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WO2017038975A1 - Fil pour soudage à l'arc submergé - Google Patents

Fil pour soudage à l'arc submergé Download PDF

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Publication number
WO2017038975A1
WO2017038975A1 PCT/JP2016/075800 JP2016075800W WO2017038975A1 WO 2017038975 A1 WO2017038975 A1 WO 2017038975A1 JP 2016075800 W JP2016075800 W JP 2016075800W WO 2017038975 A1 WO2017038975 A1 WO 2017038975A1
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WIPO (PCT)
Prior art keywords
wire
amount
less
flux
submerged arc
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Application number
PCT/JP2016/075800
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English (en)
Japanese (ja)
Inventor
和也 井海
賢 山下
Original Assignee
株式会社神戸製鋼所
Priority date (The priority date is an assumption and is not a legal conclusion. Google has not performed a legal analysis and makes no representation as to the accuracy of the date listed.)
Filing date
Publication date
Priority claimed from JP2016091902A external-priority patent/JP6760758B2/ja
Application filed by 株式会社神戸製鋼所 filed Critical 株式会社神戸製鋼所
Priority to CN201680050748.XA priority Critical patent/CN107949455B/zh
Priority to KR1020187006052A priority patent/KR102088179B1/ko
Priority to EP16842004.0A priority patent/EP3345716B1/fr
Priority to ES16842004T priority patent/ES2833354T3/es
Publication of WO2017038975A1 publication Critical patent/WO2017038975A1/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
    • B23K35/00—Rods, electrodes, materials, or media, for use in soldering, welding, or cutting
    • B23K35/22—Rods, electrodes, materials, or media, for use in soldering, welding, or cutting characterised by the composition or nature of the material
    • B23K35/24—Selection of soldering or welding materials proper
    • B23K35/30—Selection of soldering or welding materials proper with the principal constituent melting at less than 1550 degrees C
    • 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
    • B23K35/00—Rods, electrodes, materials, or media, for use in soldering, welding, or cutting
    • B23K35/22—Rods, electrodes, materials, or media, for use in soldering, welding, or cutting characterised by the composition or nature of the material
    • B23K35/36—Selection of non-metallic compositions, e.g. coatings, fluxes; Selection of soldering or welding materials, conjoint with selection of non-metallic compositions, both selections being of interest
    • B23K35/362—Selection of compositions of fluxes

