WO2019049792A1 - Procédé de soudure et élément d'assemblage - Google Patents

Procédé de soudure et élément d'assemblage Download PDF

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Publication number
WO2019049792A1
WO2019049792A1 PCT/JP2018/032428 JP2018032428W WO2019049792A1 WO 2019049792 A1 WO2019049792 A1 WO 2019049792A1 JP 2018032428 W JP2018032428 W JP 2018032428W WO 2019049792 A1 WO2019049792 A1 WO 2019049792A1
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Prior art keywords
welding
joint
heat
less
phase stainless
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PCT/JP2018/032428
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English (en)
Japanese (ja)
Inventor
冨村　宏紀
延時　智和
徹 家成
義光 村田
朝田　博
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日新製鋼株式会社
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Publication of WO2019049792A1 publication Critical patent/WO2019049792A1/fr

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    • B—PERFORMING OPERATIONS; TRANSPORTING
    • B23—MACHINE TOOLS; METAL-WORKING NOT OTHERWISE PROVIDED FOR
    • B23K—SOLDERING OR UNSOLDERING; WELDING; CLADDING OR PLATING BY SOLDERING OR WELDING; CUTTING BY APPLYING HEAT LOCALLY, e.g. FLAME CUTTING; WORKING BY LASER BEAM
    • B23K26/00—Working by laser beam, e.g. welding, cutting or boring
    • B23K26/20—Bonding
    • B23K26/21—Bonding by welding
    • B—PERFORMING OPERATIONS; TRANSPORTING
    • B23—MACHINE TOOLS; METAL-WORKING NOT OTHERWISE PROVIDED FOR
    • B23K—SOLDERING OR UNSOLDERING; WELDING; CLADDING OR PLATING BY SOLDERING OR WELDING; CUTTING BY APPLYING HEAT LOCALLY, e.g. FLAME CUTTING; WORKING BY LASER BEAM
    • B23K26/00—Working by laser beam, e.g. welding, cutting or boring
    • B23K26/346—Working by laser beam, e.g. welding, cutting or boring in combination with welding or cutting covered by groups B23K5/00 - B23K25/00, e.g. in combination with resistance welding
    • B23K26/348—Working by laser beam, e.g. welding, cutting or boring in combination with welding or cutting covered by groups B23K5/00 - B23K25/00, e.g. in combination with resistance welding in combination with arc heating, e.g. TIG [tungsten inert gas], MIG [metal inert gas] or plasma welding
    • B—PERFORMING OPERATIONS; TRANSPORTING
    • B23—MACHINE TOOLS; METAL-WORKING NOT OTHERWISE PROVIDED FOR
    • B23K—SOLDERING OR UNSOLDERING; WELDING; CLADDING OR PLATING BY SOLDERING OR WELDING; CUTTING BY APPLYING HEAT LOCALLY, e.g. FLAME CUTTING; WORKING BY LASER BEAM
    • B23K9/00—Arc welding or cutting
    • B23K9/23—Arc welding or cutting taking account of the properties of the materials to be welded
    • 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
    • C22C38/28—Ferrous alloys, e.g. steel alloys containing chromium with titanium or zirconium
    • B—PERFORMING OPERATIONS; TRANSPORTING
    • B23—MACHINE TOOLS; METAL-WORKING NOT OTHERWISE PROVIDED FOR
    • B23K—SOLDERING OR UNSOLDERING; WELDING; CLADDING OR PLATING BY SOLDERING OR WELDING; CUTTING BY APPLYING HEAT LOCALLY, e.g. FLAME CUTTING; WORKING BY LASER BEAM
    • B23K9/00—Arc welding or cutting
    • B23K9/16—Arc welding or cutting making use of shielding gas
    • 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
    • C22C38/58—Ferrous alloys, e.g. steel alloys containing chromium with nickel with more than 1.5% by weight of manganese

