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WO2016123715A1 - Alliages de nickel-chrome-fer présentant une résistance améliorée à la fissuration par corrosion sous contrainte dans des environnements nucléaires - Google Patents

Alliages de nickel-chrome-fer présentant une résistance améliorée à la fissuration par corrosion sous contrainte dans des environnements nucléaires Download PDF

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WO2016123715A1
WO2016123715A1 PCT/CA2016/050104 CA2016050104W WO2016123715A1 WO 2016123715 A1 WO2016123715 A1 WO 2016123715A1 CA 2016050104 W CA2016050104 W CA 2016050104W WO 2016123715 A1 WO2016123715 A1 WO 2016123715A1
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Prior art keywords
alloy
alloys
scc
article
figures
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Inventor
Robert L. TAPPING
Roger W. STAEHLE
Koji Arioka
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Atomic Energy of Canada Ltd AECL
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Atomic Energy of Canada Ltd AECL
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Priority to CA2975304A priority Critical patent/CA2975304A1/fr
Priority to EP16746041.9A priority patent/EP3253898A4/fr
Priority to US15/547,134 priority patent/US20180010222A1/en
Publication of WO2016123715A1 publication Critical patent/WO2016123715A1/fr
Anticipated expiration legal-status Critical
Ceased legal-status Critical Current

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    • 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
    • C—CHEMISTRY; METALLURGY
    • C21—METALLURGY OF IRON
    • C21D—MODIFYING THE PHYSICAL STRUCTURE OF FERROUS METALS; GENERAL DEVICES FOR HEAT TREATMENT OF FERROUS OR NON-FERROUS METALS OR ALLOYS; MAKING METAL MALLEABLE, e.g. BY DECARBURISATION OR TEMPERING
    • C21D1/00—General methods or devices for heat treatment, e.g. annealing, hardening, quenching or tempering
    • C21D1/26—Methods of annealing
    • C—CHEMISTRY; METALLURGY
    • C21—METALLURGY OF IRON
    • C21D—MODIFYING THE PHYSICAL STRUCTURE OF FERROUS METALS; GENERAL DEVICES FOR HEAT TREATMENT OF FERROUS OR NON-FERROUS METALS OR ALLOYS; MAKING METAL MALLEABLE, e.g. BY DECARBURISATION OR TEMPERING
    • C21D1/00—General methods or devices for heat treatment, e.g. annealing, hardening, quenching or tempering
    • C21D1/26—Methods of annealing
    • C21D1/28—Normalising
    • C—CHEMISTRY; METALLURGY
    • C21—METALLURGY OF IRON
    • C21D—MODIFYING THE PHYSICAL STRUCTURE OF FERROUS METALS; GENERAL DEVICES FOR HEAT TREATMENT OF FERROUS OR NON-FERROUS METALS OR ALLOYS; MAKING METAL MALLEABLE, e.g. BY DECARBURISATION OR TEMPERING
    • C21D6/00—Heat treatment of ferrous alloys
    • C21D6/004—Heat treatment of ferrous alloys containing Cr and Ni
    • 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
    • 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
    • C22C38/02—Ferrous alloys, e.g. steel alloys containing silicon
    • 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
    • C22C38/04—Ferrous alloys, e.g. steel alloys containing manganese
    • 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
    • C22C38/06—Ferrous alloys, e.g. steel alloys containing aluminium
    • 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
