JP6257489B2 - Gas shield arc welding method - Google Patents

Gas shield arc welding method Download PDF

Info

Publication number
JP6257489B2
JP6257489B2 JP2014197531A JP2014197531A JP6257489B2 JP 6257489 B2 JP6257489 B2 JP 6257489B2 JP 2014197531 A JP2014197531 A JP 2014197531A JP 2014197531 A JP2014197531 A JP 2014197531A JP 6257489 B2 JP6257489 B2 JP 6257489B2
Authority
JP
Japan
Prior art keywords
mass
wire
flux
welding
lower plate
Prior art date
Legal status (The legal status 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 status listed.)
Active
Application number
JP2014197531A
Other languages
Japanese (ja)
Other versions
JP2016068097A (en
Inventor
亮 陳
亮 陳
石▲崎▼　圭人
圭人 石▲崎▼
尚英 古川
尚英 古川
Current Assignee (The listed assignees may be inaccurate. Google has not performed a legal analysis and makes no representation or warranty as to the accuracy of the list.)
Kobe Steel Ltd
Original Assignee
Kobe Steel Ltd
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
Application filed by Kobe Steel Ltd filed Critical Kobe Steel Ltd
Priority to JP2014197531A priority Critical patent/JP6257489B2/en
Priority to CN201510583561.3A priority patent/CN105458465B/en
Publication of JP2016068097A publication Critical patent/JP2016068097A/en
Application granted granted Critical
Publication of JP6257489B2 publication Critical patent/JP6257489B2/en
Active legal-status Critical Current
Anticipated expiration legal-status Critical

Links

Classifications

    • 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
    • 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
    • B23K35/3053—Fe as the principal constituent
    • B23K35/3073—Fe as the principal constituent with Mn as next major constituent

Landscapes

  • Engineering & Computer Science (AREA)
  • Mechanical Engineering (AREA)
  • Physics & Mathematics (AREA)
  • Plasma & Fusion (AREA)
  • Nonmetallic Welding Materials (AREA)
  • Butt Welding And Welding Of Specific Article (AREA)

Description

本発明は、片側すみ肉ガスシールドアーク溶接方法に関する。より詳しくは、水平方向に対して下板を傾けて下板と立板とのすみ肉部を溶接するガスシールドアーク溶接方法に関する。   The present invention relates to a one-side fillet gas shielded arc welding method. More specifically, the present invention relates to a gas shielded arc welding method in which a fillet portion between a lower plate and a standing plate is welded by tilting the lower plate with respect to the horizontal direction.

橋梁鋼床板は、強度補強のために、鋼板にＵリブや縦リブを溶接で取付けた構造を採用することが多い。その際の溶接方法としては、主に、ガスシールドアーク溶接方法が用いられている。一方、橋梁鋼床板は、路面を走行する車両の振動荷重を受けるため、構造物全体で高い疲労強度が要求されており、特に溶接部の品質が重要となる。一般的に、溶接継手の強度を確保するためには、溶込みをリブ材の８割以上とすることが望ましいが、溶接時の高温割れを防ぐためには、完全溶込みになってはならない。   Bridge steel floor boards often employ a structure in which U-ribs or vertical ribs are attached to steel sheets by welding for strength reinforcement. As a welding method at that time, a gas shield arc welding method is mainly used. On the other hand, since the bridge steel floor board receives the vibration load of the vehicle which drive | works a road surface, the high fatigue strength is requested | required by the whole structure, and especially the quality of a welding part becomes important. In general, in order to ensure the strength of the welded joint, it is desirable that the penetration be 80% or more of the rib material, but in order to prevent hot cracking during welding, the penetration must not be complete.

また、橋梁鋼床板などの溶接構造物には、応力集中を軽減すると共に、疲労強度を確保するため、溶接ビードにも、アンダーカットフリーや止端部の滑らかさなどが要求され、更に、溶接金属部にも十分な強度と衝撃性能が要求される。溶接構造物において、このような高品質な溶接を実現するためには、溶接条件及びその溶接材料がポイントとなる。   In addition, welded structures such as bridge steel floor plates are required to have undercut-free and smooth toe to weld bead to reduce stress concentration and secure fatigue strength. Metal parts are also required to have sufficient strength and impact performance. In order to realize such high-quality welding in a welded structure, the welding conditions and the welding material are the key.