Definitions

  • the present invention relates to a welding method and the like for welding ferritic single-phase stainless steels.
  • Laser welding uses (1) high-speed deep penetration welding as compared to arc welding such as TIG welding because it uses a concentrated high energy density heat source, and (2) the effect of welding heat is extremely small. (3) There is a feature that welding deformation is small.
  • Patent Document 1 is a method of refining the crystal grains of a ferrite single phase stainless steel weld metal portion, and when the temperature of the weld portion becomes 400 ° C. or less by penetrating welding with the first laser beam, the corresponding weld portion is lowered.
  • a method of partially welding is provided by irradiating a second laser beam of heat input.
  • this method of refining the grain of the weld metal by using two laser beams does not improve the reduction of the Vickers hardness of the contact bead center and the Vickers hardness of the base material.
  • Patent document 2 preheats to 250 degreeC or more before laser tube welding of ferrite single phase stainless steel, welds the protrusion height of an inner surface bead to 0.15 mm or more, and deteriorates a welding part in the plate thickness direction, and is processed.
  • preheating to at least 250 ° C before laser tube welding is not only a cost problem of attaching a heating device to tube forming equipment, but there is also the concern of a drop in corrosion resistance by applying an oxide film to a stainless steel base material. is there.
  • Japanese Patent Publication Japanese Patent Application Laid-Open No. 8-155665 (June 18, 1996)” Japanese Patent Publication "Japanese Patent Application Laid-Open No. 5-277769 (October 26, 1993)” Japanese patent publication "Tokukai 2015-526295" (released on September 10, 2015)
  • the hardness of the ferrite single-phase stainless steel is significantly increased by welding, as compared with the base material portion. In the welded portion, segregation of alloying elements and coarsening of the structure occur, and many factors of toughness decrease are included. That the hardness of the weld is high, in other words, the ductility is lowered, and it is important to reduce the hardness of the weld.
  • One aspect of the present invention aims to realize a welding method capable of manufacturing a joint member excellent in toughness.
  • welding concerning one mode of the present invention is in mass%, and (1) Ti: 0.05-0.50% and Nb: 0.05-0.50% A single ferrite system containing one or more, (2) C: 0.015% or less, (3) N: 0.020% or less, and (4) Cr: 11.0 to 35.0%.
  • a welding method for welding phase stainless steels comprising: a first heat input process for forming a joint portion in which the ferritic single phase stainless steels are joined by heat input from a first heat source; and the first heat input process Before the temperature of the bonding portion is reduced to 500 ° C./s or less in the temperature range of 1300 ° C. to 700 ° C. before the temperature of the bonding portion is cooled to 700 ° C.
  • a bonding member having excellent toughness can be manufactured.
  • FIG. 6 shows a solubility curve of It is a figure explaining the laser TIG compound welding method concerning the embodiment of the present invention. It is an example of the bead external appearance of the laser TIG composite welding member which concerns on embodiment of this invention. It is an example of the bead section of the laser TIG composite welding member concerning the embodiment of the present invention. It is a graph which shows the relationship of the distance from a bead center part, and a cross-sectional Vickers hardness about a laser * TIG composite welding member and a laser independent welding member which are the examples of the present invention.
  • the inventors of the present application focused attention on the cooling process immediately after welding as a means for reducing the hardness of the welded portion. More specifically, the inventors have found that carbonitrides of Ti and Nb can be precipitated by reducing the cooling rate in the cooling process, and have completed the present invention.
  • the precipitation of Nb-based carbonitrides and Ti-based carbides has temperature dependency of the following (1) and (2).
  • the present inventors precipitate carbides / nitrides of Ti and Nb by slow cooling the temperature range (700 to 1300 ° C.) where carbides / nitrides of Ti and Nb precipitate, and Ti, Nb in steel It has been found that it is possible to prevent solid solution in the matrix, and the present invention has been made.
  • C forms a carbide, which acts as a recrystallization nucleus of the randomization of the recrystallized ferrite in the final annealing.
  • C is an element that raises the strength after cold rolling annealing, and if it is too high, it causes a decrease in ductility, so it is made 0.015% or less.
  • N forms a nitride, which, like C, acts as a recrystallization nucleus of crystal orientation randomization of recrystallized ferrite in the final annealing.
  • N is an element that raises the strength of the cold-rolled annealed material, and if it is too high, it causes a decrease in ductility, so it was made 0.020% or less.