    • C22C38/42—Ferrous alloys, e.g. steel alloys containing chromium with nickel with copper
    • F—MECHANICAL ENGINEERING; LIGHTING; HEATING; WEAPONS; BLASTING
    • F01—MACHINES OR ENGINES IN GENERAL; ENGINE PLANTS IN GENERAL; STEAM ENGINES
    • F01K—STEAM ENGINE PLANTS; STEAM ACCUMULATORS; ENGINE PLANTS NOT OTHERWISE PROVIDED FOR; ENGINES USING SPECIAL WORKING FLUIDS OR CYCLES
    • F01K5/00—Plants characterised by use of means for storing steam in an alkali to increase steam pressure, e.g. of Honigmann or Koenemann type
    • F—MECHANICAL ENGINEERING; LIGHTING; HEATING; WEAPONS; BLASTING
    • F22—STEAM GENERATION
    • F22B—METHODS OF STEAM GENERATION; STEAM BOILERS
    • F22B37/00—Component parts or details of steam boilers
    • F22B37/02—Component parts or details of steam boilers applicable to more than one kind or type of steam boiler
    • F22B37/10—Water tubes; Accessories therefor
    • F22B37/107—Protection of water tubes
    • G—PHYSICS
    • G21—NUCLEAR PHYSICS; NUCLEAR ENGINEERING
    • G21D—NUCLEAR POWER PLANT
    • G21D1/00—Details of nuclear power plant
    • G21D1/006—Details of nuclear power plant primary side of steam generators
    • C—CHEMISTRY; METALLURGY
    • C21—METALLURGY OF IRON
    • C21D—MODIFYING THE PHYSICAL STRUCTURE OF FERROUS METALS; GENERAL DEVICES FOR HEAT TREATMENT OF FERROUS OR NON-FERROUS METALS OR ALLOYS; MAKING METAL MALLEABLE, e.g. BY DECARBURISATION OR TEMPERING
    • C21D2211/00—Microstructure comprising significant phases
    • C21D2211/004—Dispersions; Precipitations
    • Y—GENERAL TAGGING OF NEW TECHNOLOGICAL DEVELOPMENTS; GENERAL TAGGING OF CROSS-SECTIONAL TECHNOLOGIES SPANNING OVER SEVERAL SECTIONS OF THE IPC; TECHNICAL SUBJECTS COVERED BY FORMER USPC CROSS-REFERENCE ART COLLECTIONS [XRACs] AND DIGESTS
    • Y02—TECHNOLOGIES OR APPLICATIONS FOR MITIGATION OR ADAPTATION AGAINST CLIMATE CHANGE
    • Y02E—REDUCTION OF GREENHOUSE GAS [GHG] EMISSIONS, RELATED TO ENERGY GENERATION, TRANSMISSION OR DISTRIBUTION
    • Y02E30/00—Energy generation of nuclear origin
    • Y—GENERAL TAGGING OF NEW TECHNOLOGICAL DEVELOPMENTS; GENERAL TAGGING OF CROSS-SECTIONAL TECHNOLOGIES SPANNING OVER SEVERAL SECTIONS OF THE IPC; TECHNICAL SUBJECTS COVERED BY FORMER USPC CROSS-REFERENCE ART COLLECTIONS [XRACs] AND DIGESTS
    • Y02—TECHNOLOGIES OR APPLICATIONS FOR MITIGATION OR ADAPTATION AGAINST CLIMATE CHANGE
    • Y02E—REDUCTION OF GREENHOUSE GAS [GHG] EMISSIONS, RELATED TO ENERGY GENERATION, TRANSMISSION OR DISTRIBUTION
    • Y02E30/00—Energy generation of nuclear origin
    • Y02E30/30—Nuclear fission reactors

Definitions

  • the present disclosure relates to materials science and corrosion engineering.
  • Nickel-chromium-iron Alloy 800 As currently used in nuclear and other applications, has good corrosion resistance, especially resistance to stress corrosion cracking (SCC).
  • a Ni-Cr-Fe alloy with improved resistance to stress corrosion cracking in nuclear environments may have between about 23 and 28 wt% Cr. In some examples, the alloy may have between about 24 to 27 wt% Cr, or about 25 wt% Cr. In some examples, the alloy may have between about 25 and 35 wt% Ni, or between about 32 and 35 wt% Ni.
  • the alloy may have about 32 wt% Ni and about 25 wt% Cr, or about 25 wt% Ni and about 25 wt% Cr, or about 35 wt% Ni and about 25 wt% Cr, or about 32 wt% Ni and about 27 wt% Cr.