Definitions

  • the present invention relates to a wire for submerged arc welding.
  • Thermal power boilers, turbines, and chemical reaction vessels (reactors) for desulfurization and reforming are operated at high temperature and high pressure, so 1.25Cr-0.5Mo steel, 2. Ferritic heat-resistant steels such as 25Cr-1.0Mo steel, 2.25Cr-1.0Mo-V steel, and high Cr-based CSEF steel (Creep Strength Enhanced Ferritic Steel) containing 8% by mass or more of Cr are applied. .
  • the high Cr-based CSEF steel is a ferritic heat-resistant steel that has been subjected to a predetermined heat treatment to precipitate fine carbides to enhance the creep strength.
  • ASTM American Society for Testing and Materials: American Society for Materials Testing
  • ASME American Society of Mechanical Engineers
  • 9Cr-1Mo steel has excellent high-temperature strength and corrosion resistance, and is applied to piping in thermal power generation boilers.
  • high Cr-based CSEF steel has been studied.
  • submerged arc welding of high Cr system CSEF steel generally has high welding heat input and is likely to generate hot cracks (so-called solidification cracks).
  • solidification cracks hot cracks
  • Patent Documents 1 and 2 have been proposed as welding methods for high Cr-based CSEF steel.
  • Patent Document 1 specifically, C: 0.01 to 0.15% (mass%: the same applies hereinafter), Mn: 0.4 to 2.5%, Cr: 8.0 to 11.0% , Mo: 0.5 to 1.2%, Ni: 0.05 to 1.3%, V: 0.03 to 0.30%, Nb: 0.02 to 0.12%, Al: 0.005 Containing 1.5 to 1.5%, N: 0.004 to 0.100%, and Si: 0.05% or less, O: 0.01% or less, CaF 2 : 25 to 70%, One or two types of CaO and MgO: 8 to 30%, Al 2 O 3 , one or two types of ZrO 2 : 2 to 35%, Al: 0.5 to 7%, and SiO 2 : 9Cr-1Mo steel submerged arc welding method has been proposed, characterized by being combined with a welding flux that is limited to 5% or less and substantially does not contain Si. There.
  • Patent Document 2 discloses that, by weight ratio, C: 0.03 to 0.12%, Si: 0.3% or less, Mn: 0.3 to 1.5%, Cr: 8 to 13%, Nb : 0.01 to 0.15%, V: 0.03 to 0.40%, N: 0.01 to 0.08%, with the balance being a wire composed of Fe and inevitable impurities, and CaF 2 : 10
  • submerged arc welding of high Cr-based CSEF steel generally has a problem of high welding heat input and high temperature cracking (so-called solidification cracking).
  • a thermal power generation boiler, a turbine, and a reactor are welded by appropriately combining pipes, tubes, bent steel sheets, and forged rings.
  • the reactor is welded using a member having a plate thickness of 150 to 450 mm and a maximum outer diameter of about 7 m.
  • the submerged arc welding method is generally used in a narrow groove in order to place importance on efficiency.
  • operation at higher temperatures and higher hydrogen partial pressures has been demanded, and application of high Cr CSEF steel has been studied.
  • welds of high Cr CSEF steel have high self-hardness and high temperature cracking. Is likely to occur.
  • Patent Document 1 proposes a component system that achieves both solidification cracking resistance and welding workability by reducing the Si of the wire and flux and adding Al from the flux.
  • SiO 2 is a component that affects the viscosity of slag and affects the bead appearance
  • CaF 2 increases basicity, reduces the amount of O in the weld metal, and improves toughness. Deteriorates the bead shape and slag peelability. Therefore, Patent Document 1 does not sufficiently study welding workability.
  • the invention proposed in Patent Document 2 has a post-weld heat treatment (PWHT) temperature as low as 740 ° C., and in recent years the actual situation of PWHT, which is carried out for a long time in the manufacture of overseas boilers and reactors, etc. There is a gap. Therefore, it is unclear whether the invention proposed in Patent Document 2 can cope with PWHT performed for a long time, that is, the creep strength after a long time PWHT is unknown.
  • the welding workability is determined by the mutual action of the wire component and the flux component, and there is no mention of this point. For example, the range of the amount of wire Cr is very wide, and it is not considered to have the same workability.
  • the present invention has been made in view of the above circumstances, and an object thereof is to provide a wire for submerged arc welding excellent in creep performance, toughness, crack resistance and welding workability.
  • the present inventors have intensively researched and developed to provide a wire for submerged arc welding excellent in creep performance, toughness, crack resistance and welding workability, and solved this by the following knowledge and efforts.
  • the present inventors have designed the chemical composition of the wire for submerged arc welding in an attempt to obtain a weld metal that does not generate hot cracks during welding and has excellent toughness and creep strength after PWHT.
  • (1) reduction of elements that form a low melting point compound in the final solidified part, and (2) reduction of elements that lower the solidification completion temperature are effective. is there.
  • impurities such as P and S.
  • these impurities are already managed at a sufficiently low level industrially, and further reduction in melting capacity is possible. Is difficult.
  • main alloy components such as C and Cr.
  • the precipitate size is increased by PWHT which is performed for a long time while securing / complementing the amount of C reduced for improving hot cracking resistance with other elements. It is necessary to suppress.
  • an increase in the amount of carbonitride forming elements such as Cr, Nb, and V is effective, but an increase in the amount of precipitated carbonitride deteriorates toughness.
  • Mn or Ni which stabilizes the austenite phase and relatively destabilizes the ferrite phase by reducing the alloy components such as Si, Cr and Mo which stabilize the ferrite phase. It is effective to increase the amount of alloy components such as Co.
  • alloy components such as Co.
  • some of these alloy elements change the amount of carbonitride deposited and affect the toughness and creep performance of the deposited metal.
  • the carbonitride referred to here mainly refers to a composite compound of Nb and V carbides and nitrides. Moreover, it is necessary to control the content of these elements so as not to impair the effect (3).
  • the flux component also affects the toughness. Therefore, a predetermined amount of metal fluoride or metal carbonate is added as a flux component for the purpose of ensuring toughness. However, if these addition amounts increase, welding workability such as slag peelability may be deteriorated. Therefore, in order to ensure the workability of welding, it was decided to consider to achieve both high toughness and slag peelability by adding appropriate amounts of Ca, Si, and Al.
  • Ni is concentrated in the final solidified portion during welding to lower the solidification completion temperature and promote hot cracking.
  • Ni does not affect the precipitation amount of carbonitride during PWHT, but destabilizes the carbonitride and promotes growth so that the surface area per unit volume called so-called Ostwald growth is reduced as much as possible.
  • Ostwald growth is reduced as much as possible.
  • the coarsening was promoted and the creep strength was deteriorated. Therefore, by using a low Ni design for the wire for submerged arc welding, high-temperature cracking is suppressed, and the carbonitride is stabilized without degrading toughness by not affecting the amount of carbonitride precipitation. Succeeded in increasing the creep strength.
  • the submerged arc welding wire according to the present invention which has solved the above problems by the knowledge and efforts described above, is a submerged arc welding wire used in combination with a flux, and the wire has a mass per total mass of the wire.
  • % C: 0.03 to 0.13%, Si: 0.05 to 0.50%, Mn: 0.20 to 1.40%, Cr: 8.00 to 10.50%, Mo: 0 .85 to 1.20%, V: 0.15 to 0.30%, Nb: 0.02 to 0.09%, N: 0.03 to 0.09%, and Ni: 0.70 % Or less, P: 0.010% or less, S: 0.010% or less, Cu: 0.30% or less, Al: 0.04% or less, B: 0.0015% or less, O: 0.030% or less
  • the submerged arc welding wire according to the present invention has the above-described chemical components, the total amount of Mn and Ni contained, the ratio of Mn and S contained (Mn / S), Are controlled within the above ranges. Therefore, the submerged arc welding wire according to the present invention does not cause hot cracking during welding, and is excellent in creep strength and toughness after PWHT and excellent in workability.
  • the wire for submerged arc welding according to the present invention is a wire for submerged arc welding used in combination with a flux, and the wire is in mass% with respect to the total mass of the wire, and C: 0.07 to 0.13%.
  • Si 0.05 to 0.50%
  • Mn 0.20 to 1.00%
  • Cr 8.00 to 10.50%
  • Mo 0.85 to 1.20%
  • V 0.15 -0.30%
  • Nb 0.02-0.08%
  • Co: 0.05-0.80% N: 0.03-0.07%
  • Ni 0.50% or less
  • P 0.010% or less
  • O 0.030%
  • the total amount of Mn content and Ni content 0.50 to 1.15%
  • the submerged arc welding wire according to the present invention can obtain more excellent creep performance, toughness, crack resistance and welding workability.
  • the flux is mass% per total mass of the flux, metal fluoride (value converted to F): 1.5 to 11%, metal carbonate (CO 2 (Converted value): 3 to 15%, MgO, Al 2 O 3 , ZrO 2 , TiO 2 , one or more total: 10 to 60%, SiO 2 : 5 to 20%, Mn: 2 0.5% or less, Ni: 0.10% or less, S: 0.010% or less, one or more of Ca, Si, and Al: a total of 0.5 to 2.5%,
  • the Mn amount (%) and Ni amount (%) of the wire component are [Mn] W and [Ni] W , respectively, and the Mn amount (%) and Ni amount (%) of the flux component are [Mn], respectively.
  • the submerged arc welding wire according to the present invention can obtain more excellent creep performance, toughness, crack resistance and welding workability.
  • the wire and the flux contain at least one of Pb and Bi, and the amount of Pb (%) and Bi amount (%) of the component of the wire is [ Pb] W , [Bi] W , where Pb amount (%) and Bi amount (%) of the flux component are [Pb] F and [Bi] F , respectively, [Pb] W + [Bi] It is preferable that W + 0.2 ⁇ [Pb] F + 0.2 ⁇ [Bi] F ⁇ 2.0 ppm.
  • the submerged arc welding wire according to the present invention can obtain better toughness.
  • P P content
  • Sn Sn content
  • Sb