  • Ti is an element that fixes C and N and improves the workability and corrosion resistance, and the minimum amount of the effect is 0.05%.
  • the addition of Ti causes an increase in the cost of steel materials, and surface defects caused by Ti-based inclusions become a problem, so the upper limit of the Ti content was set to 0.50%.
  • Nb is an element that fixes C and N and improves impact resistance and secondary processability, and the minimum amount at which these effects appear is 0.05%. However, if Nb is added too much, the material hardens and adversely affects the processability. Further, the upper limit is made 0.50% because the recrystallization temperature is raised.
  • Cr needs to be contained at 11.0% in order to provide corrosion resistance as stainless steel. However, if the amount of Cr is increased, the toughness and the workability are reduced, so the upper limit of the Cr content is 35.0%.
  • Si is generally used for the purpose of deoxidation, but it has a high solid solution strengthening ability, and if its content is too large, the material hardens and causes a decrease in ductility, so the content is made 0.5% or less.
  • B is an alloy component having the function of fixing N and improving corrosion resistance and workability, and is added as necessary. In order to exhibit the said effect
  • Mo is an element effective for improving the corrosion resistance, but excessive addition causes a decrease in hot workability due to solid solution strengthening at high temperatures and a delay in dynamic recrystallization, so 3.0% or less did.
  • Ni is an austenite-forming element, and addition exceeding 2.0% causes hardening and cost increase, so 2.0% was made the upper limit.
  • Cu is unavoidably contained, such as mixing from scraps at the time of melting, but excessive addition causes the hot workability and corrosion resistance to deteriorate, so the content is made 2.0% or less.
  • Al is an element effective for deoxidation and oxidation resistance, but the upper limit is made 4.0% because excessive addition causes surface defects.
  • Mn is an austenite-forming element, has a small solid solution strengthening ability, and has little adverse effect on the material. However, if the content is high, manufacturability is lowered, for example, Mn fumes are formed during melting, so the component range is desirably made 2.0% or less.
  • P is an element harmful to hot workability.
  • the content exceeds 0.050%, the effect becomes significant, so the content is desirably 0.050% or less.
  • S is an element which is easily segregated at grain boundaries and promotes reduction in hot workability, etc. by grain boundary embrittlement. If the content exceeds 0.020%, the effect becomes significant, so the content is desirably 0.020% or less.
  • V is a useful element in view of processability improvement by the effect of precipitating solid solution C as carbides, and Zr in terms of processability and toughness improvement by capturing oxygen in steel as an oxide.
  • the productivity decreases, so the appropriate content of V and Zr is 0.01 to 0.30%.
  • Ca, Mg, Co, REM (rare earth metal) and the like may be contained in the melt from the scrap which is the raw material, but the ferrite single particle of the present invention is excluded except in the case where it is contained in a large amount. It does not affect the characteristics of duplex stainless welds.
  • the welding method according to one aspect of the present invention comprises, in mass%, one or more of (1) Ti: 0.05 to 0.50%, and Nb: 0.05 to 0.50%, (2) C A welding method for welding ferritic single phase stainless steels containing 0.015% or less, (3) N: 0.020% or less, and (4) Cr: 11.0 to 35.0%. is there.
  • the welding method according to one aspect of the present invention includes a first heat input step and a second heat input step.
  • the first heat source is not particularly limited, and for example, laser welding, TIG welding, plasma welding and the like can be used.
  • the ferrite single-phase stainless steels are melted and joined by heating the ferrite single-phase stainless steel to 1400 ° C. or more, more specifically to 1450 ° C. to 1700 ° C.
  • the second heat input step is a step of performing heat input to the bonded portion by the second heat source before the temperature of the bonded portion is cooled to 700 ° C. after the first heat input step. Specifically, in the temperature range of 1300 ° C. to 700 ° C. of the joint portion, the heat input to the joint portion is performed by the second heat source so that the cooling rate of the joint portion is 500 ° C./s or less. Do.
  • the second heat source is not particularly limited, for example, laser welding, TIG welding, plasma welding and the like can be used. However, since it is preferable to receive heat to the entire joint, the second heat source is preferably TIG welding and plasma welding which can perform heat input over a wider range.
  • the first heat source and the second heat source may be the same type of heat source.
