US20190100826A1 - Ni-Fe-Cr Alloy - Google Patents

Ni-Fe-Cr Alloy Download PDF

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US20190100826A1
US20190100826A1 US16/089,395 US201616089395A US2019100826A1 US 20190100826 A1 US20190100826 A1 US 20190100826A1 US 201616089395 A US201616089395 A US 201616089395A US 2019100826 A1 US2019100826 A1 US 2019100826A1
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alloy
content
average grain
rel
grain size
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Kiyoko Takeda
Takamitsu Takagi
Hirokazu Okada
Masaaki Terunuma
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Nippon Steel Corp
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Nippon Steel Corp
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    • C—CHEMISTRY; METALLURGY
    • C22—METALLURGY; FERROUS OR NON-FERROUS ALLOYS; TREATMENT OF ALLOYS OR NON-FERROUS METALS
    • C22C—ALLOYS
    • C22C30/00—Alloys containing less than 50% by weight of each constituent
    • C22C30/02—Alloys containing less than 50% by weight of each constituent containing copper
    • C—CHEMISTRY; METALLURGY
    • C22—METALLURGY; FERROUS OR NON-FERROUS ALLOYS; TREATMENT OF ALLOYS OR NON-FERROUS METALS
    • C22C—ALLOYS
    • C22C38/00—Ferrous alloys, e.g. steel alloys
    • C—CHEMISTRY; METALLURGY
    • C22—METALLURGY; FERROUS OR NON-FERROUS ALLOYS; TREATMENT OF ALLOYS OR NON-FERROUS METALS
    • C22C—ALLOYS
    • C22C38/00—Ferrous alloys, e.g. steel alloys
    • C22C38/18—Ferrous alloys, e.g. steel alloys containing chromium
    • C22C38/40—Ferrous alloys, e.g. steel alloys containing chromium with nickel
    • C22C38/50—Ferrous alloys, e.g. steel alloys containing chromium with nickel with titanium or zirconium

Definitions

  • Installations such as reheating furnace pipes, in a petroleum refining plant and a petrochemical plant are used under high-temperature environments. In addition, those installations are brought into contact with process fluid including sulfides and/or chlorides. Therefore, a material used for the installations is required to have an excellent corrosion resistance.
  • Ni-based alloys or Ni—Fe—Cr alloys having excellent corrosion resistances typically Alloy825 (TM), are used.
  • Patent Literature 1 Japanese Patent Application Publication No. 61-227148
  • Patent Literature 2 Japanese Patent Application Publication No. 6-240407
  • Patent Literature 1 A high-nickel alloy disclosed in Patent Literature 1 consisting of, in mass percent, C: 0.1% or less, Si: 1.0% or less, Mn: 1.5% or less, S: 0.015% or less, Ni: 30.0 to 30.5%, Cr: 19.0 to 25.0%, Cu: 1.0% or less, Al: 0.1 to 1.0%, Ti: 0.05 to 1.0%, and Nb: 0.05 to 1.0%, with the balance being iron and unavoidable impurities, and satisfies conditions of (3Ti+Nb)/S ⁇ 150 and (Ti+Nb)/C ⁇ 15.
  • Patent Literature 1 describes that the high-nickel alloy can be thereby given an excellent intergranular corrosion resistance.
  • a high-strength clad steel disclosed in Patent Literature 2 has a base-metal composition consisting of, in mass percent, C: 0.03 to 0.12%, Si: 0.5% or less, Mn: 1 to 1.8%, Nb: 0.06% or less, Mo: 0.25% or less, V: 0.06% or less, and Al: 0.01 to 0.06%, with the balance being Fe and unavoidable impurities.
  • the high-strength clad steel is a Ni-based alloy having a cladding-material composition consisting of C: 0.05% or less.
  • Patent Literature 2 describes that the high-strength clad steel can be provided with an excellent corrosion resistance by heating to 900 to 1030° C., then quenched, and tempering at 500 to 630° C.