  • the submerged arc welding wire according to the present invention can obtain better toughness.
  • the wire for submerged arc welding according to the present invention is a wire for submerged arc welding used in combination with a flux, and the wire is in mass% with respect to the total mass of the wire, and C: 0.03 to 0.08%.
  • the wire for submerged arc welding according to the present invention can be more excellent in crack resistance and creep performance after a long time PWHT.
  • the wire for submerged arc welding has a V content (%), an Nb content (%), a C content (%), an N content (%), an Ni content (%), and an Mn content (%).
  • Al amount (%) are [V] W , [Nb] W , [C] W , [N] W , [Ni] W , [Mn] W , and [Al] W , respectively ([ C] W + 1.5 ⁇ [N] W ) ⁇ ([V] W + 10 ⁇ [Nb] W ⁇ [Al] W ) / ([Mn] W + [Ni] W ) ⁇ 100 ⁇ 5% Is preferred.
  • the wire for submerged arc welding according to the present invention can have better creep performance after a long time PWHT.
  • the flux is mass% per total mass of the flux, metal fluoride (value converted to F): 1.5 to 11%, metal carbonate (CO 2 (Converted value): 3 to 15%, MgO, Al 2 O 3 , ZrO 2 , TiO 2 , one or more total: 10 to 60%, SiO 2 : 5 to 20%, Mn: 2 0.5% or less, Ni: 0.10% or less, S: 0.010% or less, one or more of Ca, Si, and Al: a total of 0.5 to 2.5%, V amount (%), Nb amount (%), C amount (%), N amount (%), Ni amount (%), Mn amount (%), and Al amount (%) of the wire component are set to [V ] W, [Nb] W, [C] W, [N] W, [Ni] W, [Mn] W, and [Al] W, the Flack Mn amount of component (%), Ni content (%) of each [Mn] F, when the [V ] W, [Nb] W, [C]
  • the wire for submerged arc welding according to the present invention can have better creep performance after a long time PWHT.
  • the wire when the wire further contains Co: 0.05 to 0.80%, and the Co content (%) of the component of the wire is [Co] W , ([C] W + 1.5 ⁇ [N] W ) ⁇ ([V] W + 10 ⁇ [Nb] W ⁇ [Al] W ) / ([Mn] W + 0.1 ⁇ [Mn] F + [Ni] W + [Ni] F + [Co] W ) ⁇ 100 ⁇ 5% is preferable.
  • the wire for submerged arc welding according to the present invention can have better creep performance after a long time PWHT.
  • the submerged arc welding wire according to the present invention is excellent in creep performance, toughness, crack resistance and welding workability.
  • the numerical values before and after connecting with “to” shall include the numerical values, and when not including the numerical values, the numerical values are “less than”, “smaller”, “exceeding”, “greater than”. "With a word such as” Further, “above”, “below”, “ ⁇ ”, and “ ⁇ ” include the numerical values shown, and “ ⁇ ” and “>” do not include the numerical values shown.
  • the wire according to the first embodiment is used in combination with a flux. Any flux can be used, but a suitable flux will be described later.
  • This wire is in mass% with respect to the total mass of the wire, C: 0.03 to 0.13%, Si: 0.05 to 0.50%, Mn: 0.20 to 1.40%, Cr: 8.
  • C (C: 0.03-0.13%) C has a great influence on the hardenability in the weld metal and the amount of carbonitride deposited, and functions as an austenite stabilizing element, and suppresses the remaining of the ⁇ ferrite phase in the weld metal.
  • the amount of C in the weld metal is too small, the amount of carbide precipitated becomes insufficient, and the ⁇ ferrite phase remains and a predetermined creep strength cannot be obtained.
  • the amount of C is too large, the sensitivity to hot cracking increases, and cracking is likely to occur particularly in submerged arc welding in a narrow groove.
  • the C content is 0.03 to 0.13%.
  • the lower limit of the C content is preferably 0.04%, more preferably 0.07%, and even more preferably 0.08%.
  • the upper limit of the C amount is preferably 0.12%.
  • Si 0.05-0.50%
  • Si improves the conformability of the weld bead and functions as a deoxidizer to improve the strength and toughness of the deposited metal. If the amount of Si in the deposited metal is too small, welding workability (for example, weld bead conformability and coalescence) deteriorates, and toughness and creep strength also deteriorate. On the other hand, if the amount of Si is too large, the strength of the deposited metal is remarkably increased and the toughness is deteriorated. Therefore, the Si amount is set to 0.05 to 0.50%. Note that the lower limit of the amount of Si is preferably 0.10%. The upper limit of Si content is preferably 0.40%, more preferably 0.30%.
  • Mn functions as a deoxidizer and improves the toughness of the deposited metal. Further, Mn functions as an austenite stabilizing element and suppresses the remaining of the ⁇ ferrite phase in the deposited metal. If the amount of Mn in the weld metal is too small, a predetermined toughness cannot be obtained, and a soft ⁇ ferrite phase remains in the weld metal to deteriorate the creep strength. On the other hand, if the amount of Mn in the weld metal is too large, the carbonitride is destabilized and the creep strength is deteriorated. As will be described later, Mn also has an effect of mitigating the adverse effect of S on hot cracking. Therefore, the Mn content is 0.20 to 1.40%. The lower limit of the amount of Mn is preferably 0.55%, and more preferably 0.60%. The upper limit of the Mn content is preferably 1.00%, more preferably 0.80%.
  • Cr 8.00 to 10.50% Cr forms a carbonitride during PWHT and increases the creep strength of the deposited metal. If the amount of Cr is too small, the amount of precipitated carbonitride is insufficient and a predetermined creep strength cannot be obtained. On the other hand, if the amount of Cr is too large, the solidification completion temperature is lowered to increase the hot cracking susceptibility, and the ⁇ ferrite phase remains in the deposited metal to deteriorate the creep strength and toughness. Moreover, when there is too much Cr amount, slag peelability will deteriorate significantly. Therefore, the Cr amount is set to 8.00 to 10.50%. The lower limit of the Cr content is preferably 8.40%. The upper limit of Cr content is preferably 9.20%.
  • Mo 0.85-1.20%
  • Mo is solid-solved in the Cr-based carbide or the matrix during PWHT and improves the creep strength of the deposited metal. If the amount of Mo is too small, a predetermined creep strength cannot be obtained. On the other hand, if the amount of Mo is too large, the amount of solid solution in the Cr-based carbide and the matrix is excessively increased, the strength of the deposited metal is remarkably increased, and the toughness is deteriorated. Therefore, the Mo amount is set to 0.85 to 1.20%.
  • the lower limit of the Mo amount is preferably 0.94%.
  • the upper limit of Mo content is preferably 1.05%.
  • V 0.15-0.30%
  • V forms carbonitride during PWHT and improves the creep strength of the deposited metal. If the V amount is too small, a predetermined creep strength cannot be obtained. On the other hand, when the amount of V is too large, the amount of carbonitride deposited is remarkably increased, the strength of the deposited metal is increased, and the toughness is deteriorated. Therefore, the V amount is set to 0.15 to 0.30%.
  • the lower limit of the V amount is preferably 0.21%.
  • the upper limit of the V amount is preferably 0.27%.
  • Nb 0.02 to 0.09%
  • Nb forms carbonitrides during PWHT and improves the creep strength of the deposited metal. If the amount of Nb is too small, a predetermined creep strength cannot be obtained. On the other hand, when the amount of Nb is too large, the amount of carbonitride deposited is significantly increased, the strength of the deposited metal is increased, and the toughness is deteriorated. Moreover, when there is too much Nb amount, slag peelability will deteriorate significantly. Therefore, the Nb content is 0.02 to 0.09%.
  • the lower limit of the Nb amount is preferably 0.04%.
  • the upper limit of the Nb amount is preferably 0.08%, and more preferably 0.07%.
  • N 0.03-0.09% N combines with Cr, V, Nb, etc. during PWHT to form carbonitrides and improves the creep strength of the deposited metal. If the amount of N is too small, a predetermined creep strength cannot be obtained. On the other hand, when the amount of N increases, the amount of carbonitride deposited increases significantly, the strength of the deposited metal increases, and the toughness deteriorates. Furthermore, if the amount of N is too large, N 2 gas generated during the welding process tends to remain in the molten metal, and blow holes are generated. Therefore, the N content is 0.03 to 0.09%.
  • the lower limit of the N amount is preferably 0.04%.
  • the upper limit of the N amount is preferably 0.07%, and more preferably 0.06%.
  • Ni is the most characteristic element in the embodiment of the present invention. Ni is concentrated in the final solidified part during welding, and the solidification completion temperature is lowered to increase the hot cracking susceptibility. Ni also coarsens the size of carbonitride during creep deformation and degrades creep strength. Therefore, the Ni amount is set to 0.70% or less. The amount of Ni is preferably 0.50% or less, and more preferably 0.20% or less.
  • P 0.010% or less
  • P not only forms a low-melting-point compound in the final solidified part at the time of welding and increases the hot cracking susceptibility, but also causes the weld metal to become brittle and degrade toughness. Therefore, the P content is 0.010% or less.
  • the amount of P is preferably 0.006% or less.
  • S (S: 0.010% or less) S combines with Fe during welding to form a low melting point eutectic of Fe—FeS in the final solidified portion, not only increasing the hot cracking property, but also embrittles the weld metal and degrades toughness. Therefore, the S amount is 0.010% or less.
  • the amount of S is preferably 0.007% or less.
  • S has an effect of improving the conformability and slag peelability of the weld bead, and when obtaining this effect, the amount of S is preferably 0.002% or more, and is 0.003% or more. Is more preferable.
  • the Cu amount is set to 0.30% or less.
  • the amount of Cu is preferably 0.10% or less.
  • the Cu amount is 0.30% or less including the coated Cu as described above.
  • Al (Al: 0.04% or less) Al also combines with N to form AlN, reducing the amount of Cr, Nb, and V carbonitrides that are indispensable for ensuring the creep strength, and deteriorating the creep strength.
  • An increase in the amount of Al causes the beads to seize and deteriorates the slag peelability. Further, the yield of elements in the weld metal is improved, the strength is increased, and as a result, the toughness is deteriorated. Therefore, the Al amount is set to 0.04% or less.