  • a plurality of heat sources may be used as the second heat source. Thereby, the heat input can be applied to the joint in a wider range.
  • FIG. 1 (a) shows solubility curves of niobium nitride (NbN) and niobium carbide (NbC) in pure Fe base
  • FIG. 1 (b) shows titanium nitride (TiN in pure Fe base).
  • solubility curves of titanium carbide (TiC) were determined from theoretical solubility products. The right side of each solubility curve is a precipitation area, and the left side is a solid solution area.
  • NbN precipitates at about 1300 degreeC.
  • the lower limit temperature at which Nb is completely precipitated and Nb can form a solid solution in the ferrite matrix phase is about 700.degree.
  • Nb contained in the ferritic single phase stainless steel in the present invention is Nb: 0.05 to 0.50 mass%
  • the precipitation temperature of NbN is expected to be 700 to 1300 ° C.
  • the deposition temperatures of NbC and TiN are expected to be 700-1100 ° C. and 700-900 ° C., respectively.
  • the diagrams shown in (a) and (b) of FIG. 1 are pure Fe-based solubility curves. Therefore, when an alloying element mainly containing Cr is included as in ferrite single-phase stainless steel, the precipitation temperature range of NbN, NbC and TiN fluctuates somewhat.
  • the deposition amount of NbN, NbC and TiC can be increased in the welded portion.
  • the amount of precipitation of NbN, NbC, and TiC is increased by suppressing the cooling rate of the weld in the temperature range of 700 to 1300 ° C. low using the second heat source. More specifically, NbN, NbC, and NbC are obtained so that the joint member has good toughness by heat input so that the cooling rate of the weld in the temperature range of 700 to 1300 ° C. is 500 ° C./s or less. Deposit TiC.
  • the precipitation amount of NbN, NbC, and TiC is increased when the temperature of the bonding portion is 700 to 1000 ° C. Therefore, it is more preferable to receive heat so that the cooling rate of the weld in the temperature range of 700 to 1000 ° C. is 400 ° C./s or less. Furthermore, the present inventors (1) heat input so that the cooling rate of the weld portion is 900 ° C./s or less in the temperature range of the joint portion of 1300 to 1000 ° C., and (2) It has been found that it is more preferable to receive heat so that the cooling rate of the weld is 400 ° C./s or less in the temperature range of 1000 to 700 ° C.
  • FIG. 2 is a view for explaining TIG leading welding in the laser-TIG composite welding method according to the present invention.
  • reference numeral 1 is a beam of laser light for performing laser welding
  • reference numeral 2 is a TIG welding torch
  • symbol 3 is a ferrite single phase stainless steel material which is a raw material.
  • TIG welding with the TIG welding torch 2 precedes, followed by laser welding with the beam 1 of laser light.
  • FIGS. 3 and 4 show an example of the bead appearance and the bead cross section of a ferrite single-phase stainless steel welded member subjected to laser-TIG composite welding.
  • the ferrite single-phase stainless steel welding member according to the present embodiment is characterized in that spatter is small as shown in FIG. 3 and the undercut is as small as 0.1 mm as shown in FIG.
  • the Vickers hardness at the central portion of the joint is Hv (w)
  • the ferritic single-phase stainless steel is not affected by the thermal effects of the welds.
  • the Vickers hardness of the matrix is Hv (b)
  • a bonding member satisfying Hv (w) ⁇ Hv (b) ⁇ 50 can be obtained.
  • the bonding member in the present embodiment has good toughness because Hv (w) -Hv (b) ⁇ 50. In other words, the bonding member in the present embodiment has good processability.
  • the bonding member in the present embodiment includes one or more compounds selected from carbides of Nb, nitrides of Nb, and carbides of Ti, and the vertical cross section of the bonding portion (with respect to the extending direction of the bonding portion)
  • the area ratio of the above-mentioned compound is 1.8% or more when the vertical cross section is analyzed using FE-EPMA (field emission electron probe micro analysis, field emission electron probe micro analysis).
  • FE-EPMA field emission electron probe micro analysis, field emission electron probe micro analysis
  • Table 1 shows the component compositions of the ferritic single phase stainless steels 1 to 9 used in this example. All numerical values shown in Table 1 are values as mass%.
  • Ferrite-based single-phase stainless steels 1 to 6 shown in Table 1 are ferrite-based single-phase stainless steels satisfying the following condition 1 and ferrite-based single-phase stainless steels 7 to 9 shown in Table 1 do not satisfy the following condition 1 Ferrite-based single-phase stainless steel.
  • Condition 1 One or more of (1) Ti: 0.05 to 0.50% and Nb: 0.05 to 0.50%, (2) C: 0.015% or less, (3) N: 0.020% or less and (4) Cr: 11.0 to 35.0%.
  • the welding was performed by butt welding, and the end face was machined.
  • the welding conditions are as follows.
  • the distance between the torch for performing TIG welding and the beam for performing laser welding was 3 mm.
  • the assist gas for laser welding was used only when performing laser-only welding, and was not used when performing laser-TIG combined welding.