  • the alloy may further have: ⁇ 0.03 wt% C; ⁇ 0.70 wt% Si; ⁇ 1 .0 wt% Mn; ⁇ 0.015 wt% S; > 0.35 wt% Ti; between 0.15 and 0.45 wt% Al; ⁇ 0.75 wt% Cu; ⁇ 0.03 wt% N; > 12 Ti/C; and balance substantially Fe.
  • the alloy may be used in a nuclear reactor.
  • the alloy may be used in steam generator tubing of a nuclear reactor.
  • a method of producing an article may include: providing the alloy as disclosed herein; forming the alloy into the article; and heat treating the article.
  • the step of heat treating may consist of solution annealing the article at at least about 1000°C for at least about 3 minutes, or between about 1050°C to 1 100°C for at least about 3 minutes, or at about 1075°C for about 1 hour.
  • the method may further include, after the step of heat treating, rapidly cooling the article.
  • the step of forming may include cold working the article to about 20%.
  • the article may have an average grain size of about 100 ⁇ .
  • FIG 1 is a drawing of a compact tension (CT) specimen
  • Figure 2 is an image of a CT specimen with fatigue pre-crack before testing
  • Figure 3A is a graph showing crack growth vs. cavity formation for cold-worked (CW) carbon steel in creep and SCC conditions;
  • Figure 3B is a graph showing crack growth vs. cavity formation rates for CW Alloy 600 (UNS N06600) and Alloy 690 (UNS N06690);
  • Figure 4A is a graph showing temperature, conductivity and dissolved hydrogen vs. time in pressurized water reactor (PWR) primary water at 360°C (20%CW, 32%Ni-27%Cr-Fe, 1075°C x 1 h W.C.);
  • Figure 4B is a graph showing temperature, conductivity and dissolved hydrogen vs. time in PWR primary water at 360°C (20%CW, 35%Ni- 25%Cr-Fe, 1075°C x 1 h W.C.);
  • Figure 4C is a graph showing temperature, conductivity and dissolved hydrogen vs. time in PWR primary water at 360°C (20%CW, 25%Ni- 25%Cr-Fe, 1075°C x 1 h W.C.);
  • Figures 5A and 5B show fracture surfaces after testing in PWR primary water at 360°C (20%CW, 32%Ni-27%Cr-Fe, 1075°C x 1 h W.C.) (12.5mm'));
  • Figures 6A and 6B show fracture surfaces after testing in PWR primary water at 360°C (20%CW, 35%Ni-25%Cr-Fe, 1075°C x 1 h W.C.) (12.5mm 1 ));
  • Figures 7A and 7B show fracture surfaces after testing in PWR primary water at 360°C (20%CW, 25%Ni-25%Cr-Fe, 1075°C x 1 h W.C.) (12.5mm 1 ));
  • Figure 8A is a graph showing temperature, conductivity and dissolved hydrogen vs. time in PWR primary water at 340°C (20%CW, 32%Ni- 27%Cr-Fe, 1075°C x 1 h W.C);
  • Figure 8B is a graph showing temperature, conductivity and dissolved hydrogen vs. time in PWR primary water at 340°C (20%CW, 35%Ni- 25%Cr-Fe, 1075°C x 1 h W.C.);
  • Figure 8C is a graph showing temperature, conductivity and dissolved hydrogen vs. time in PWR primary water at 340°C (20%CW, 25%Ni- 25%Cr-Fe, 1075°C x 1 h W.C.);
  • Figures 9A and 9B show fracture surfaces after testing in PWR primary water at 340°C (20%CW, 32%Ni-27%Cr-Fe, 1075°C x 1 h W.C.) (12.5mm'));
  • Figures 10A and 10B show fracture surfaces after testing in PWR primary water at 340°C (20%CW, 35%Ni-25%Cr-Fe, 1075°C x 1 h W.C.) (12.5mm'));
  • Figures 1 1 A and 1 1 B show fracture surfaces after testing in PWR primary water at 340°C (20%CW, 25%Ni-25%Cr-Fe, 1075°C x 1 h W.C.) (12.5mm'));
  • Figure 12A is a graph showing temperature, conductivity and dissolved hydrogen vs. time in PWR primary water at 320°C (20%CW, 32%Ni- 27%Cr-Fe, 1075°C x 1 h W.C);