そこで、下板及び立板からなる水平すみ肉部材の立板が傾斜したすみ肉角度が９０°超の水平すみ肉部の溶接において、アークが安定で、スパッタ発生量が少なく、更に深い溶込みを得るため、ワイヤ組成などを特定した片側水平すみ肉ガスシールドアーク溶接方法が提案されている（特許文献１参照）。特許文献１に記載の溶接方法では、ワイヤ全質量％で、Ｓｉ：０．３〜１．８％、Ｍｎ：０．８〜４．０％、アーク安定剤：０．０５〜１．８％を含み、フラックス充填率が３〜１０％であるフラックス入りワイヤを用いている。この溶接方法では、例えばワイヤが１．４ｍｍの場合は、溶接電流を３２０〜５２０Ａの範囲にしている。   Therefore, in welding of a horizontal fillet where the fillet angle of the horizontal fillet member consisting of the lower plate and the standing plate is inclined and the fillet angle is more than 90 °, the arc is stable, less spatter is generated, and deeper penetration. Therefore, a one-side horizontal fillet gas shielded arc welding method in which the wire composition is specified has been proposed (see Patent Document 1). In the welding method described in Patent Document 1, the total mass% of the wire is Si: 0.3 to 1.8%, Mn: 0.8 to 4.0%, and arc stabilizer: 0.05 to 1.8%. And a flux-cored wire having a flux filling rate of 3 to 10% is used. In this welding method, for example, when the wire is 1.4 mm, the welding current is set in the range of 320 to 520A.

また、従来、Ｕリブ溶接においてＵリブ材の８割以上の溶込みと良好なビード形状を確保するために、スパッタが少なく、ワイヤ送給性がよく、スラグ発生量の少ないフラックス入りワイヤを用いて、溶接電流を２８０〜３４０Ａ、アーク電圧を３２〜３６Ｖ、溶接速度を２２〜２８ｍ／時間、溶接姿勢を下向とする溶接方法も提案されている（特許文献２参照）。   Conventionally, in U-rib welding, in order to ensure more than 80% penetration of U-rib material and a good bead shape, a flux-cored wire with less spatter, good wire feedability, and low slag generation is used. A welding method is also proposed in which the welding current is 280 to 340 A, the arc voltage is 32 to 36 V, the welding speed is 22 to 28 m / hour, and the welding posture is downward (see Patent Document 2).

特開２００３−８０３９６号公報JP 2003-80396 A 中国特許出願公開第１０２８６１９７０号明細書Chinese Patent Application No. 102861970

しかしながら、前述した特許文献１，２に記載の溶接方法では、橋梁鋼床板などの溶接構造物のリブ取付けなどの溶接において、溶け込みがリブ材の８割以上であるが完全溶込みにはならず、かつアンダーカットフリーで滑らかな溶接ビードを得ることは難しい。具体的には、特許文献１に記載の溶接方法は、フラックス充填率が３〜１０％のフラックス入りワイヤを用いているため、スラグ発生量が少なく、凸ビードになりやすく、溶接ビードと下板のなじみが不十分となる。   However, in the welding methods described in Patent Documents 1 and 2 described above, in welding such as rib attachment of a welded structure such as a bridge steel floor plate, the penetration is 80% or more of the rib material, but it is not complete penetration. In addition, it is difficult to obtain a smooth weld bead with undercut free. Specifically, since the welding method described in Patent Document 1 uses a flux-cored wire with a flux filling rate of 3 to 10%, the amount of slag generation is small, and a convex bead tends to be formed. The familiarity becomes insufficient.

また、特許文献２に記載の溶接方法は、使用するワイヤに関して成分組成やフラックスの割合などが特定されておらず、また、溶接条件も溶接電流、電圧及び溶接速度しか特定されていないため、要求されている溶接品質を満たす溶接構造物は得られない。   In addition, the welding method described in Patent Document 2 does not specify the component composition, the flux ratio, or the like for the wire used, and the welding conditions include only the welding current, voltage, and welding speed. It is not possible to obtain a welded structure that satisfies the weld quality.