  • Placement TIG leading, or laser leading laser welding: 4 kW power, Spot diameter ⁇ 0.6 mm, Tilt 0 °, Assist gas Ar 100%, 10 L / min TIG welding: Reverse angle 30 °, Current 300A or 400A Arc length 1.5mm, Shield gas Ar 100%, 15 L / min Welding speed: Laser and TIG combined welding 8.0m / min, Laser only welding 4.0m / min TIG welding only 5.0 m / min.
  • Table 2 shows the Vickers hardness Hv (w) of the bead center after laser-TIG composite welding, the Vickers hardness Hv (b) of the base material, and their differences for these joining members. It shows.
  • Vickers hardness was calculated
  • the Vickers hardness of a base material part is defined by the three-point average value in the position of 1.5 mm, 1.75 mm, and 2.0 mm from the bead center before welding.
  • the cooling rate was calculated from the temperature at which the welded portion after welding was measured by a radiation thermometer.
  • the rating rate of the radiation thermometer was set in advance to fit the cooling curve by obtaining a cooling rate by attaching a thermocouple in the vicinity of the plate surface weld.
  • No. 4 which is an invention example of the present application, is heat input and joined such that the cooling rate of the welded portion in the temperature range of 700 to 1300 ° C. is 500 ° C./s or less.
  • the difference between the Vickers hardness (Hv (w)) of the weld bead central portion and the Vickers hardness (Hv (b)) of the base material portion satisfies 50 or less.
  • the difference in Vickers hardness is smaller in TIG welding than in laser welding.
  • No. 5 which is a comparative example of the present invention, is joined by heat input such that the cooling rate of the weld in the temperature range of 700 to 1300 ° C. is higher than 500 ° C./s.
  • the difference between the Vickers hardness (Hv (w)) of the weld bead central portion and the Vickers hardness (Hv (b)) of the base material in the joint members 14 to 18 and 22 was greater than 50. . This is considered to be because the precipitation rate of NbN, NbC and TiC is small because the cooling rate after welding is fast, and the hardness is increased by solid solution strengthening.
  • the amount of Cr contained in the ferritic single phase stainless steel is small, so a martentensite layer is formed during cooling, and the hardness of the bonding portion is increased.
  • the joining members 6 to 8 and 15 differ in the distance between the laser and the TIG in joining. As shown in Table 2, it can be seen that as the laser-TIG distance increases, the cooling effect acts between the two heat source supplies, and the cooling rate increases.
  • FIG. 5 shows No. 1 in Table 1 as the material.
  • No. 4 subjected to laser and TIG composite welding (TIG leading) using No. 4 ferrite single phase stainless steel.
  • No. 11 in which the welding members and the laser alone were welded.
  • It is a graph which shows the relationship of the distance from a bead center part, and a cross-sectional Vickers hardness about 22 joining members.
  • the Vickers hardness is the highest in the bead central part, when comparing the Vickers hardness difference between the bead central part and the base metal part, No. 4 to which laser-TIG composite welding was applied.
  • No. 11 joints were clearly laser-only welded. The increase in hardness is suppressed more than in the joint member 22.
  • the area ratio of the deposit in the weld was determined using FE-EPMA.
  • the conditions are as follows.
  • n was measured as 9 counts
  • a threshold N for identifying precipitates was measured as 20 counts.
  • the ratio of the field of view in which N is at least 20 counts was taken as the area ratio of precipitates.
  • the area ratio of the precipitate calculated by this method is overestimated than the area ratio of the actual precipitate.
  • a V-bending test was conducted using an autograph extrusion test apparatus.
  • the size of the test piece is 20 mm wide ⁇ 60 mm long, and includes a 20 mm wide weld at approximately the center in the length direction.
  • a bending test was performed by pressing a punch having a V-shaped tip so that the position of the welded portion of the test piece is a ridge of bending.
  • the radius of the tip of the punch was 1 mm, and the pressing speed was 30 mm / min.
  • test temperature was adjusted as follows.
  • the test piece equipped with a thermocouple was immersed in liquid nitrogen (-196 ° C), and maintained at that temperature for 1 minute after the temperature of the test piece fell below -180 ° C. Thereafter, the test piece was taken out of liquid nitrogen, and the V-bending test was conducted when the test piece reached -20 ° C. while the temperature of the test piece returned to normal temperature.
  • Table 3 shows the results of measurement of area ratio of precipitates in welds, V-curve test, and strain aging measurement.
  • the joint members 5 to 9 are No. 1 and Comparative example. ⁇ Hv was smaller than that of 15 to 17 bonding members. That is, no. It is understood that in the joints of the joint members 5 to 9, the amounts of Nb and Ti solid-solved in the weld are small.

