 -- -- 0.162 0.003 15.0 12.5 10738 0.256 0.183 0.243 0.038 0.002 0.068 0.466 8.69 0.221 2.419 0.0778 0.042 -- -- 0.389 0.003 17.5 15.8 19839 0.219 0.572 0.708 0.019 0.002 0.042 0.085 8.95 0.629 1.881 0.0474 0.893 -- -- 0.109 0.012 17.8 12.4 17940 0.179 0.303 0.684 0.049 0.003 0.115 0.420 9.82 0.894 2.155 0.0889 0.370 -- -- 0.199 0.006 22.7 4.69 22241 0.187 0.297 0.323 0.035 0.009 0.058 0.205 9.76 0.207 1.210 -- -- 0.065 -- 0.329 0.006 19.2 9.50 13642 0.010 0.703 0.969 0.025 0.009 0.088 0.427 12.17 0.252 0.775 -- -- 0.215 -- 0.377 0.009 19.2 8.48 24743 0.138 0.506 0.381 0.046 0.004 0.074 0.269 10.54 0.220 1.320 -- -- 0.456 -- 0.422 0.006 19.4 4.07 20744 0.041 0.617 0.703 0.026 0.006 0.034 0.265 8.26 0.792 2.052 -- -- 0.971 -- 0.332 0.002 21.8 12.9 12045 0.068 0.413 0.885 0.012 0.007 0.087 0.270 8.76 0.159 2.161 -- -- 0.946 -- 0.187 0.019 18.1 16.5 23646 0.120 0.416 0.665 0.010 0.004 0.052 0.143 10.44 0.989 0.894 -- -- 0.574 -- 0.254 0.014 15.2 3.72 13647 0.257 0.393 0.211 0.010 0.008 0.098 0.430 9.35 0.506 1.243 -- -- 0.547 -- 0.211 0.018 15.3 5.21 22548 0.247 0.102 0.467 0.039 0.002 0.095 0.304 11.36 0.871 1.153 -- -- 0.555 -- 0.140 0.007 20.1 16.5 15549 0.287 0.086 0.393 0.045 0.002 0.061 0.306 12.46 0.296 1.104 -- -- 0.781 -- 0.115 0.012 16.4 5.38 17850 0.287 0.092 0.929 0.014 0.005 0.064 0.297 11.05 0.946 2.816 -- -- 0.908 -- 0.208 0.009 21.1 9.21 247__________________________________________________________________________ CS: Creep rupture strength at 650.degree. C., 150 thousand hours VE: Charpy absorption energy at 0.degree. C. after aging at 700.degree. C for 10 thousand hours TO: Oxidation scale thickness after oxidation at 650.degree. C. for 10 thousand hours in air
TABLE 2__________________________________________________________________________(Wt. %) Invention Steels CS kg/ VE TONo. C Si Mn P S Nb V Cr Mo W Zr Ta Hf Ti N O mm.sup.2 kgf .multidot. .mu.m__________________________________________________________________________51 0.297 0.257 0.215 0.014 0.004 0.022 0.350 8.01 0.509 1.727 0.0460 -- 0.130 -- 0.289 0.010 21.0 9.55 16552 0.083 0.346 0.812 0.032 0.009 0.054 0.331 11.82 0.178 2.066 0.0283 -- 0.610 -- 0.437 0.011 23.0 16.2 18553 0.280 0.120 0.471 0.016 0.003 0.080 0.102 10.95 0.143 1.821 0.0278 -- 0.572 -- 0.330 0.004 19.2 10.9 18854 0.076 0.503 0.944 0.015 0.008 0.070 0.196 11.34 0.591 1.461 0.0137 -- 0.690 -- 0.441 0.012 21.3 3.30 20055 0.246 0.076 0.774 0.014 0.006 0.089 0.245 8.88 0.705 1.435 0.0033 -- 0.643 -- 0.444 0.011 21.1 9.65 24756 