  • Patent Literature 1 Japanese Patent Application Publication No. 61-227148
  • Patent Literature 2 Japanese Patent Application Publication No. 6-240407
  • a Ni-based alloy or a Ni—Fe—Cr alloy may be sensitized in a weld heat affected zone when welding is performed.
  • the sensitization may likely cause intergranular corrosion. Therefore, a Ni-based alloy or a Ni—Fe—Cr alloy used under the high-temperature environments described above is required to have an excellent intergranular corrosion resistance achieved by inhibiting the sensitization.
  • An objective of the present invention is to provide a Ni—Fe—Cr alloy having an excellent intergranular corrosion resistance.
  • a Ni—Fe—Cr alloy of the present embodiment has a chemical composition consisting of, in mass percent, C: 0.005 to 0.015%, Si: 0.05 to 0.50%, Mn: 0.05 to 1.5%, P: 0.030% or less, S: 0.020% or less, Cu: 1.0 to 5.0%, Ni: 30.0 to 45.0%, Cr: 18.0 to 30.0%, Mo: 2.0 to 4.5%, Ti: 0.5 to 2.0%, N: 0.001 to 0.015%, and Al: 0 to 0.50%, with the balance being Fe and impurities.
  • An average grain size d ( ⁇ m) satisfies Formula (1):
  • Ni—Fe—Cr alloy according to the present invention has an excellent intergranular corrosion resistance.
  • FIG. 1 is a graph illustrating the relation between relative amount of dissolved C (C rel ), average grain size d ( ⁇ m), and intergranular corrosion resistance.
  • the present inventors conducted studies about the sensitization and intergranular corrosion resistance of Ni—Fe—Cr alloys. As a result, the present inventors obtained the following findings.
  • the sensitization occurs by the following mechanism.
  • Cr carbide precipitates in crystal grain boundaries.
  • the precipitation of Cr carbide consumes Cr present around the crystal grain boundaries. Therefore, when Cr carbide precipitates.
  • Cr-depleted zones develop along the crystal grain boundaries. This phenomenon is called sensitization.
  • sensitization In the Cr-depleted zones, adequate formation of passivation films fails, which leads to a decrease in corrosion resistance, resulting in the occurrence of intergranular corrosion. If an amount of dissolved C in a Ni—Fe—Cr alloy is reduced, the sensitization can be inhibited, which increases the intergranular corrosion resistance.
  • the content of C in a Ni—Fe—Cr alloy is reduced, the amount of dissolved C in the Ni—Fe—Cr alloy is reduced.
  • the content of C is set at 0.005 to 0.015%.
  • C If C is immobilized by Ti in the form of Ti carbide, the amount of dissolved C in the Ni—Fe—Cr alloy can be further reduced. However, if N is present in the Ni—Fe—Cr alloy, Ti nitride precipitates earlier than Ti carbide in solidification because N has a greater affinity for Ti than C. As a result, Ti runs short, failing to immobilize C. Therefore, the content of N is preferably low. Thus, in the present embodiment, the content of N is set at 0.015% or less.
  • the amount of dissolved C in an actual Ni—Fe—Cr alloy is a value determined from the contents of C, Ti, and N in a relative way.
  • a theoretical amount of dissolved C is determined as follows.
  • Amount of dissolved C Content of C in Alloy ⁇ Content of C immobilized by Ti in the form of TiC.
  • Ti precipitates in the form of Ti nitride, and thus the amount of Ti available for the immobilization of C is determined as follows.
  • k 1 is a constant of the amount of dissolved C.
  • an amount of C used in the precipitation of Cr carbide (total precipitation amount of C (C pre )) is as follows, with a solid-solubility limit of C denoted by k 2 (%).
  • the relation between the average grain size d and unit precipitation amount of C (C unit ) is determined as follows.
  • the average grain size is d ( ⁇ m)
  • the grain boundary area of a grain is determined as k 3 ⁇ d 2 ⁇ m 2 (k 3 is a constant).
  • the number of grains per unit volume is k 4 /d 3 (k 4 is a constant)
  • the total grain boundary area is determined as follows.