  • Figure 12B is a graph showing temperature, conductivity and dissolved hydrogen vs. time in PWR primary water at 320°C (20%CW, 35%Ni- 25%Cr-Fe, 1075°C x 1 h W.C);
  • Figure 12C is a graph showing temperature, conductivity and dissolved hydrogen vs. time in PWR primary water at 320°C (20%CW, 25%Ni- 25%Cr-Fe, 1075°C x 1 h W.C);
  • Figures 13A and 13B show fracture surfaces after testing in PWR primary water at 320°C (20%CW, 32%Ni-27%Cr-Fe, 1075°C x 1 h W.C.) (12.5mm')); Figures 14A and 14B show fracture surfaces after testing in PWR primary water at 320°C (20%CW, 35%Ni-25%Cr-Fe, 1075°C x 1 h W.C.) (12.5mm'));
  • Figures 15A and 15B show fracture surfaces after testing in PWR primary water at 320°C (20%CW, 25%Ni-25%Cr-Fe, 1075°C x 1 h W.C.) (12.5mm'));
  • Figure 16A is a graph showing temperature, conductivity and dissolved hydrogen vs. time in PWR primary water at 290°C (20%CW, 32%Ni- 27%Cr-Fe, 1075°C x 1 h W.C);
  • Figure 16B is a graph showing temperature, conductivity and dissolved hydrogen vs. time in PWR primary water at 290°C (20%CW, 35%Ni- 25%Cr-Fe, 1075°C x 1 h W.C);
  • Figure 16C is a graph showing temperature, conductivity and dissolved hydrogen vs. time in PWR primary water at 290°C (20%CW, 25%Ni- 25%Cr-Fe, 1075°C x 1 h W.C);
  • Figures 17A and 17B show fracture surfaces after testing in PWR primary water at 290°C (20%CW, 32%Ni-27%Cr-Fe, 1075°C x 1 h W.C.) (12.5mm'));
  • Figures 18A and 18B show fracture surfaces after testing in PWR primary water at 290°C (20%CW, 35%Ni-25%Cr-Fe, 1075°C x 1 h W.C.) (12.5mm'));
  • Figures 19A and 19B show fracture surfaces after testing in PWR primary water at 290°C (20%CW, 25%Ni-25%Cr-Fe, 1075°C x 1 h W.C.) (12.5mm'));
  • Figures 20A, 20B and 20C show scanning electron microscope (SEM) images of the surface after testing on the bottom of the CT specimens;
  • Figures 21A, 21 B, 21 C, 21 D, 21 E, 21 F, 21G, 21 H, 211 and 21J show Auger electron spectroscopy (AES) mapping of the cross section after testing on the bottom of the CT specimens;
  • Figures 22A, 22B and 22C show SEM images of the cross section after testing on the bottom of the CT specimens;
  • Figures 23A and 23B show fracture surfaces after testing in air at 460°C (20%CW, 32%Ni-25%Cr-Fe, 1075°C x 1 h W.C.) (12.5mm'));
  • Figures 24A and 24B show fracture surfaces after testing in air at 440°C (20%CW, 32%Ni-25%Cr-Fe, 1075°C x 1 h W.C.) (12.5mm'));
  • Figures 25A and 25B show fracture surfaces after testing in air at 425°C (20%CW, 32%Ni-25%Cr-Fe, 1075°C x 1 h W.C.) (12.5mm'));
  • Figures 26A and 26B show fracture surfaces after testing in air at 445°C (19%CW, 34%Ni-22%Cr-Fe, 1065°C x 10m A.C.) (1 1 mm'));
  • Figure 27A is a graph showing SCC growth rate vs. Cr concentration for alloys in PWR primary water at 360°C;
  • Figures 27B and 27E are graphs showing SCC growth rate vs. Cr concentration for alloys in PWR primary water at 320°C;
  • Figures 27C and 27D are graphs showing SCC growth rate vs. Cr concentration for alloys in PWR primary water at 290°C;
  • Figures 28A and 28B are graphs showing SCC growth rate vs. 1/T for alloys in PWR primary water
  • Figures 29A and 29B show SEM images of the surface after testing on the bottom of the CT specimens
  • Figure 30A is a graph showing parabolic law vs. 1/T for alloys in PWR primary water
  • Figure 30B is a graph showing SCC initiation time vs. 1/T for alloys in PWR primary water
  • Figure 30C is a graph showing crack growth rate vs. 1/T for alloys in PWR primary water.