  • the Al content is preferably 0.03% or less.
  • B (B: 0.0015% or less) B lowers the final solidification temperature during welding and increases hot cracking susceptibility. Therefore, the B amount is set to 0.0015% or less.
  • the amount of B is preferably 0.0003% or less.
  • O (O: 0.030% or less) O is combined with Si, Mn, Al and the like in the solidification process during welding to form an oxide and increase the amount of slag. Further, the formed oxide acts as a starting point of brittle fracture and deteriorates the toughness of the deposited metal. Therefore, the O amount is 0.030% or less. The amount of O is preferably 0.005% or less.
  • Total amount of Mn and Ni contained 0.50 to 1.75% From the viewpoint of securing toughness, reducing the ⁇ ferrite phase, and securing the creep strength, it is effective to manage the total amount of Mn and Ni contained. That is, it is necessary to define the lower limit of the total amount of Mn and Ni contained from the viewpoint of ensuring toughness, and the total amount of Mn and Ni contained from the viewpoint of reducing the ⁇ ferrite phase and ensuring the creep strength An upper limit is required. Specifically, the total amount of Mn and Ni contained is 0.50 to 1.75%. The lower limit of the total amount of Mn and Ni contained is preferably 0.70%. The upper limit of the total amount of Mn and Ni contained is preferably 1.15%, and more preferably 1.00%.
  • Mn / S (Ratio of Mn content to S content Mn / S: 87 or more) Further, Mn combines with S in the process of welding solidification to form MnS, thereby reducing the above-mentioned adverse effects and reducing hot cracking. In order to obtain such an effect, it is necessary to set the ratio Mn / S ratio Mn / S to be 87 or more. Preferably, the ratio Mn / S of Mn content to S content is 100 or more, more preferably 150 or more.
  • the balance is Fe and inevitable impurities.
  • inevitable impurities include Sn, As, Sb, Pb, Bi, and the like.
  • Sn, As, and Sb may be 0.005% by mass or less, for example, and 0.015% by mass or less in total.
  • Pb and Bi should just be 0.001 mass% or less, for example.
  • the wire according to the first embodiment described above includes the above-described chemical components, the total amount of Mn and Ni contained, and the ratio of Mn and S contained (Mn / S). Each has control over the range. Therefore, by using this wire in combination with an arbitrary flux, hot cracking does not occur during welding, and the creep strength and toughness after PWHT are excellent, and the welding workability is excellent.
  • the chemical components of the wire according to the second embodiment and the wire according to the first embodiment are substantially the same, but the contents of C, Mn, Nb, N, Ni, and S of the wire according to the second embodiment and The total amount of Mn and Ni contained is different from that of the wire according to the first embodiment.
  • the wire according to the second embodiment is different from the wire according to the first embodiment in that it contains Co.
  • the wire according to the second embodiment is C: 0.07 to 0.13%, Si: 0.05 to 0.50%, Mn: 0.20 to mass% with respect to the total mass of the wire. 1.00%, Cr: 8.00 to 10.50%, Mo: 0.85 to 1.20%, V: 0.15 to 0.30%, Nb: 0.02 to 0.08%, Co : 0.05 to 0.80%, N: 0.03 to 0.07%, Ni: 0.50% or less, P: 0.010% or less, S: 0.002 to 0.010 %, Cu: 0.30% or less, Al: 0.04% or less, B: 0.0015% or less, O: 0.030% or less, and the total amount of Mn and Ni contained: 0.50 ⁇ 1.15%, ratio of contained Mn amount to S amount Mn / S: 87 or more, the balance being made of Fe and inevitable impurities.
  • the wire according to the second embodiment has C: 0.07 to 0.13%, Mn: 0.20 to 1.00%, Nb: 0.02 to 0.08%, Co: 0.05 to 0.80%, N: 0.03-0.07%, Ni: 0.50% or less, S: 0.002-0.010%, Total amount of Mn and Ni contained: It is different from the wire according to the first embodiment in that it is 0.50 to 1.15%.
  • Other points of the wire according to the second embodiment are the same as those of the wire according to the first embodiment.
  • Each content of C, Mn, Nb, N, Ni, and S in the wire according to the second embodiment, and the total amount of Mn and Ni contained are different from those in the first embodiment.
  • the reason for limitation is the same as that of the wire according to the first embodiment, description thereof will be omitted, and here, the reason for limiting Co will be described.
  • Co (Co: 0.05-0.80%) Co functions as an austenite stabilizing element. Therefore, Co can suppress the remaining of the ⁇ ferrite phase and improve the creep strength. If the amount of Co is too small, the effect is not exhibited, and if it is too large, the strength of the deposited metal is improved and the toughness is deteriorated. Therefore, the Co content is preferably 0.05 to 0.80%. In order to further satisfy both the creep strength and toughness, the Co content is more preferably 0.10 to 0.75%, and further preferably 0.10 to 0.50%.
  • the wires according to the first embodiment and the second embodiment can be used in combination with any flux, but are preferably used in combination with the flux defined below.
  • flux for example, metal fluoride (value converted to F): 1.5 to 11%, metal carbonate (value converted to CO 2 ): 3 to 5% by mass with respect to the total mass of the flux 15%, total of one or more of MgO, Al 2 O 3 , ZrO 2 , TiO 2 : 10 to 60%, SiO 2 : 5 to 20%, Mn: 2.5% or less, Ni: It preferably contains 0.10% or less, S: 0.010% or less, and one or more of Ca, Si, and Al: a total of 0.5 to 2.5%.
  • Metal fluoride (value converted to F): 1.5 to 11%) Metal fluoride has the effect of reducing the amount of diffusible hydrogen in the weld metal and improving cold cracking resistance, the role of controlling the amount of oxygen in the weld metal, and the effect of adjusting the bead shape.
  • the value obtained by converting the metal fluoride to F is 1.5% or more, the amount of oxygen in the weld metal is reduced and the toughness is improved.
  • the value obtained by converting the metal fluoride into F is 11% or less, the arc is stabilized, and the bead shape and slag peelability are improved.
  • the value obtained by converting the metal fluoride in the flux into F is preferably 1.5 to 11%.
  • the lower limit of the metal fluoride is more preferably 4%.
  • the upper limit of the metal fluoride is more preferably 9%.
  • Examples of the metal fluoride include CaF 2 , AlF 3 , BaF 3 , Na 3 AlF 6 , MgF 2, and NaF. If the value converted to F is the same, the same effect is obtained.
  • Metal carbonate (value converted to CO 2 ): 3 to 15%) CO 2 by metal carbonate has the role of reducing the amount of diffusible hydrogen in the weld metal and improving cold cracking resistance, and controlling the amount of oxygen in the weld metal.
  • the value obtained by converting the metal carbonate into CO 2 is preferably 3% or more.
  • the metal carbonate is a value in terms of CO 2 15% or less, it reduces the amount of oxygen in the weld metal, the toughness is improved, thereby improving the slag removability. Therefore, the value obtained by converting the metal carbonate to CO 2 is preferably 3 to 15%.
  • the lower limit of the metal carbonate is more preferably 5%.
  • the upper limit of the metal carbonate is more preferably 10%.
  • Examples of the metal carbonate include CaCO 3 , BaCO 3, and MgCO 3, but the same effect is obtained when the value converted to CO 2 is the same.
  • MgO, Al 2 O 3 , ZrO 2 and TiO 2 are slag making agents. These slag making agents have the effect of improving the fluidity of the slag and adjusting the bead shape. In the case of the wire according to the embodiment of the present invention, in order to efficiently obtain such an effect, it is preferable that the total of one or more of these is 10% or more. In addition, when the total of one or more of these is 60% or less, slag entrainment hardly occurs and welding workability is improved.
  • the total of one or more of MgO, Al 2 O 3 , ZrO 2 and TiO 2 in the flux is preferably 10 to 60%.
  • Na 2 O, K 2 O, LiO 2 , BaO or the like can be added to the flux as necessary. When adding these, it is preferable to make each 10% or less.
  • SiO 2 has the effect of improving the fluidity of the slag and adjusting the bead shape.
  • the amount of SiO 2 is preferably 5% or more. Further, when the amount of SiO 2 is 20% or less, slag entrainment hardly occurs, and welding workability is improved. Therefore, the amount of SiO 2 in the flux is preferably 5 to 20%.
  • the lower limit of the amount of SiO 2 is more preferably 8%.
  • the upper limit of the amount of SiO 2 is more preferably 15%.
  • This SiO 2 includes SiO 2 derived from water glass used as a binder.
  • Mn in the flux has the same effect as Mn in the wire. That is, Mn in the flux functions as a deoxidizer and improves the toughness of the deposited metal. However, since Mn in the flux is easily segregated in the weld metal, a sufficient effect may not be obtained. Further, most of Mn in the flux becomes slag, so that there is a case where the yield of the weld metal is not sufficient. Basically, Mn is more stable when added from a wire. Therefore, the amount of Mn in the flux is preferably 2.5% or less. The amount of Mn in the flux is more preferably 2.0% or less.
  • Ni in the flux exhibits the same effect as Ni in the wire, and there is a possibility of increasing hot cracking susceptibility by lowering the solidification completion temperature. Moreover, since Ni in the flux is easily segregated in the weld metal, there is a possibility of locally increasing the hot cracking sensitivity. Therefore, the amount of Ni in the flux is preferably 0.10% or less. The amount of Ni in the flux is more preferably 0.05% or less.
  • S in the flux exhibits the same effect as S in the wire and enhances hot cracking sensitivity. Moreover, since S in the flux is easily segregated in the deposited metal, there is a possibility that the hot cracking sensitivity is locally increased. Therefore, the amount of S in the flux is preferably 0.010% or less.
  • Total of one or more of Ca, Si, Al 0.5 to 2.5%)
  • Ca, Si, and Al in the flux act as a deoxidizer and reduce O in the deposited metal.
  • the total of one or more of Ca, Si, and Al in the flux is 0.5% or more, a sufficient deoxidation effect is obtained and the bead appearance is improved. It becomes good.