  • the unit precipitation amount of C (C unit ) is determined as follows.
  • the average grain size d is in proportion to the unit precipitation amount of C (C unit ). In other words, the smaller the average grain size d, the less the unit precipitation amount of C (C unit ), and as a result, the sensitization is inhibited.
  • the present inventors introduced an idea of an index of the intergranular corrosion resistance based on the average grain size d and the amount of C contributing to the precipitation of Cr carbide described above. As a result, the present inventors found that increasing the intergranular corrosion resistance cannot be simply achieved only reducing the average grain size d, and an appropriate average grain size d exists in the relation with the amount of C contributing to the precipitation of Cr carbide.
  • FIG. 1 is a graph illustrating the relation between the amount of C contributing the precipitation of Cr carbide (relative amount of dissolved C (C rel )), the average grain size d ( ⁇ m), and the intergranular corrosion resistance.
  • the horizontal axis represents the formula of the total precipitation amount of C (C pre ) from which the constants k 1 and k 2 are omitted (the relative amount of dissolved C (C rel ) to be described later).
  • FIG. 1 is obtained through Example to be described later.
  • those showed excellent intergranular corrosion resistances are plotted as “ ⁇ ”, and those showed poor intergranular corrosion resistances are plotted as “x”.
  • the average grain size d needs to be decreased with an increase in the total precipitation amount of C (C pre ).
  • the less the total precipitation amount of C (C pre ) the larger the average grain size d can be made.
  • the total precipitation amount of C (C pre ) is in an inversely proportional relation with the average grain size, and is expressed as follows:
  • F1 can be obtained by determining the constants k 1 , k 2 , k 5 and k 6 , with the broken line of FIG. 1 set as a boundary:
  • C rel is the amount of dissolved C determined from the contents of C, Ti, and N in a relative way (the relative amount of dissolved C (C rel )), and defined as follows:
  • the average grain size d needs to be decreased with an increase in the relative amount of dissolved C (C rel ).
  • C rel the relative amount of dissolved C
  • F1 is an index of the intergranular corrosion resistance.
  • the average grain size d is less than F1
  • the average grain size d is proper for the relative amount of dissolved C (C rel ).
  • the unit precipitation amount of C (C unit ) is reduced sufficiently, which inhibits the sensitization.
  • the intergranular corrosion resistance can be increased.
  • the average grain size d is not less than F1
  • the average grain size d is excessively large for the relative amount of dissolved C (C rel ).
  • the unit precipitation amount of C (C unit ) is not reduced sufficiently, which contributes to the sensitization. As a result, the intergranular corrosion resistance is decreased.
  • FIG. 2 is a graph illustrating the relation between the average grain size d ( ⁇ m), the subtraction (F1 ⁇ d) of d from F1, and the intergranular corrosion resistance.
  • FIG. 2 is obtained through Example to be described later, as with FIG. 1 .
  • those showed excellent intergranular corrosion resistances are plotted as “ ⁇ ”, and those showed poor intergranular corrosion resistances are plotted as “x”.
  • Formula (1) when the average grain size d satisfies Formula (1), namely, when F1 ⁇ d makes a positive value, an excellent intergranular corrosion resistance can be provided even when the average grain size d is large.
  • Formula (1) namely, when F1 ⁇ d makes a negative value, the intergranular corrosion resistance decreases even when the average grain size d is small.
  • a Ni—Fe—Cr alloy according to the present embodiment completed based on the above findings has a chemical composition consisting of, in mass percent, C: 0.005 to 0.015%, Si: 0.05 to 0.50%, Mn: 0.05 to 1.5%, P: 0.030% or less, S: 0.020% or less, Cu: 1.0 to 5.0%, Ni: 30.0 to 45.0%, Cr: 18.0 to 30.0%, Mo: 2.0 to 4.5%, Ti: 0.5 to 2.0%, N: 0.001 to 0.015%, and Al: 0 to 0.50%, with the balance being Fe and impurities.