  • Figure 30D is a graph showing discharged vacancies vs. time for two sizes of grains.
  • the present disclosure relates to optimizing the material specification of Alloy 800 to give reliable SCC resistance in initiation and propagation during long term exposures, for example, to at least 80 years in Canada Deuterium Uranium (CANDU) reactor and PWR primary systems.
  • Materials considered herein are modifications of Alloy 800 with different concentrations of Cr and Ni.
  • the measured SCC growth rates were compared with rates obtained previously for Alloys 690 (61 % Ni) and 316 (10% Ni) in PWR primary water. Furthermore, measured SCC growth rates were compared with other test results of alloys with variations of nickel and chromium.
  • Alloys of the present disclosure may provide significantly improved resistance to SCC compared to Alloy 800 alloys currently available. Thus, the alloys of the present disclosure may be useful for applications where Alloy 800 is currently used, and potentially other applications where Ni-Cr and austenitic stainless steels are used.
  • Alloys of the present disclosure may provide improved corrosion resistance, which becomes an economic benefit if the improved material reduces instances of component failure and results also in longer life of materials and components in service.
  • alloys of the present disclosure may have commercial benefits for manufacturers of Ni-Cr-Fe alloys, and in particular for suppliers of materials to the nuclear industry, and potentially also to the suppliers of materials for all other applications that use Alloy 800 or related materials.
  • Rates of SCC growth were measured in the range of temperatures between 290°C and 360°C in PWR primary water using 20% cold rolled CT specimens. The specimens were broken after testing by fatigue in air. The fracture surfaces were analyzed using SEM to determine the crack morphology and the depth of IGSCC. Maximum IGSCC depths were determined using SCC depth data that are measured from at least four points. SCC crack growth rate was calculated by equation (1 ):
  • Tests were performed under constant load conditions without dynamic loading in the test environment at 360°C, 340°C, 320°C and 290°C.
  • the initial K value was 30MPam 1 ⁇ 2 in all cases.
  • Rates of SCC growth were measured in test facilities at 360°C, 340°C, 320°C and 290°C in typical PWR primary water, which contains boric acid (H 3 BO 3 , 500ppm as B), lithium hydroxide (LiOH, 2ppm as Li), and dissolved hydrogen (DH, -30 cc/kg H 2 0).
  • the concentration of hydrogen was adjusted by bubbling an appropriate gas pressure through the solution in the storage tank at room temperature before the solution is pumped into the autoclaves; hydrogen and oxygen were measured at ambient temperatures using a hydrogen and oxygen gas monitor. Dissolved oxygen was controlled to less than 5ppb through the testing.
  • the depth of intergranular corrosion was measured by SEM observation in cross sectional view using focussed ion beam (FIB) of the bottom of CT specimens to characterize the Cr concentration and temperature with peak.
  • Film analyses by AES were performed on specimens after testing in PWR primary water at 290°C, 320°C, 340°C and 360°C. These measurements provided information on the cause of the measured temperature dependence.