0.264 0.550 0.513 0.022 0.003 0.107 0.333 9.51 0.672 2.212 0.0652 -- 0.619 -- 0.214 0.005 20.6 4.85 20957 0.043 0.115 0.310 0.046 0.002 0.095 0.323 11.70 0.190 0.520 0.0693 -- 0.809 -- 0.225 0.014 21.6 5.42 11558 0.213 0.087 0.311 0.014 0.004 0.068 0.066 8.80 0.420 1.799 0.0335 -- 0.892 -- 0.351 0.006 15.9 6.88 21559 0.248 0.224 0.668 0.012 0.001 0.097 0.100 9.33 0.067 2.789 0.0265 -- 0.074 -- 0.268 0.002 15.4 5.07 16660 0.206 0.297 0.748 0.049 0.004 0.103 0.074 11.79 0.839 2.783 0.0192 -- 0.542 -- 0.456 0.006 22.3 9.67 14561 0.141 0.436 0.682 0.013 0.007 0.101 0.280 12.03 0.402 2.144 -- 0.209 0.468 -- 0.186 0.004 23.2 9.25 10662 0.112 0.410 0.635 0.010 0.006 0.062 0.365 8.54 0.950 2.671 -- 0.712 0.067 -- 0.339 0.007 15.0 13.3 15063 0.165 0.744 0.345 0.029 0.002 0.054 0.178 9.71 0.667 1.021 -- 0.123 0.986 -- 0.180 0.010 24.5 10.6 23264 0.214 0.031 0.765 0.036 0.003 0.046 0.480 8.99 0.739 2.675 -- 0.243 0.934 -- 0.392 0.017 18.7 10.6 22865 0.164 0.349 0.836 0.039 0.004 0.054 0.454 12.25 0.842 1.840 -- 0.067 0.102 -- 0.440 0.011 19.4 9.12 16666 0.218 0.308 0.724 0.045 0.005 0.102 0.416 8.02 0.682 2.775 -- 0.146 0.176 -- 0.207 0.017 23.6 15.7 22867 0.286 0.441 0.577 0.043 0.001 0.055 0.452 12.29 0.954 2.209 -- 0.053 0.348 -- 0.372 0.008 23.1 11.9 13968 0.276 0.099 0.928 0.020 0.008 0.031 0.407 8.32 0.816 1.771 -- 0.471 0.768 -- 0.401 0.008 19.5 14.3 15069 0.239 0.215 0.342 0.022 0.009 0.102 0.376 9.67 0.969 0.759 -- 0.139 0.179 -- 0.167 0.009 20.1 4.70 14470 0.089 0.165 0.970 0.038 0.001 0.036 0.446 9.77 0.121 0.892 -- 0.214 0.241 -- 0.156 0.016 16.7 13.7 22271 0.027 0.081 0.551 0.015 0.006 0.097 0.240 11.99 0.917 2.561 0.0707 0.013 0.114 -- 0.436 0.014 20.7 15.5 10872 0.095 0.495 0.430 0.020 0.005 0.111 0.299 9.77 0.568 2.552 0.0031 0.166 0.035 -- 0.274 0.015 19.7 13.5 13873 0.077 0.022 0.788 0.042 0.005 0.093 0.265 9.21 0.779 1.373 0.0272 0.010 0.181 -- 0.365 0.014 20.1 9.92 11274 0.016 0.748 0.562 0.048 0.004 0.113 0.444 8.66 0.731 0.704 0.0626 0.054 0.231 -- 0.179 0.014 19.1 14.4 13275 0.260 0.082 0.296 0.045 0.008 0.090 0.243 11.54 0.104 2.254 0.0780 0.388 0.378 -- 0.182 0.019 18.4 8.75 22876 0.137 0.511 0.940 0.041 0.004 0.041 0.194 8.78 0.081 1.492 0.0907 0.307 0.797 -- 0.456 0.005 24.8 9.23 20177 0.278 0.620 0.241 0.023 0.009 0.034 0.155 8.79 0.844 2.616 0.0697 0.045 0.180 -- 0.470 0.010 15.1 4.46 15378 0.156 0.541 0.342 0.017 0.005 0.089 0.434 9.98 0.084 2.337 0.0340 0.083 0.701 -- 0.295 0.003 16.3 4.30 18879 0.120 0.051 0.607 0.014 0.008 0.025 0.445 8.37 