  • An average grain size d ( ⁇ m) satisfies Formula (1):
  • the above chemical composition may contain Al: 0.05 to 0.50%.
  • the chemical composition of the Ni—Fe—Cr alloy according to the present embodiment consisting of the following elements.
  • Carbon (C) increases the strength of the alloy.
  • C deoxidizes the alloy.
  • An excessively low content of C results in failure to provide these effects.
  • an excessively high content of C leads to an increase in precipitation of Cr carbides to grain boundaries, resulting in a decrease in the intergranular corrosion resistance. Consequently, the content of C is 0.005 to 0.015%.
  • a lower limit of the content of C is preferably 0.008%.
  • An upper limit of the content of C is preferably 0.013%, more preferably 0.010%.
  • Si deoxidizes the alloy. An excessively low content of Si results in failure to provide this effect. In contrast, an excessively high content of Si makes inclusions likely to be produced. Consequently, the content of Si is 0.05 to 0.50%. A lower limit of the content of Si is preferably 0.15%, more preferably 0.20%. An upper limit of the content of Si is preferably 0.45%, more preferably 0.40%.
  • Mn deoxidizes the alloy.
  • An excessively low content of Mn results in failure to provide these effects.
  • an excessively high content of Mn causes S to combine with Mn to form a sulfide, which becomes nonmetallic inclusions, resulting in a decrease in pitting resistance. Consequently, the content of Mn is 0.05 to 1.5%.
  • a lower limit of the content of Mn is preferably 0.15%, more preferably 0.30%.
  • An upper limit of the content of Mn is preferably 1.2%, more preferably 1.0%.
  • Phosphorus (P) is an impurity. P segregates in grain boundaries in weld solidification, increasing crack susceptibility that occurs due to embrittlement of a heat affected zone. Therefore, the content of P is 0.030% or less. An upper limit of the content of P is preferably 0.025%, more preferably 0.020%. The content of P is preferably as low as possible.
  • S Sulfur
  • S is an impurity.
  • S segregates in grain boundaries in weld solidification, increasing the crack susceptibility that occurs due to embrittlement of a heat affected zone.
  • S forms MnS, resulting in a decrease in the pitting resistance. Therefore, the content of S is 0.020% or less.
  • An upper limit of the content of S is preferably 0.010%, more preferably 0.005%.
  • the content of S is preferably as low as possible.
  • Copper (Cu) increases the corrosion resistance of the alloy.
  • An excessively low content of Cu results in failure to provide this effect.
  • an excessively high content of Cu results in a decrease in the hot workability of the alloy. Therefore, the content of Cu is 1.0 to 5.0%.
  • a lower limit of the content of Cu is preferably 1.2%, more preferably 1.5%.
  • An upper limit of the content of Cu is preferably 4.0%, more preferably 3.0%.
  • Nickel (Ni) increases the pitting resistance of the alloy. An excessively low content of Ni results in failure to provide this effect. In contrast, an excessively high content of Ni leads to saturation of the effect. Therefore, the content of Ni is 30.0 to 45.0%. A lower limit of the content of Ni is preferably 35.0%, more preferably 38.0%. An upper limit of the content of Ni is preferably 44.5%, more preferably 44.0%.
  • Molybdenum (Mo) increases the corrosion resistance of the alloy.
  • An excessively low content of Mo results in failure to provide this effect.
  • an excessively high content of Mo causes Laves phases to precipitate in grain boundaries in an alloy having a high content of Cr, resulting in a decrease in the corrosion resistance of the alloy. Therefore, the content of Mo is 2.0 to 4.5%.
  • a lower limit of the content of Mo is preferably 2.4%, more preferably 2.8%.
  • An upper limit of the content of Mo is preferably 4.0%, more preferably 3.5%.
  • Titanium (Ti) forms Ti carbide, inhibiting the sensitization of the alloy.
  • An excessively low content of Ti results in failure to provide this effect.
  • an excessively high content of Ti results in a decrease in the hot workability of the alloy. Therefore, the content of Ti is 0.5 to 2.0%.