  • Rates of creep crack growth were measured at 425°C, 440°C and 460°C in air using -20% cold rolled CT specimens of solution annealed 32%Ni- 25%Cr-Fe alloy (1075°C x 1 h W.C.). Furthermore, 19%CW 34%Ni-22%Cr (1065°C x 10m A.C.) with fine grains was tested at 445°C to confirm the reproducibility of the results at 460°C to examine effects of grain size. Tests were performed under constant load conditions without dynamic loading in the test environment. The initial K value was 40MPam 1 ⁇ 2 in all cases. Specimens were broken by fatigue in air after testing. The fracture surfaces were analyzed using SEM to determine the crack morphology and the depth of creep crack. Maximum creep crack depth was determined using creep crack depth data that are measured from at least four points. Creep crack growth rate was calculated by equation (2):
  • Test conditions of test 1 at 360°C are summarized in Figures 4A, 4B and 4C.
  • Test duration in test 1 was 5,233 h.
  • Water chemistries of the test environments were well controlled during testing. After testing, the specimens were broken by fatigue in air to determine the depth of SCC and fracture morphologies. The observed results of the fracture surfaces of test specimens are shown in Figures 5A, 5B, 6A, 6B, 7A and 7B.
  • Test conditions of test 2 at 340°C are summarized in Figures 8A, 8B and 8C.
  • Test duration in test 2 was 5,233 h.
  • Water chemistries of the test environments were well controlled during the testing. After testing, the specimens were broken by fatigue in air to determine the depth of SCC and the fracture morphologies. The observed results of the fracture surfaces of the specimens are shown in Figures 9A, 9B, 10A, 10B, 1 1A and 1 1 B.
  • Test conditions of test 3 at 320°C are summarized in Figures 12A, 12B and 12C.
  • Test duration in test 3 was 6,609 h.
  • Water chemistries of the test environments were well controlled during the testing. After testing, the specimens were broken by fatigue in air to determine the depth of SCC and the fracture morphologies. The observed results of the fracture surfaces of test specimens are shown in Figures 13A, 13B, 14A, 14B, 15A and 15B.
  • Test conditions of test 4 at 290°C are summarized in Figures 16A, 16B and 16C.
  • Test duration in test 4 was 6, 155 h.
  • Water chemistries of the test environments were well controlled during the testing. After testing, the specimens were broken by fatigue in air to determine the depth of SCC and the fracture morphologies. The observed results of the fracture surfaces of test specimens are shown in Figures 17A, 17B, 18A, 18B, 19A and 19B.
  • Test durations were between 4,030 h and 9,590 h. After testing, the specimens were broken by fatigue in air to determine the depth of creep cracking and the fracture morphologies. The results of observations on fracture surfaces are shown in Figures 23A, 23B, 24A, 24B, 25A, 25B, 26A and 26B.
  • the peak of the SCC growth rate of the Ni-Cr-Fe alloys seems to be in the range of temperatures between 320°C and 290°C, judging from results obtained for 32%Ni-16%Cr-Fe alloy, as shown in Figure 28A.
  • Thickness of inner layer (mm) (K p ⁇ time) 1 / 2 (3)
  • carbide precipitation may accelerate cavity formation, by providing nucleation sites for cavities, thereby enhancing the rate of cavity formation near the carbides.
  • Evidence for this correlation includes the rapid crack growth in carbide precipitated alloy in a double heat treatment at 1075°C x 1 h + 900°C x 1 h.
  • solution annealed alloy in a single high temperature heat treatment is better for the Ni- Cr-Fe alloys described herein so as to not precipitate carbides.
  • rapid cavity formation may occur in material with small grains, for example, SG tubing relative to thick components such as control rod drive mechanism (CRDM) housings.
  • CRDM control rod drive mechanism
  • An estimated crack initiation time for Alloy 690 TT with large grains may be about 100 years at operating temperature (320°C), based on an extrapolated value in Figure 30B.
  • the estimated time may decrease by a factor of ten. Consequently, the estimated SCC initiation time may be about 10 years.
  • the degree of cold work may alter these influences.
  • the rate of intergranular crack growth may be about 100 times slower for solution annealed 32%Ni-25%Cr-Fe than for Alloy 690 TT.