そこで、本発明は、適度な溶け込みを有し、溶接ビードが良好なすみ肉溶接継手が得られるガスシールドアーク溶接方法を提供することを主目的とする。   Accordingly, the main object of the present invention is to provide a gas shielded arc welding method capable of obtaining a fillet welded joint having an appropriate penetration and a good weld bead.

本発明に係るガスシールドアーク溶接方法は、下板と立板とを片側すみ肉ガスシールドアーク溶接する方法であり、水平方向に対して前記下板を傾けて、電極ワイヤの直径Ｄを１．２〜１．６ｍｍ、前記下板と前記立板とがなす角度θを９０〜１３０°、溶接トーチの溶接方向における傾斜角度αを−１０〜２０°、前記下板の水平方向に対する傾斜角度βを１０〜５０°、前記溶接トーチと前記下板とがなす角度γを下記数式（Ａ）で示す範囲にして、前記下板と前記立板とのすみ肉部を溶接する。   A gas shielded arc welding method according to the present invention is a method in which a lower plate and a standing plate are subjected to one-side fillet gas shielded arc welding, and the lower plate is inclined with respect to the horizontal direction so that the diameter D of the electrode wire is 1. 2 to 1.6 mm, an angle θ between the lower plate and the upright plate is 90 to 130 °, an inclination angle α in the welding direction of the welding torch is −10 to 20 °, and an inclination angle β with respect to the horizontal direction of the lower plate 10 to 50 °, and the angle γ formed by the welding torch and the lower plate is set in the range indicated by the following mathematical formula (A), and the fillet portions of the lower plate and the standing plate are welded.

[数１]
（θ／２）−２０°≦γ≦９０°−β ・・・ （Ａ） [Equation 1]
(Θ / 2) −20 ° ≦ γ ≦ 90 ° −β (A)

このガスシールドアーク溶接方法では、例えば、溶接速度を２００〜７００ｍｍ／分、溶接電流を２００〜４５０Ａ、アーク電圧を２０〜４５Ｖ、チップ母材間距離を１５〜３５ｍｍにすることができる。
一方、前記電極ワイヤには、鋼製外皮にフラックスが充填され、前記フラックスの充填率が１０〜２０質量％であり、かつ、ワイヤ全質量あたり、ワイヤ全質量あたり、Ｃ：０．０１〜０．１０質量％、Ｓｉ：０．５〜１．５質量％、Ｍｎ：１．５〜３．５質量％、Ｍｇ及びＡｌのうち少なくとも１種：合計で０．１〜２．０質量％、ＴｉＯ２：１．５〜６．０質量％、Ｎａ化合物、Ｋ化合物及びＬｉ化合物のうち少なくとも１種の化合物：合計で０．０５〜０．４質量％、Ａｌ２Ｏ３、ＺｒＯ２及びＳｉＯ２のうち少なくとも１種の酸化物：ＴｉＯ２との合計で２〜８質量％、Ｆｅ：８６質量％以上を含有し、Ｍｎ含有量（質量％）とＳｉ含有量（質量％）との比（Ｍｎ／Ｓｉ）が１．５〜５．５である組成を有するフラックス入りワイヤを用いることができる。
その場合、前記フラックス入りワイヤは、更に、Ｎｉ及びＭｏのうち少なくとも１種の元素を、ワイヤ全質量あたり、合計で０．１〜３．０質量％含有していてもよい。
また、前記フラックス入りワイヤとしては、破断強度が３００〜９００ＭＰａのものを使用することができる。 In this gas shield arc welding method, for example, the welding speed can be 200 to 700 mm / min, the welding current can be 200 to 450 A, the arc voltage can be 20 to 45 V, and the distance between the tip base materials can be 15 to 35 mm.
On the other hand, the electrode wire is filled with a flux in a steel outer sheath, the flux filling rate is 10 to 20% by mass, and C: 0.01 to 0 per total wire mass per total wire mass. 10 mass%, Si: 0.5-1.5 mass%, Mn: 1.5-3.5 mass%, at least one of Mg and Al: 0.1-2.0 mass% in total, TiO 2 : 1.5 to 6.0% by mass, at least one compound among Na compound, K compound and Li compound: 0.05 to 0.4% by mass in total, Al 2 O 3 , ZrO 2 and SiO 2 to 8% by mass in total of at least one oxide of TiO 2 : 2 and Fe: 86% by mass or more, ratio of Mn content (% by mass) and Si content (% by mass) Containing flux having a composition in which (Mn / Si) is 1.5 to 5.5 It is possible to use the ear.
In that case, the flux-cored wire may further contain at least one element of Ni and Mo in a total amount of 0.1 to 3.0% by mass based on the total mass of the wire.
Further, as the flux-cored wire, one having a breaking strength of 300 to 900 MPa can be used.