0.984 2.421 0.0034 0.022 0.574 -- 0.213 0.014 15.4 4.31 18780 0.226 0.467 0.788 0.019 0.006 0.112 0.056 9.90 0.265 0.856 0.0954 0.038 0.482 -- 0.104 0.002 24.1 14.2 10181 0.235 0.360 0.620 0.040 0.009 0.115 0.229 10.42 0.565 0.505 -- -- -- 0.082 0.433 0.014 19.2 15.4 10682 0.056 0.280 0.265 0.024 0.002 0.057 0.171 10.94 0.111 1.953 -- -- -- 0.017 0.482 0.018 17.9 3.78 23683 0.037 0.372 0.280 0.040 0.009 0.057 0.408 9.95 0.580 0.629 -- -- -- 0.028 0.125 0.009 16.9 16.9 13984 0.086 0.379 0.392 0.015 0.009 0.027 0.338 8.22 0.140 1.935 -- -- -- 0.036 0.233 0.007 17.8 7.96 14385 0.105 0.067 0.764 0.014 0.002 0.044 0.063 11.82 0.497 1.436 -- -- -- 0.065 0.280 0.008 18.0 8.27 20586 0.017 0.375 0.758 0.049 0.001 0.022 0.113 11.72 0.350 2.072 -- -- -- 0.083 0.152 0.014 19.0 13.0 20087 0.157 0.256 0.504 0.024 0.008 0.032 0.338 11.23 0.360 0.532 -- -- -- 0.019 0.113 0.002 17.8 4.10 23388 0.148 0.263 0.962 0.028 0.004 0.041 0.157 11.37 0.724 1.066 -- -- -- 0.067 0.243 0.012 21.4 11.9 10789 0.043 0.142 0.681 0.049 0.002 0.118 0.103 10.56 0.641 2.890 -- -- -- 0.022 0.215 0.019 16.4 11.0 14790 0.184 0.044 0.213 0.012 0.003 0.033 0.482 9.75 0.789 2.704 -- -- -- 0.033 0.106 0.010 19.7 11.3 23591 0.194 0.501 0.498 0.047 0.004 0.103 0.480 12.32 0.351 2.238 0.0009 -- -- 0.074 0.185 0.013 23.4 8.33 17292 0.271 0.501 0.500 0.021 0.002 0.099 0.408 11.80 0.027 1.969 0.0340 -- -- 0.072 0.339 0.016 24.4 4.68 13893 0.182 0.572 0.368 0.021 0.004 0.038 0.350 9.11 0.998 2.356 0.0831 -- -- 0.087 0.233 0.011 24.2 16.7 23294 0.264 0.455 0.225 0.034 0.005 0.088 0.156 12.52 0.430 2.589 0.0177 -- -- 0.091 0.339 0.013 20.0 5.44 18695 0.287 0.324 0.660 0.048 0.001 0.020 0.375 8.21 0.054 1.936 0.0569 -- -- 0.058 0.142 0.005 23.5 8.32 10396 0.162 0.308 0.599 0.031 0.006 0.101 0.183 9.48 0.518 2.105 0.0196 -- -- 0.093 0.111 0.010 16.7 13.9 23397 0.083 0.547 0.585 0.030 0.002 0.050 0.108 9.70 0.019 0.996 0.0772 -- -- 0.077 0.119 0.012 16.4 10.9 23298 0.252 0.429 0.794 0.012 0.001 0.037 0.479 10.02 0.267 2.957 0.0378 -- -- 0.076 0.447 0.015 19.6 9.07 12899 0.146 0.093 0.967 0.026 0.001 0.081 0.241 11.24 0.928 0.867 0.0828 -- -- 0.013 0.370 0.005 23.0 4.02 250100 0.109 0.072 0.449 0.039 0.007 0.099 0.159 11.86 0.210 1.484 0.0758 -- -- 0.042 0.363 0.011 23.7 12.2 174__________________________________________________________________________ CS: Creep rupture strength at 650.degree. C., 150 thousand hours VE: Charpy absorption energy at 0.degree. C. after aging at 700.degree. C for 10 thousand hours TO: Oxidation scale thickness after oxidation at 650.degree. C. for 10 thousand hours in air