  • slag peelability improves that the 1 type, or 2 or more types of total in Ca, Si, and Al in a flux is 2.5% or less. Therefore, the total of one or more of Ca, Si and Al in the flux is preferably 0.5 to 2.5%.
  • the relation between the chemical components of the wire and the flux preferably satisfies the following relational expression.
  • the Mn amount (%) and the Ni amount (%) of the above-described wire component are [Mn] W and [Ni] W , respectively, and the Mn amount (%) of the flux component and Ni the amount (percent), respectively [Mn] F, when the [Ni] F, it is preferable to satisfy the following relational expression (1) to (3).
  • the relational expression (1) takes into account the yield of Mn in the wire and flux in the wire according to the embodiment of the present invention.
  • Mn functions as an austenite stabilizing element and suppresses the remaining of the ⁇ ferrite phase in the deposited metal. If the amount of Mn in the weld metal is too small, the predetermined toughness may not be obtained. Also, if the amount of Mn in the weld metal is too small, a soft ⁇ ferrite phase may remain in the weld metal and deteriorate the creep strength. On the other hand, if the amount of Mn in the weld metal is too large, the carbonitride may be destabilized and the creep strength may be deteriorated.
  • the range of the calculated value is preferably 0.55 to 1.00%.
  • the lower limit of the value calculated by the relational expression (1) is more preferably 0.60%.
  • the upper limit of the value calculated by the relational expression (1) is more preferably 0.80%.
  • the relational expression (2) takes into account the yield of Ni in the wire and flux in the wire according to the embodiment of the present invention. Ni may increase the hot cracking susceptibility by lowering the solidification completion temperature. Therefore, as shown by the relational expression (2), the calculated value is preferably 0.50% or less. The value calculated by the relational expression (2) is more preferably 0.20% or less.
  • the relational expression (3) takes into account the yield of Mn and Ni in the wire and flux in the wire according to the embodiment of the present invention. It is preferable to define the lower limit of the total amount of Mn and Ni contained from the viewpoint of securing toughness, and the upper limit of the total amount of Mn and Ni contained from the viewpoint of reducing the ⁇ ferrite phase and ensuring the creep strength. It is preferable to specify. Therefore, as indicated by the relational expression (3), the range of the calculated value is preferably 0.60 to 1.15%.
  • the lower limit of the value calculated by the relational expression (3) in the second embodiment is more preferably 0.70%.
  • the upper limit of the value calculated by the relational expression (3) is more preferably 1.00%.
  • the wire and flux described above can contain at least one of Pb and Bi as an impurity component.
  • the Pb amount (ppm (meaning ppm by mass; the same applies hereinafter)) and Bi amount (ppm) of the above-described wire components are respectively set to [Pb] W . It is preferable that the following relational expression (4) is satisfied when [Bi] W is set and Pb amount (ppm) and Bi amount (ppm) of the flux component are [Pb] F and [Bi] F , respectively.
  • the relational expression (4) takes into account the yields of Pb and Bi in the wire and flux in the wire according to the embodiment of the present invention.
  • Pb and Bi are elements that segregate and become brittle at the grain boundaries by tempering, and may significantly deteriorate toughness. Therefore, as shown by the relational expression (4), the calculated value is preferably 2.0 ppm or less.
  • the value calculated by the relational expression (4) is more preferably 1.5 ppm or less.
  • the wire and flux described above can contain at least one of P, Sn, As, and Sb as an impurity component.
  • the P amount (ppm), the Sn amount (ppm), the As amount (ppm), and the Sb amount (ppm) of the components of the wire described above are set to [P] W , [Sn] W , [As] W , and [Sb] W
  • the flux component P amount (ppm), Sn amount (ppm), As amount (ppm), and Sb amount (ppm) are set to [P] F
  • [Sn] F , [As] F , and [Sb] F it is preferable that the following relational expressions (5) to (7) are satisfied.
  • X 10 ⁇ [P] W + 4 ⁇ [Sn] W + [As] W + 5 ⁇ [Sb] W (5)
  • Y 10 ⁇ [P] F + 4 ⁇ [Sn] F + [As] F + 5 ⁇ [Sb] F (6)
  • the relational expression (7) obtained by substituting the relational expressions (5) and (6) is obtained by considering the yield of P, Sn, As, and Sb in the wire and flux in the wire according to this embodiment. It is. P, Sn, As, and Sb are elements that segregate and become brittle at the crystal grain boundaries by tempering, and may significantly deteriorate toughness. Therefore, the value calculated by the relational expression (7) obtained by substituting the relational expressions (5) and (6) is preferably 1500 ppm or less. The value calculated by the relational expression (7) is more preferably 1200 ppm or less.
  • the submerged arc welding method according to the second embodiment may be performed by combining the wire and flux described in the second embodiment, and is not limited to specific conditions, but can be performed as follows.
  • a multi-electrode method using 2 to 4 electrodes (wires) can be used, and a single electrode method using one electrode can also be used.
  • the wire diameter can be 2.4 to 4.8 mm ⁇ .
  • the power supply polarity may be either DCEP (Direct Current Electrode Positive) or AC (Alternating Current).
  • the wire feeding speed can be 100 to 170 g / min.
  • the welding speed can be 20 to 60 cm / min.
  • the welding current can be 350 to 500 A.
  • the arc voltage can be 29-33V.
  • the welding heat input can be 15 to 25 kJ / cm.
  • the distribution height of the flux can be 25 to 35 mm.
  • the distance between the tip and the base material can be 25 to 35 mm. Since the submerged arc welding method according to the second embodiment uses a combination of the wire and flux described in the second embodiment, it may be excellent in creep performance, toughness, crack resistance, and welding workability. it can.
  • the wire according to the third embodiment contains C: 0.03 to 0.08%, Si: 0.05 to 0.50%, Mn: 0.0. 20 to 1.40%, Cr: 8.00 to 10.50%, Mo: 0.85 to 1.20%, V: 0.15 to 0.30%, Nb: 0.02 to 0.09% N: 0.03 to 0.09%, Ni: 0.70% or less, P: 0.010% or less, S: 0.010% or less, Cu: 0.30% or less, Al: 0.04% or less, B: 0.0015% or less, O: 0.030% or less, the total amount of Mn and Ni contained: 0.60 to 1.75%, the content of Mn and S Ratio of amount Mn / S: 87 or more, total amount of C and N contained: 0.09 to 0.15%, the balance being made of Fe and inevitable impurities .
  • the wire according to the third embodiment contains C: 0.03 to 0.08%, the total amount of Mn and Ni contained: 0.60 to 1.75%, the amount of C and N contained The total amount is 0.09 to 0.15%, which is different from the wire according to the first embodiment.
  • the amount of C and the total amount of Mn and Ni contained in the wire according to the third embodiment have a numerical range narrower than that of the first embodiment, but the reason for limitation is the wire according to the first embodiment. Therefore, the description thereof will be omitted, and here, the total amount of C and N contained will be described.
  • Total amount of C and N contained 0.09 to 0.15%
  • the creep strength is improved when the total amount of the C amount and the N amount is 0.09% or more.
  • toughness improves that the total amount of C amount and N amount is 0.15% or less.
  • the total amount of C and N contained is preferably 0.09 to 0.15%.
  • the lower limit of the total amount of C and N contained is more preferably 0.10%.
  • the upper limit of the total amount of C and N contained is more preferably 0.14%.
  • the wire according to the third embodiment includes a V amount (%), an Nb amount (%), a C amount (%), an N amount (%), an Ni amount (%), and an Mn amount (%).
  • Al content (%) are [V] W , [Nb] W , [C] W , [N] W , [Ni] W , [Mn] W , and [Al] W , respectively, It is preferable to satisfy Expression (8).
  • the relational expression (8) takes into account ensuring the creep performance after long time PWHT.
  • the wire according to this embodiment is designed to positively precipitate carbonitrides mainly composed of Nb and V. These carbonitrides are kept fine even after PWHT for a long time, and are effective in ensuring creep performance.
  • the numerator of this formula is a term representing the amount of effective precipitates, and the denominator is a term affecting the coarsening of the precipitates. That is, the larger the value calculated by the relational expression (8), the more effective the amount and size of the precipitate can be secured for the creep performance.
  • the value calculated by the relational expression (8) is preferably 7% or more, more preferably 10% or more.
  • the above-described flux can be suitably used similarly.
  • the relationship between the wire and the chemical component of the flux preferably satisfies the following relational expression.
  • the wire according to the third embodiment has the following relational expressions (9) to (9) when the Mn amount (%) and the Ni amount (%) of the flux component are [Mn] F and [Ni] F , respectively. It is preferable to satisfy (12). [V] W , [Nb] W , [C] W , [N] W , [Ni] W , [Mn] W , and [Al] W are synonymous with the relational expression (8).
  • the relational expression (9) is exactly the same as the relational expression (1) described in the second embodiment.
  • the numerical range of the relational expression (10) is wider than that of the relational expression (2), the purpose of defining this is for the same reason as the relational expression (2) described in the second embodiment. That is, the relational expression (10) takes into account the yield of Ni in the wire and flux in the third embodiment. Ni may increase the hot cracking susceptibility by lowering the solidification completion temperature. Therefore, as indicated by the relational expression (10) in the third embodiment, the calculated value is preferably 0.70% or less.
  • the value calculated by the relational expression (10) is more preferably 0.50% or less.
  • the value calculated by the relational expression (10) is more preferably 0.30% or less.