  • a lower limit of the content of Ti is preferably 0.55%, more preferably 0.60%.
  • An upper limit of the content of Ti is preferably 1.5%, more preferably 1.3%.
  • N Nitrogen
  • N forms fine carbo-nitrides in grains, increasing the strength, and therefore may be contained.
  • an excessively high content of N causes Ti to combine with N to form TiN, which hinders C from being immobilized in the form of Ti carbide, resulting in a decrease in inhibition of sensitization. Therefore, the content of N is 0.001 to 0.015%.
  • a lower limit of the content of N is preferably 0.002%, more preferably 0.005%.
  • An upper limit of the content of N is preferably 0.013%, more preferably 0.010%.
  • Ni—Fe—Cr alloy described above may further contain Al in lieu of Fe.
  • F1 is an index of the intergranular corrosion resistance.
  • the average grain size d is less than F1
  • the average grain size d is proper for the relative amount of dissolved C (C rel ).
  • the unit precipitation amount of C (C unit ) is reduced sufficiently, which inhibits the sensitization.
  • the intergranular corrosion resistance can be increased.
  • the average grain size d is not less than F1
  • the average grain size d is excessively large for the relative amount of dissolved C (C rel ).
  • the unit precipitation amount of C (C unit ) is not reduced sufficiently, which promotes to the sensitization.
  • the intergranular corrosion resistance is decreased.
  • Ni—Fe—Cr alloy according to the present embodiment can be produced by various producing methods. As one example of the producing methods, a producing method for a Ni—Fe—Cr alloy tube will be described below.
  • the starting material is, for example, a hollow billet.
  • the hollow billet can be produced by, for example, machining or vertical piercing.
  • the hollow billet is subjected to hot extrusion working.
  • the hot extrusion working is, for example, the Ugine-Sejoumet process.
  • a Ni—Fe—Cr alloy pipe is produced.
  • the Ni—Fe—Cr alloy tube may be produced by hot working other than the hot extrusion working. The hot working may be repeated several times.
  • a cooling rate to reach a temperature of 900° C. after final hot working is 0.3° C./sec or higher.
  • the cooling rate to reach a temperature of 900° C. after the final hot working is 0.3° C./sec or higher, it is possible to adjust the average grain size d such that the average grain size d satisfies Formula (1).
  • the Ni—Fe—Cr alloy can have an excellent intergranular corrosion resistance.
  • the cooling rate to reach a temperature of 900° C. can be made 0.3° C./sec or higher by performing mist cooling after the final hot working.
  • cold working including cold rolling and/or cold drawing may be performed.
  • Performing the cold working enables the reduction of the average grain size d. In this case, the intergranular corrosion resistance is further increased.
  • a final heat treatment such as solution treatment may be performed to obtain a desired mechanical property.
  • a lower limit of a heat treatment temperature is preferably 900° C., more preferably 915° C., still more preferably 930° C.
  • a lower limit of the heat treatment temperature is preferably 1020° C. In this case, Cr carbide can be dissolved. As a result, the intergranular corrosion resistance can be further inhibited.
  • An upper limit of the heat treatment temperature is preferably 1100° C. more preferably 1080° C., still more preferably 1060° C.
  • an upper limit of the heat treatment temperature is preferably less than 1000° C.
  • a heat treatment temperature less than 1000° C. enables the precipitation of TiC.
  • the heat treatment temperature less than 1000° C. enables the reduction of the average grain size d.
  • the sensitization can be further inhibited.
  • the intergranular corrosion resistance can be further inhibited.
  • the sensitization can be inhibited even when the heat treatment is performed at a high temperature of 1000 to 1100° C.
  • a heat treatment duration of the final heat treatment is preferably 2 to 30 minutes.
  • the description of the above one example of the producing methods has been made about the producing method of a Ni—Fe—Cr alloy tube.
  • the Ni—Fe—Cr alloy may be a plate product, a welded tube, a bar product, or the like.
  • the Ni—Fe—Cr alloy is not limited to a particular product shape.