TABLE 3__________________________________________________________________________(Wt. %) Invention Steels CS kg/ VE TONo. C Si Mn P S Nb V Cr Mo W Zr Ta Hf Ti N O mm.sup.2 kgf .multidot. .mu.m__________________________________________________________________________101 0.048 0.124 0.995 0.018 0.007 0.060 0.091 10.28 0.779 1.508 -- 0.544 -- 0.089 0.297 0.011 23.3 8.29 153102 0.161 0.777 0.344 0.030 0.008 0.084 0.112 9.88 0.817 1.368 -- 0.675 -- 0.080 0.447 0.017 23.9 8.96 142103 0.071 0.230 0.250 0.023 0.002 0.088 0.319 9.16 0.039 1.591 -- 0.772 -- 0.078 0.489 0.004 17.2 9.70 241104 0.117 0.196 0.870 0.025 0.005 0.042 0.341 9.06 0.106 2.627 -- 0.021 -- 0.055 0.298 0.013 20.2 6.30 182105 0.213 0.034 0.746 0.023 0.005 0.064 0.261 10.46 0.216 1.174 -- 0.912 -- 0.072 0.148 0.010 24.7 15.3 215106 0.269 0.288 0.436 0.025 0.008 0.074 0.393 11.91 0.560 1.502 -- 0.319 -- 0.056 0.320 0.009 17.5 4.28 144107 0.045 0.313 0.479 0.018 0.006 0.089 0.367 9.22 0.323 1.528 -- 0.065 -- 0.025 0.478 0.011 15.8 4.09 225108 0.037 0.273 0.642 0.030 0.006 0.030 0.498 8.45 0.696 1.762 -- 0.328 -- 0.041 0.111 0.013 16.2 10.2 108109 0.296 0.702 0.674 0.028 0.005 0.064 0.195 8.04 0.374 1.422 -- 0.249 -- 0.029 0.288 0.017 20.5 11.1 120110 0.146 0.540 0.288 0.038 0.009 0.109 0.427 11.18 0.007 2.138 -- 0.524 -- 0.051 0.270 0.017 20.8 16.6 142111 0.229 0.767 0.884 0.031 0.006 0.037 0.399 11.64 0.328 1.998 0.0334 0.049 -- 0.036 0.157 0.018 24.0 15.4 127112 0.163 0.324 0.984 0.032 0.003 0.064 0.411 12.66 0.495 2.660 0.0659 0.047 -- 0.045 0.407 0.012 21.7 16.9 101113 0.290 0.149 0.750 0.049 0.006 0.059 0.327 10.27 0.721 0.882 0.0903 0.122 -- 0.049 0.302 0.005 16.0 9.83 168114 0.083 0.381 0.717 0.030 0.003 0.041 0.445 10.29 0.162 0.807 0.0752 0.171 -- 0.065 0.110 0.007 18.6 3.81 132115 0.035 0.393 0.647 0.042 0.004 0.029 0.184 11.29 0.028 2.970 0.0407 0.012 -- 0.066 0.113 0.014 21.6 15.5 171116 0.201 0.330 0.284 0.013 0.008 0.042 0.076 11.60 0.498 1.561 0.0525 0.221 -- 0.066 0.385 0.011 16.7 12.4 162117 0.196 0.341 0.991 0.029 0.010 0.049 0.210 9.76 0.268 2.087 0.0831 0.154 -- 0.042 0.197 0.019 15.9 11.3 134118 0.078 0.566 0.501 0.020 0.008 0.067 0.436 9.15 0.017 1.210 0.0477 0.130 -- 0.051 0.228 0.005 20.9 7.80 115119 0.045 0.378 0.571 0.031 0.004 0.116 0.173 10.69 0.434 1.936 0.0174 0.110 -- 0.022 0.352 0.010 23.7 4.41 208120 0.152 0.305 0.955 0.011 0.009 0.116 0.175 10.36 0.709 0.994 0.0109 0.342 -- 0.018 0.442 