  • the relational expression (11) considers the yield of Mn and Ni in the wire and flux in the third embodiment. It is preferable to define the lower limit of the total amount of Mn and Ni contained from the viewpoint of securing toughness, and the upper limit of the total amount of Mn and Ni contained from the viewpoint of reducing the ⁇ ferrite phase and ensuring the creep strength. It is preferable to specify. Therefore, as indicated by the relational expression (11) in the third embodiment, the calculated value range is preferably 0.60 to 1.45%. The lower limit of the value calculated by the relational expression (11) in the third embodiment is more preferably 0.70%. The upper limit of the value calculated by the relational expression (11) in the third embodiment is more preferably 1.35%.
  • the relational expression (12) further considers the yield of Mn and Ni in the wire and flux with respect to the relational expression (8). If the relational expression (12) is satisfied, even when a combination of a wire and a flux is welded in the manufacture of a reactor or the like, the creep strength is unlikely to decrease due to PWHT performed for a long time. That is, if the wire and the flux satisfy the relational expression (12), they can be suitably used for manufacturing a reactor.
  • the wire according to the third embodiment may contain Co: 0.05 to 0.80%.
  • the significance of containing Co and the reason for limiting the content are as described in the second embodiment.
  • the wire which concerns on 3rd Embodiment contains Co, it can use combining an above described flux. In that case, it is preferable to satisfy the following relational expression (13).
  • [Co] W represents the Co content (%) of the wire component.
  • [V] W , [Nb] W , [C] W , [N] W , [Ni] W , [Mn] W , and [Al] W are synonymous with the relational expression (8), and [Mn] F , [Ni] F is synonymous with the relational expression (12).
  • the relational expression (13) is a relational expression (8) that considers the yield of Co in the wire as well as the yield of Mn and Ni in the wire and flux.
  • the relational expression (13) is satisfied, even in the case of manufacturing a reactor or the like, even when the wire and the flux are combined and welded, the creep strength is unlikely to be lowered by PWHT performed for a long time. That is, if the wire and the flux satisfy the relational expression (13), it can be suitably used for manufacturing a reactor.
  • the submerged arc welding method according to the third embodiment may be performed by combining the wire and the flux described in the third embodiment.
  • the submerged arc welding method according to the third embodiment can use the same conditions as the submerged arc welding method according to the second embodiment described above, for example. Since the submerged arc welding method according to the third embodiment uses a combination of the wire and the flux described in the third embodiment, it may have excellent creep performance, toughness, crack resistance, and welding workability. it can. Further, when the welding is performed by the submerged arc welding method according to the third embodiment, the creep strength is not easily lowered by the PWHT performed for a long time. Therefore, the submerged arc welding method according to the third embodiment can be preferably applied particularly to the manufacture of a reactor.
  • Wires having the chemical components shown in Table 1 and fluxes having the chemical components shown in Table 2 were produced.
  • the welding wire was extruded, annealed and drawn after being melted in a high-frequency melting furnace to 2.4 mm ⁇ .
  • Wire numbers 1 to 13 are examples, and wire numbers 14 to 37 are comparative examples.
  • the flux was prepared by mixing predetermined raw materials (fluoride, ore powder containing metal carbonate, molten flux), stirring, granulating with water glass, and sintering at 500 ° C. for about 1 hour.
  • Flux numbers 1 to 5 are examples, and flux numbers 6 to 10 are comparative examples. In Tables 1 and 2, “-” indicates that it is less than the detection limit value.
  • the wires according to numbers 1 to 37 shown in Table 1 and the fluxes according to numbers 1 to 10 shown in Table 2 were combined and welded as shown in Table 4.
  • As the welding power source KRUMC-1000 manufactured by Daihen Co., Ltd., which exhibits drooping characteristics, was used.
  • Table 3 shows welding conditions for submerged arc welding.
  • the groove shape of the test plate which performed the welding test in FIG. 1 is shown.
  • the base material of the test plate is ASTM A387 Gr. 22 was used.
  • the groove surface was battered with a wire to a thickness of about 10 mm. Welding was carried out from the first layer in one layer and two passes, and the bead appearance and slag peelability in the final layer were evaluated as a confirmation test of welding workability.
  • FIG. 3 shows a specimen collection position 10 for a Charpy impact specimen and a specimen collection position 20 for a creep specimen.
  • the toughness of all the deposited metals is “ ⁇ ” when the three-point average of the absorbed energy (vE + 20 ° C.) in the Charpy impact test at 20 ° C. is 65 J or more, “ ⁇ ” when 45 J or more and less than 65 J, and less than 45 J. Evaluated as “x”. ⁇ and ⁇ are acceptable and ⁇ is unacceptable.
  • Table 4 shows combinations of wires and fluxes used for welding, and also shows evaluation results of welding workability, hot crack resistance, toughness, and creep performance.
  • “-” indicates that the element related to the relational expression could not be calculated because it was less than the detection limit.
  • the evaluation results of welding workability and hot cracking resistance were “ ⁇ ”, and the evaluation results of toughness and creep performance were “ ⁇ ”, were evaluated as comprehensive evaluation “ ⁇ ”.
  • the evaluation results of welding workability and hot cracking resistance were “ ⁇ ”, and the evaluation results of toughness or creep performance were “ ⁇ ”.
  • those having at least one “x” were evaluated as comprehensive evaluation “x”.
  • the knowledge was also shown collectively.
  • the wire component and the flux component are suitable.
  • the expressions (1) to (3) were satisfied.
  • These weld specimens particularly satisfy the relational expression (1) and contain Co as a wire component.
  • the welding test body according to 15 uses the wire according to wire number 14 in Table 1.
  • the weld specimen according to No. 15 was inferior in hot cracking resistance and toughness because the amount of C in the wire was too large.
  • the welding test body according to 16 uses the wire according to wire number 15 in Table 1.
  • No. The welded specimen according to 17 uses the wire according to wire number 16 in Table 1.
  • No. The weld specimen of No. 17 was inferior in toughness because the amount of Si in the wire was too large.
  • the welded specimen according to 18 uses the wire according to wire number 17 in Table 1.
  • the weld specimen according to No. 18 was inferior in toughness because the amount of Mn in the wire was too small.
  • the welding test body according to 19 uses the wire according to wire number 18 in Table 1.
  • No. The weld specimen according to No. 19 had inferior creep performance because the wire had too much Mn.
  • the wire according to wire number 18 is an example in which the total amount of Mn and Ni contained in the wire (Mn + Ni amount) satisfies Claim 1 but not Claim 2.
  • the welding test body according to 20 uses the wire according to wire number 19 in Table 1.
  • No. The weld specimen according to No. 20 was inferior in creep performance because the amount of Ni in the wire was too large.
  • wire according to wire number 19 is an example in which the amount of Mn + Ni satisfies claim 1 but not claim 2.
  • the welding test body according to 21 uses a wire according to wire number 20 in Table 1.
  • the weld specimen according to No. 21 was inferior in toughness because the total amount of Mn and Ni contained in the wire (Mn + Ni amount) was too small.
  • the welded specimen according to 22 uses the wire according to wire number 21 in Table 1.
  • No. The weld specimen according to No. 22 had inferior creep performance because the wire had too much Mn + Ni.
  • the wire according to the wire number 21 is an example in which the Mn amount and the Ni amount satisfy Claim 1 but not Claim 2.
  • No. 23 uses a wire according to wire number 22 in Table 1.
  • the weld specimen according to No. 23 had an excessive amount of S in the wire, and the ratio of Mn to S contained in the wire (Mn / S) was too low, so the hot crack resistance and toughness were inferior.
  • the welding test body according to No. 24 uses the wire according to the wire number 23 in Table 1. No. Since the Mn / S of the wire was too low, the weld specimen according to No. 24 was inferior in hot crack resistance.
  • the welded specimen according to No. 25 uses the wire according to the wire number 24 in Table 1.
  • the weld specimen according to No. 25 had inferior hot cracking resistance and toughness because the P content of the wire was too large.
  • the welding test body according to No. 26 uses the wire according to the wire number 25 in Table 1.
  • the welding test body according to No. 27 uses a wire according to wire number 26 in Table 1.
  • No. The weld specimen according to No. 27 had inferior creep performance because the amount of Cr in the wire was too small.
  • the welding test body according to No. 28 uses the wire according to the wire number 27 in Table 1. No.
  • the weld specimen according to No. 28 was inferior in hot crack resistance, toughness and creep performance because the amount of Cr in the wire was too large.
  • the weld specimen according to No. 28 had many seizures, and the slag peelability deteriorated. Therefore, no.
  • the welding test body according to No. 28 was inferior in welding workability.
  • the welded specimen according to 29 uses a wire according to wire number 28 in Table 1.
  • No. The weld specimen of No. 29 was inferior in creep performance because the amount of Mo in the wire was too small.
  • the welding test body according to 30 uses the wire according to wire number 29 in Table 1.
  • No. The weld specimen of No. 30 was inferior in toughness because the amount of Mo in the wire was too large.
  • the welded specimen according to No. 31 uses a wire according to wire number 30 in Table 1.
  • the weld specimen according to No. 31 was inferior in creep performance because the V amount of the wire was too small.