  • carbide precipitated 32%Ni-25%Cr-Fe alloy may be about 100 times faster than for solution annealed 32%Ni-25%Cr-Fe alloy.
  • the estimated SCC initiation time caused by cavity formation of 20%CW Alloy 690 TT with large size of grains ( ⁇ 100 ⁇ ) is estimated to be about 100 years, based on the extrapolated value at 320°C, as shown in Figure 30B. Taking into account the grain size effect described above, the estimated SCC initiation time with fine grains may be assumed to be about ten years, although other effects, such as degree of cold work may be considered. No significant effect of Cr concentration on the rate of cavity formation was observed in the range of Cr concentration between 20% and 25%.
  • Ni-Cr-Fe alloys described herein produced excellent crack initiation resistance relative to Alloy 690 from the point of view of resistance of cavity formation.
  • Lower cavity formation rates may yield an initiation rate for Ni-Cr-Fe alloys described herein that is about 100 times less than an initiation rate for Alloy 690.
  • a significant increase in rates of cavity formation may occur with carbide precipitation and small grain sizes. Therefore, a high temperature final heat treatment followed by rapid cooling may produce a low rate of cavity formation for the Ni-Cr-Fe alloys described herein.
  • the heat treatment of the Ni-Cr-Fe alloys described herein may be carried out at a temperature of at least 1000°C, for a minimum of 3 minutes, and followed by rapid water cooling. More particularly, the heat treatment may be carried out in the range of 1050-1 100°C.
  • the intent for the Ni-Cr-Fe alloys is to avoid carbide precipitation, which may occur below 1050°C. There may be no specified maximum time because the total time may be determined by the thickness of the material, and thus how long it takes the material to get to temperature. Once at temperature, a time of 3 minutes or possibly more may be required.
  • a thin wall e.g., 1 mm
  • 3 minutes the time it takes to go through an annealing furnace
  • Maximum times may depend on material thicknesses, initial conditions, etc., and may be optimized according to product specifications, including grain size, surface cleanliness, hardness, etc.

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Abstract

L'invention porte sur un alliage de Ni-Cr-Fe présentant une résistance améliorée à la fissuration par corrosion sous contrainte dans des environnements nucléaires, l'alliage comprenant 23 à 28 % en poids de Cr, 25 à 35 % en poids de Ni, < 0,03 % en poids de C, < 0,70 % en poids de Si, < 1,0 % en poids de Mn, < 0,015 % en poids de S, > 0,35 % en poids de Ti, 0,15 à 0,45 % en poids d'Al et < 0,75 % en poids de Cu, le reste étant du Fe et des impuretés fortuites. L'alliage peut être utilisé dans une tuyauterie de générateur de vapeur d'un réacteur nucléaire. L'invention porte également sur un procédé de fabrication d'un article comprenant : l'utilisation de l'alliage selon la présente invention ; le formage de l'alliage en l'article par écrouissage de l'alliage à 20 % ; et le traitement thermique de l'article.
PCT/CA2016/050104 2015-02-06 2016-02-05 Alliages de nickel-chrome-fer présentant une résistance améliorée à la fissuration par corrosion sous contrainte dans des environnements nucléaires Ceased WO2016123715A1 (fr)

Priority Applications (3)

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CA2975304A CA2975304A1 (fr) 2015-02-06 2016-02-05 Alliages de nickel-chrome-fer presentant une resistance amelioree a la fissuration par corrosion sous contrainte dans des environnements nucleaires
EP16746041.9A EP3253898A4 (fr) 2015-02-06 2016-02-05 Alliages de nickel-chrome-fer présentant une résistance améliorée à la fissuration par corrosion sous contrainte dans des environnements nucléaires
US15/547,134 US20180010222A1 (en) 2015-02-06 2016-02-05 Nickel-chromium-iron alloys with improved resistance to stress corrosion cracking in nuclear environments

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CN113528928A (zh) * 2021-07-15 2021-10-22 山西太钢不锈钢股份有限公司 精密带钢用铁镍基合金连铸坯及其生产方法

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