0.009 16.3 10.9 217121 0.019 0.109 0.995 0.028 0.006 0.084 0.075 9.06 0.024 2.564 -- -- 0.724 0.098 0.175 0.014 20.3 15.7 168122 0.278 0.720 0.852 0.048 0.001 0.088 0.187 10.28 0.576 0.894 -- -- 0.621 0.056 0.429 0.012 17.6 14.5 239123 0.256 0.312 0.250 0.038 0.006 0.099 0.362 12.31 0.033 2.664 -- -- 0.611 0.043 0.265 0.004 15.4 3.17 238124 0.162 0.623 0.574 0.028 0.003 0.084 0.246 11.30 0.109 0.891 -- -- 0.874 0.076 0.179 0.005 20.3 4.99 112125 0.186 0.225 0.758 0.044 0.008 0.114 0.141 8.06 0.971 2.284 -- -- 0.124 0.038 0.232 0.008 19.2 15.8 119126 0.244 0.047 0.555 0.033 0.010 0.106 0.138 8.62 0.831 2.322 -- -- 0.515 0.079 0.105 0.008 19.1 10.3 210127 0.097 0.613 0.502 0.024 0.009 0.028 0.083 11.27 0.843 2.655 -- -- 0.737 0.037 0.267 0.008 16.7 11.8 111128 0.085 0.525 0.366 0.023 0.008 0.050 0.076 12.07 0.223 2.580 -- -- 0.500 0.018 0.199 0.001 19.0 9.18 229129 0.127 0.312 0.687 0.018 0.008 0.040 0.190 11.90 0.637 2.537 -- -- 0.477 0.086 0.174 0.011 22.8 5.04 215130 0.126 0.121 0.821 0.017 0.001 0.068 0.066 11.73 0.291 1.743 -- -- 0.354 0.075 0.266 0.012 15.0 15.8 171131 0.137 0.096 0.512 0.027 0.005 0.051 0.459 9.96 0.855 1.909 0.0215 -- 0.320 0.049 0.150 0.010 17.5 9.31 203132 0.216 0.391 0.323 0.016 0.006 0.060 0.335 10.11 0.043 2.292 0.0553 -- 0.083 0.070 0.303 0.006 17.2 16.2 113133 0.273 0.367 0.387 0.031 0.010 0.062 0.446 10.52 0.014 0.811 0.0056 -- 0.295 0.063 0.401 0.004 15.9 4.00 228134 0.213 0.554 0.462 0.040 0.005 0.076 0.203 9.67 0.464 1.706 0.0411 -- 0.658 0.045 0.310 0.016 20.5 10.3 202135 0.095 0.720 0.299 0.049 0.003 0.021 0.368 8.51 0.087 1.695 0.0810 -- 0.864 0.080 0.116 0.002 22.9 9.79 214136 0.117 0.226 0.843 0.048 0.001 0.117 0.349 12.93 0.068 1.256 0.0452 -- 0.607 0.094 0.490 0.018 15.0 5.13 215137 0.040 0.771 0.648 0.022 0.009 0.029 0.230 11.41 0.586 0.839 0.0996 -- 0.060 0.058 0.303 0.014 18.6 5.78 234138 0.213 0.552 0.253 0.040 0.001 0.029 0.314 9.81 0.328 2.143 0.0647 -- 0.899 0.078 0.231 0.010 15.5 14.4 150139 0.254 0.514 0.628 0.029 0.003 0.084 0.469 9.17 0.988 1.925 0.0089 -- 0.834 0.038 0.357 0.011 22.6 12.7 213140 0.068 0.391 0.306 0.016 0.002 0.064 0.104 12.89 0.265 1.905 0.0516 -- 0.560 0.089 0.347 0.011 17.0 3.45 156141 0.295 0.339 0.648 0.010 0.009 0.039 0.204 11.91 0.336 2.541 -- 0.090 0.744 0.023 0.479 0.013 15.5 3.05 155142 0.121 0.123 0.203 0.037 0.008 0.025 0.401 12.19 0.886 0.572 -- 0.022 0.588 0.038 0.433 0.003 19.8 14.2 237143 0.176 0.651 0.714 0.046 0.009 0.042 0.102 9.61 0.107 1.418 -- 0.250 0.271 0.059 0.275 0.011 