  • the welding test body according to No. 32 uses the wire according to wire number 31 in Table 1.
  • the weld specimen according to No. 32 was inferior in toughness because the V amount of the wire was too large.
  • the welding test body according to No. 33 uses the wire according to the wire number 32 in Table 1.
  • No. The weld specimen according to No. 33 was inferior in welding workability, toughness, and creep performance because the wire had too much Al.
  • the wire according to wire number 32 is an example in which the amount of Mn + Ni satisfies claim 1 but not claim 2. No.
  • the welded specimen according to No. 34 uses the wire according to the wire number 33 in Table 1.
  • No. The weld specimen according to No. 34 was inferior in hot cracking resistance because the amount of B in the wire was too large.
  • No. The welding test body according to 35 uses the wire according to the wire number 34 in Table 1.
  • No. The weld specimen according to No. 35 had inferior creep performance because the amount of Nb in the wire was too small.
  • No. The welding test body according to 36 uses a wire according to wire number 35 in Table 1.
  • No. The weld specimen according to No. 36 was inferior in toughness because the wire had too much Nb.
  • No. The welded test body according to No. 36 had a lot of seizure and the slag peelability deteriorated. Therefore, no.
  • the welding test body according to 36 was inferior in welding workability.
  • the welded specimen according to 37 uses the wire according to wire number 36 in Table 1. No. The weld specimen according to No. 37 had inferior creep performance because the N amount of the wire was too small. No. The welding test body according to No. 38 uses the wire according to the wire number 37 in Table 1. No. The weld specimen according to No. 38 was inferior in toughness because the amount of O in the wire was too large.
  • the welding test body according to No. 39 uses the flux according to the flux number 6 in Table 2.
  • the weld specimen according to No. 39 was inferior in creep performance because the amount of Mn in the flux was too large.
  • the welding test body according to No. 40 uses the flux according to Flux No. 7 in Table 2.
  • the weld specimen according to 40 had inferior creep performance because the amount of Ni in the flux was too large.
  • the welding test body according to 41 uses the flux according to flux number 8 in Table 2. No. Since the welding test body which concerns on 41 had too much S amount of flux, its hot cracking resistance was inferior.
  • the welding test body according to 42 uses the flux according to flux number 9 in Table 2. No.
  • the welding test body according to No. 43 uses the flux according to the flux number 10 in Table 2. No. Since the total amount of Ca, Si, and Al in the flux was too large, the weld specimen according to No. 43 had a lot of seizure and the slag peelability deteriorated. Therefore, no. The weld specimen according to No. 43 had poor welding workability.
  • Wires having the chemical components shown in Table 5 and fluxes having the chemical components shown in Table 6 were produced.
  • the welding wire was extruded, annealed, and drawn after being melted in a high-frequency melting furnace to 3.2 mm ⁇ .
  • Wire numbers 38 to 52 are examples, and wire numbers 53 to 66 are comparative examples.
  • the flux was prepared by mixing predetermined raw materials (fluoride, ore powder containing metal carbonate, molten flux), stirring, granulating with water glass, and sintering at 500 ° C. for about 1 hour. Flux numbers 11 to 13 are examples.
  • Table 7 shows the welding conditions for submerged arc welding.
  • the welding power source was the same as in [First Example].
  • the groove shape of the test plate subjected to the welding test was the same as that described in [First Example] (see FIG. 1). Welding was carried out from the first layer in one layer and two passes, and the bead appearance and slag peelability in the final layer were evaluated as a confirmation test of welding workability.
  • a group subjected to PWHT of 750 ° C. ⁇ 8 hr and a group subjected to PWHT of 750 ° C. ⁇ 32 hr were prepared for each weld specimen.
  • the impact performance of the weld metal part of the weld specimen was evaluated using a group subjected to PWHT at 750 ° C. ⁇ 8 hours.
  • the creep performance of the weld specimen was evaluated using a group subjected to PWHT of 750 ° C. ⁇ 32 hr.
  • the collection part of the test piece was made into the deposit center (welded metal center) and plate
  • the three-point average of absorbed energy (vE + 0 ° C) in the Charpy impact test at 0 ° C is " ⁇ " for 50J or more, " ⁇ " for 38J or more and less than 50J, and less than 38J Was evaluated as “ ⁇ ”. ⁇ and ⁇ are acceptable and ⁇ is unacceptable.
  • the test temperature is 575 ° C.
  • the initial load stress is 170 MPa
  • the creep rupture time (Tr) is 500 h or more, “ ⁇ ”, the 200 h or more and less than 500 h is “ ⁇ ”, the less than 200 h is “ ⁇ ”.
  • ⁇ and ⁇ are acceptable and ⁇ is unacceptable.
  • Table 8 shows combinations of wires and fluxes used for welding, and also shows evaluation results of welding workability, hot crack resistance, toughness, and creep performance.
  • the evaluation results of welding workability and hot cracking resistance were “ ⁇ ”, and the evaluation results of toughness and creep performance were “ ⁇ ”, were evaluated as comprehensive evaluation “ ⁇ ”.
  • the evaluation results of welding workability and hot cracking resistance were “ ⁇ ”, and the evaluation results of toughness or creep performance were “ ⁇ ”.
  • those having at least one “x” were evaluated as comprehensive evaluation “x”.
  • the welded specimen according to 59 uses a wire according to wire number 53 in Table 5.
  • the weld specimen according to No. 59 was inferior in hot cracking resistance because the amount of C in the wire was too large.
  • the weld specimen according to No. 59 had too much total amount of C and N contained in the wire (C + N amount), and this was also inferior in hot crack resistance.
  • the welded specimen according to No. 60 uses the wire according to the wire number 54 in Table 5.
  • No. The weld specimen according to No. 60 was inferior in creep performance because the amount of C in the wire was too small.
  • the welding test body according to 61 uses the wire according to wire number 55 in Table 5. No. The weld specimen according to No.
  • the welded specimen according to 62 uses a wire according to wire number 56 in Table 5.
  • the welded test body according to No. 62 was inferior in toughness because the amount of Mn in the wire was too small and the total amount of Mn and Ni contained in the wire (Mn + Ni amount) was too small.
  • the weld specimen according to 62 also had inferior creep performance.
  • the welding test body according to 63 uses a wire according to wire number 57 in Table 5. No. The weld specimen according to 63 had poor toughness because the wire had too much Nb.
  • the welded test body according to 63 had many seizures, and the slag peelability deteriorated. Therefore, no. The weld specimen according to 63 had poor welding workability.
  • the welding test body according to No. 64 uses the wire according to the wire number 58 in Table 5.
  • the weld specimen according to No. 64 was inferior in creep performance because the amount of Nb in the wire was too small.
  • the welded specimen according to 65 uses a wire according to wire number 59 in Table 5.
  • No. The weld specimen according to No. 65 was inferior in toughness because the amount of N in the wire was too large.
  • the welding test body according to 66 uses a wire according to wire number 60 in Table 5.
  • the welded test body according to No. 66 was inferior in creep performance because the amount of N in the wire was too small.
  • the welding specimen according to No. 67 uses the wire according to the wire number 61 in Table 5.
  • the weld specimen according to No. 67 was inferior in hot cracking resistance because the amount of Ni in the flux was too large.
  • the welding test body according to 68 uses the wire according to wire number 62 in Table 5. No. The weld specimen according to 68 had inferior creep performance because the wire had too much Mn + Ni. No.
  • the welding test body according to 69 uses the wire according to wire number 63 in Table 5. No. The weld specimen according to 69 had poor toughness because the amount of Mn + Ni in the wire was too small.
  • the welding test body according to 70 uses the wire according to wire number 64 in Table 5. No. The weld specimen according to No. 70 was inferior in hot cracking resistance because the total amount of C and N contained in the wire (C + N amount) was too much.
  • the welding test body according to 71 uses a wire according to wire number 65 in Table 5. No. The weld specimen according to No. 71 had inferior creep performance because the wire contained too little C + N.
  • wires and fluxes with varying amounts of impurities were prepared.
  • the wire numbers 1-2 and 1-3 shown in Table 9 and the flux numbers 3-2 and 3-3 shown in Table 10 are component systems in which impurities are intentionally increased.
  • the wire number 1-1 shown in Table 9 indicates the impurity component of wire number 1
  • the flux number 3-1 shown in Table 10 indicates the impurity component of flux number 1.
  • X shown in Table 9 and Y shown in Table 6 are values calculated by the following relational expressions (5) and (6), respectively.
  • the Pb amount (ppm) and Bi amount (ppm) of the wire component are [Pb] W and [Bi] W , respectively, and the Pb amount (ppm) and Bi amount (ppm) of the flux component ), respectively [Pb] F, were met when the [Bi] F, the following relational expression (4).
  • the P amount (ppm), the Sn amount (ppm), the As amount (ppm), and the Sb amount (ppm) of the wire components are [P] W , [Sn] W , and [As], respectively.
  • W , [Sb] Let W be the P content (ppm), Sn content (ppm), As content (ppm), and Sb content (ppm) of the flux component [P] F , [Sn] F , [As], respectively.
  • F 1 and [Sb] F are satisfied, the following relational expressions (5) to (7) were satisfied. Therefore, no.
  • the weld specimen according to No. 73 was excellent in toughness.
  • the submerged arc welding wire of the present invention is useful for welding a thermal power generation boiler, a turbine, a chemical reaction vessel (reactor) for desulfurization and reforming (heavy oil decomposition), and the like.