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Abstract

La présente invention réalise un procédé de soudage avec lequel il est possible de fabriquer un élément d'assemblage ayant une ténacité supérieure. Le procédé de soudage comprend: une première étape d'apport de chaleur pour former une section assemblée dans laquelle des aciers inoxydables à phase unique à base de ferrite sont joints les uns aux autres par apport de chaleur provenant d'une première source de chaleur; et une seconde étape d'apport de chaleur pour apporter de la chaleur à la section assemblée à partir d'une seconde source de chaleur de telle sorte que la vitesse de refroidissement de la section assemblée atteint 500°C/s ou moins tandis que la température de la section assemblée est dans une plage de 1300°C à 700°C après la première étape d'apport de chaleur et avant que la température de la section assemblée diminue jusqu'à 700°C.
PCT/JP2018/032428 2017-09-05 2018-08-31 Procédé de soudure et élément d'assemblage WO2019049792A1 (fr)

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JP2017170492 2017-09-05
JP2017-170492 2017-09-05
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JP2018159239A JP6448844B1 (ja) 2017-09-05 2018-08-28 溶接方法

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Cited By (1)

* Cited by examiner, † Cited by third party
Publication number Priority date Publication date Assignee Title
CN111266739A (zh) * 2020-02-06 2020-06-12 哈尔滨焊接研究院有限公司 一种激光-mig电弧复合焊接低镍含氮奥氏体不锈钢的方法

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CN111975203A (zh) * 2020-06-06 2020-11-24 南京理工大学 一种高氮钢双光束激光+(n-mig)电弧复合焊接方法

Citations (2)

* Cited by examiner, † Cited by third party
Publication number Priority date Publication date Assignee Title
JP2003239019A (ja) * 2002-02-18 2003-08-27 Nisshin Steel Co Ltd 加工性に優れたフェライト系ステンレス鋼電縫管の製造方法
JP2006193770A (ja) * 2005-01-12 2006-07-27 Nippon Steel & Sumikin Stainless Steel Corp 拡管加工性に優れたフェライト系ステンレス鋼溶接管およびその製造方法

Patent Citations (2)

* Cited by examiner, † Cited by third party
Publication number Priority date Publication date Assignee Title
JP2003239019A (ja) * 2002-02-18 2003-08-27 Nisshin Steel Co Ltd 加工性に優れたフェライト系ステンレス鋼電縫管の製造方法
JP2006193770A (ja) * 2005-01-12 2006-07-27 Nippon Steel & Sumikin Stainless Steel Corp 拡管加工性に優れたフェライト系ステンレス鋼溶接管およびその製造方法

Cited By (1)

* Cited by examiner, † Cited by third party
Publication number Priority date Publication date Assignee Title
CN111266739A (zh) * 2020-02-06 2020-06-12 哈尔滨焊接研究院有限公司 一种激光-mig电弧复合焊接低镍含氮奥氏体不锈钢的方法

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