21.9 4.61 132144 0.225 0.131 0.336 0.043 0.001 0.059 0.293 10.13 0.177 0.586 -- 0.039 0.477 0.013 0.286 0.003 18.7 4.80 242145 0.035 0.667 0.427 0.037 0.007 0.096 0.167 9.79 0.309 1.075 -- 0.019 0.413 0.054 0.344 0.003 22.1 10.5 222146 0.093 0.048 0.722 0.014 0.008 0.068 0.246 9.38 0.660 0.774 -- 0.330 0.245 0.062 0.317 0.004 23.8 3.14 246147 0.019 0.771 0.981 0.022 0.008 0.048 0.170 9.91 0.437 2.723 -- 0.168 0.670 0.010 0.483 0.010 20.9 13.6 122148 0.158 0.251 0.952 0.049 0.006 0.102 0.473 9.82 0.320 1.099 -- 0.162 0.376 0.093 0.319 0.014 20.1 9.29 174149 0.128 0.189 0.780 0.022 0.003 0.099 0.338 10.00 0.494 1.381 -- 0.438 0.049 0.060 0.296 0.002 18.3 6.92 133150 0.273 0.731 0.616 0.049 0.010 0.059 0.299 11.40 0.153 2.779 -- 0.045 0.859 0.061 0.489 0.005 17.5 9.10 249__________________________________________________________________________ CS: Creep rupture strength at 650.degree. C., 150 thousand hours VE: Charpy absorption energy at 0.degree. C. after aging at 700.degree. C for 10 thousand hours TO: Oxidation scale thickness after oxidation at 650.degree. C. for 10 thousand hours in air
TABLE 4__________________________________________________________________________(Wt. %) Invention Steels CS kg/ VE TONo. C Si Mn P S Nb V Cr Mo W Zr Ta Hf Ti N O mm.sup.2 kgf .multidot. .mu.m__________________________________________________________________________151 0.213 0.079 0.214 0.017 0.005 0.049 0.220 12.50 0.975 0.789 0.0684 0.078 0.529 0.025 0.376 0.008 24.4 4.45 104152 0.149 0.326 0.523 0.013 0.004 0.039 0.178 11.70 0.161 0.844 0.0017 0.542 0.220 0.056 0.430 0.014 16.0 16.5 248153 0.132 0.057 0.488 0.026 0.009 0.047 0.263 9.93 0.382 2.180 0.0271 0.297 0.619 0.038 0.125 0.018 24.1 6.08 111154 0.073 0.589 0.264 0.042 0.008 0.093 0.331 10.64 0.833 1.516 0.0632 0.034 0.427 0.032 0.338 0.013 20.6 3.65 244155 0.028 0.512 0.402 0.029 0.003 0.045 0.469 9.80 0.213 1.841 0.0787 0.263 0.824 0.011 0.145 0.005 22.4 5.02 229156 0.197 0.361 0.251 0.015 0.004 0.021 0.309 10.82 0.689 1.083 0.0423 0.036 0.997 0.081 0.420 0.004 21.3 12.4 238157 0.048 0.663 0.354 0.027 0.008 0.090 0.387 12.09 0.960 0.982 0.0724 0.166 0.641 0.079 0.234 0.005 24.3 8.05 231158 0.222 0.409 0.472 0.013 0.004 0.022 0.337 12.12 0.218 2.006 0.0384 0.280 0.936 0.066 0.268 0.003 18.2 15.0 231159 0.191 0.515 0.348 0.019 0.007 0.084 0.469 11.84 0.642 2.134 0.0582 0.195 0.571 0.060 0.394 0.019 19.8 8.23 119160 0.153 0.738 0.528 0.034 0.005 0.097 0.413 12.12 0.414 1.796 0.0023 0.271 0.732 0.033 0.485 0.011 21.2 4.30 222__________________________________________________________________________ CS: Creep rupture strength at 650.degree. C., 150 thousand hours VE: Charpy absorption energy at 0.degree. C. after aging at 700.degree. C for 10 thousand hours TO: Oxidation scale thickness after oxidation at 650.degree. C. for 10 thousand hours in air