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  • Engineering & Computer Science (AREA)
  • Mechanical Engineering (AREA)
  • Nonmetallic Welding Materials (AREA)

Abstract

L'invention concerne un fil pour soudage à l'arc submergé utilisé en combinaison avec du flux, où le fil contient, comme composants, une quantité spécifique de chacun des éléments suivants : C, Si, Mn, Cr, Mo, V, Nb et N et au plus une quantité spécifique de chacun des éléments suivants : Ni, P, S, Cu, Al, B, et O, la quantité massique totale de Mn et de Ni est de 0,5 à 1,75 %, le rapport entre Mn et S (Mn/S) est d'au moins 87, et le reste est du Fe et d'inévitables impuretés.
PCT/JP2016/075800 2015-09-04 2016-09-02 Fil pour soudage à l'arc submergé WO2017038975A1 (fr)

Priority Applications (4)

Application Number Priority Date Filing Date Title
CN201680050748.XA CN107949455B (zh) 2015-09-04 2016-09-02 埋弧焊用焊丝
KR1020187006052A KR102088179B1 (ko) 2015-09-04 2016-09-02 서브머지드 아크 용접용 와이어
EP16842004.0A EP3345716B1 (fr) 2015-09-04 2016-09-02 Fil pour soudage à l'arc submergé
ES16842004T ES2833354T3 (es) 2015-09-04 2016-09-02 Alambre para soldadura por arco sumergido

Applications Claiming Priority (4)

Application Number Priority Date Filing Date Title
JP2015-175218 2015-09-04
JP2015175218 2015-09-04
JP2016-091902 2016-04-28
JP2016091902A JP6760758B2 (ja) 2015-09-04 2016-04-28 サブマージアーク溶接用ワイヤ

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WO2017038975A1 true WO2017038975A1 (fr) 2017-03-09

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Cited By (1)

* Cited by examiner, † Cited by third party
Publication number Priority date Publication date Assignee Title
CN112548397A (zh) * 2020-12-07 2021-03-26 四川西冶新材料股份有限公司 一种汽化炉耐热钢氩弧焊丝及其制备方法

Citations (5)

* Cited by examiner, † Cited by third party
Publication number Priority date Publication date Assignee Title
JPS60174295A (ja) * 1984-02-20 1985-09-07 Sumitomo Metal Ind Ltd サブマ−ジア−ク溶接ワイヤおよび溶接方法
JPH04253595A (ja) * 1991-02-04 1992-09-09 Nippon Steel Corp Ｃｒ−Ｍｏ系低合金鋼のサブマージアーク溶接方法
JPH11291086A (ja) * 1998-04-15 1999-10-26 Nippon Steel Corp 高Ｃｒフェライト系耐熱鋼用潜弧溶接方法
JP2005329415A (ja) * 2004-05-18 2005-12-02 Kobe Steel Ltd 改良９Ｃｒ−１Ｍｏ鋼用溶接ワイヤ
WO2014119197A1 (fr) * 2013-02-04 2014-08-07 株式会社神戸製鋼所 FIL DE SOUDURE À L'ARC SUBMERGÉ POUR ACIER HAUTE RÉSISTANCE 2,25Cr-1Mo-V ET MÉTAL DE SOUDAGE

Patent Citations (5)

* Cited by examiner, † Cited by third party
Publication number Priority date Publication date Assignee Title
JPS60174295A (ja) * 1984-02-20 1985-09-07 Sumitomo Metal Ind Ltd サブマ−ジア−ク溶接ワイヤおよび溶接方法
JPH04253595A (ja) * 1991-02-04 1992-09-09 Nippon Steel Corp Ｃｒ−Ｍｏ系低合金鋼のサブマージアーク溶接方法
JPH11291086A (ja) * 1998-04-15 1999-10-26 Nippon Steel Corp 高Ｃｒフェライト系耐熱鋼用潜弧溶接方法
JP2005329415A (ja) * 2004-05-18 2005-12-02 Kobe Steel Ltd 改良９Ｃｒ−１Ｍｏ鋼用溶接ワイヤ
WO2014119197A1 (fr) * 2013-02-04 2014-08-07 株式会社神戸製鋼所 FIL DE SOUDURE À L'ARC SUBMERGÉ POUR ACIER HAUTE RÉSISTANCE 2,25Cr-1Mo-V ET MÉTAL DE SOUDAGE

Cited By (2)

* Cited by examiner, † Cited by third party
Publication number Priority date Publication date Assignee Title
CN112548397A (zh) * 2020-12-07 2021-03-26 四川西冶新材料股份有限公司 一种汽化炉耐热钢氩弧焊丝及其制备方法
CN112548397B (zh) * 2020-12-07 2021-12-07 四川西冶新材料股份有限公司 一种汽化炉耐热钢氩弧焊丝及其制备方法

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