  • the Ni—Fe—Cr alloy produced by the above producing method has an excellent intergranular corrosion resistance.
  • ingots were produced.
  • each of the respective ingots was subjected to hot forging at 1200° C., then subjected to hot rolling at 1200° C. at a reduction of area of 50%, and further subjected to cold rolling at a reduction of area of 67% to be produced into a plate product having a thickness of 5 mm, a width of 80 mm, and a length of 650 mm.
  • each of the respective ingots was subjected to hot forging at 1200° C. to be produced into a plate product having a thickness of 15 mm, a width of 60 mm, and a length of 290 mm.
  • the cold rolling was not performed.
  • the final heat treatment was performed at heat treatment temperatures and for heat treatment durations shown in Table 2.
  • the plate products subjected to the heat treatment were subjected to rapid cooling (water cooling).
  • the plate products were cut in a direction perpendicular to a rolling direction, and test specimens having a thickness of 5 mm, a width of 20 mm, and a length of 10 mm were taken.
  • the test specimens were each embedded in resin in such a manner that a surface including the rolling direction of the plate product (longitudinal section of the test specimen) becomes an observation surface, and the observation surface was subjected to mirror polish.
  • the polished surface was etched using mixed acid.
  • the etched observation surface was observed under an optical microscope.
  • the average grain size d five visual fields were shot at 100 ⁇ magnification to determine the average grain size d ( ⁇ m).
  • test specimen having a thickness of 5 mm, a width of 10 mm, and a length of 50 mm was taken.
  • the lengthwise direction of the test specimen was parallel to the lengthwise direction of the plate product.
  • the test specimen was subjected to sensitization heat treatment at 700° C. for 60 minutes, which was a simulation of a weld heat affected zone.
  • the surface of the test specimen subjected to the sensitization heat treatment was finished by wet emery polishing at #600, degreased with acetone, and dried.
  • the test specimen was subjected to the intergranular corrosion test according to the ASTM A262 C method, and the intergranular corrosion resistance of the etched test specimen was evaluated.
  • a test bath was a boiled 65% nitric acid, and three batches of an immersion test were performed, the three batches each taking 48 hours. A corrosion loss in each of the batches was measured, and from the corrosion rate in the three batches, the average corrosion rate was calculated.
  • the intergranular corrosion resistance In the evaluation of the intergranular corrosion resistance, when an average corrosion rate of the three batches was not more than 1 g/m 2 hr, the intergranular corrosion resistance was determined to be excellent (shown with “ ⁇ ” in Table 2). When the average corrosion rate was more than 1 g/m 2 hr, the intergranular corrosion resistance was determined to be poor (shown with “x” in Table 2).
  • Test Number 19 the content of Ti was excessively high. This made the hot workability low, making the working unable, and thus Test Number 19 fell outside the test.
  • the cooling rate to reach 900° C. after the final hot working was less than 0.3° C./s. Therefore, even with the heat treatment temperature set at less than 1000° C., the average grain size d was large as compared with Test Number 2, being not less than F1. As a result, the intergranular corrosion resistance was low.
  • the cooling rate to reach 900° C. after the final hot working was less than 0.3° C./s. Therefore, the average grain size d was large as compared with Test Number 3, being not less than F1. As a result, the intergranular corrosion resistance was low.
  • the cooling rate to reach 900° C. after the final hot working was less than 0.3° C./s.
  • the cold rolling was not performed after the hot working. Therefore, even with the heat treatment temperature set at less than 1000° C., the average grain size d was large as compared with Test Number 5, being not less than F1. As a result, the intergranular corrosion resistance was low.

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CA3018312A1 (en) 2017-10-05
SG11201807433RA (en) 2018-09-27
WO2017168904A1 (ja) 2017-10-05
CN109072365A (zh) 2018-12-21
EP3438306A1 (en) 2019-02-06
EP3438306B1 (en) 2021-02-24
JPWO2017168904A1 (ja) 2018-12-27
KR20180125566A (ko) 2018-11-23
CA3018312C (en) 2020-03-10

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