TABLE 5__________________________________________________________________________(Wt. %) Comparison Steels CS VE (kg/ (kgf TOultidot.No. C Si Mn P S Nb V Cr Mo W Zr Ta Hf Ti N O mm.sup.2) m) (.mu.m)__________________________________________________________________________161 0.080 0.054 0.572 0.016 0.007 0.075 0.121 8.66 0.011 1.162 0.011 0.255 0.161 0.045 0.087 0.0021 11.4 3.2 420162 0.092 0.076 0.323 0.017 0.006 0.045 0.201 11.51 0.095 1.514 0.008 0.344 0.055 0.037 0.032 0.0021 10.3 3.1 430163 0.121 0.101 0.812 0.003 0.005 0.042 0.222 9.22 0.252 1.889 0.077 0.337 0.056 0.036 0.524 0.0045 16.1 0.2 120164 0.137 0.110 0.271 0.004 0.006 0.043 0.232 10.99 0.341 2.005 0.001 0.188 0.164 0.012 0.667 0.0078 19.9 0.7 90165 0.075 0.141 0.457 0.045 0.006 0.037 0.313 9.21 0.516 0.447 0.003 0.345 0.122 0.017 0.124 0.0065 7.5 8.7 140166 0.099 0.080 0.724 0.042 0.009 0.048 0.344 9.33 0.557 2.123 0.131 0.895 0.016 0.025 0.155 0.0043 15.5 0.4 130167 0.102 0.156 0.889 0.027 0.002 0.062 0.411 9.45 0.616 1.156 0.015 1.212 0.999 0.066 0.166 0.0152 19.4 0.1 80168 0.033 0.092 0.233 0.018 0.002 0.063 0.056 9.13 0.709 0.871 0.045 0.962 1.045 0.088 0.176 0.0117 16.7 0.1 120169 0.052 0.244 0.475 0.021 0.002 0.051 0.099 10.56 0.989 0.558 0.099 0.037 0.087 0.119 0.201 0.0169 17.1 0.3 80170 0.071 0.163 0.502 0.016 0.003 0.049 0.212 9.15 0.442 2.002 0.020 -- -- -- 0.223 0.0051 3.1 0.2 110__________________________________________________________________________ CS: Creep rupture strength at 650.degree. C., 150 thousand hours VE: Charpy absorption energy at 0.degree. C. after aging at 700.degree. C for 10 thousand hours TO: Oxidation scale thickness after oxidation at 650.degree. C. for 10 thousand hours in air
The present invention provides a high-nitrogen ferritic heat-resisting steel exhibiting a high rupture strength after prolonged creep and superior high-temperature oxidation resistance and, as such, can be expected to make a major contribution to industrial progress.

Number	Date	Country
54-102221	Aug 1979	JPX
64-129282	May 1989	JPX

Method of production of high-nitrogen ferritic heat-resisting steel

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