本発明によれば、水平方向に対して下板を傾けて、特定条件ですみ肉溶接しているため、適度な溶け込みを有し、溶接ビードが良好なすみ肉溶接継手が得られる。   According to the present invention, since the fillet welding is performed under specific conditions by tilting the lower plate with respect to the horizontal direction, a fillet welded joint having an appropriate penetration and a good weld bead can be obtained.

本発明の実施形態のガスシールドアーク溶接方法を示す模式図である。It is a schematic diagram which shows the gas shield arc welding method of embodiment of this invention. Ａ及びＢは図１に示すガスシールドアーク溶接方法における電極ワイヤの傾斜角度αを示す模式図であり、Ａはαがプラスの場合、Ｂはαがマイナスの場合を示す。A and B are schematic views showing the inclination angle α of the electrode wire in the gas shielded arc welding method shown in FIG. 1, wherein A shows a case where α is positive and B shows a case where α is negative. Ａ〜Ｃは溶け込み及びビード形状の判断基準例を示す顕微鏡写真であり、Ａ及びＣは不良の例を示し、Ｂは良好の例を示す。A to C are photomicrographs showing examples of criteria for determining penetration and bead shape, A and C show examples of defects, and B shows a good example.

以下、本発明を実施するための形態について、詳細に説明する。なお、本発明は、以下に説明する実施形態に限定されるものではない。図１は本発明の実施形態のガスシールドアーク溶接方法を示す模式図である。また、図２Ａ，Ｂは図１に示すガスシールドアーク溶接方法における電極ワイヤの傾斜角度αを示す模式図であり、図２Ａはαがプラスの場合、図２Ｂはαがマイナスの場合を示す。   Hereinafter, embodiments for carrying out the present invention will be described in detail. Note that the present invention is not limited to the embodiments described below. FIG. 1 is a schematic view showing a gas shielded arc welding method according to an embodiment of the present invention. 2A and 2B are schematic views showing the inclination angle α of the electrode wire in the gas shielded arc welding method shown in FIG. 1, FIG. 2A shows a case where α is positive, and FIG. 2B shows a case where α is negative.

図１に示すように、本実施形態のガスシールドアーク溶接方法は、水平方向に対して下板１を傾け、下板１と立板２とのすみ肉部を片側すみ肉ガスシールドアーク溶接する。ここで、下板１及び立板２はいずれも鋼製部材であり、立板２は図１に示すＵリブに限定されず縦リブなどの他の形態でもよい。   As shown in FIG. 1, in the gas shield arc welding method of the present embodiment, the lower plate 1 is inclined with respect to the horizontal direction, and the fillet portion between the lower plate 1 and the upright plate 2 is subjected to one-side fillet gas shield arc welding. . Here, both the lower plate 1 and the upright plate 2 are steel members, and the upright plate 2 is not limited to the U-rib shown in FIG.

本実施形態のガスシールドアーク溶接方法では、電極ワイヤ４には直径（ワイヤ径）Ｄが１．２〜１．６ｍｍのものを使用し、下板１と立板２とがなす角度θは９０〜１３０°、電極ワイヤ４の溶接方向における傾斜角度αは−１０〜２０°、下板１の水平方向に対する傾斜角度βは１０〜５０°、電極ワイヤ４と下板１とがなす角度γは下記数式（Ａ）で示す範囲にする。   In the gas shielded arc welding method of the present embodiment, the electrode wire 4 having a diameter (wire diameter) D of 1.2 to 1.6 mm is used, and the angle θ formed by the lower plate 1 and the standing plate 2 is 90. ~ 130 °, the inclination angle α in the welding direction of the electrode wire 4 is -10 to 20 °, the inclination angle β with respect to the horizontal direction of the lower plate 1 is 10 to 50 °, and the angle γ between the electrode wire 4 and the lower plate 1 is The range is represented by the following formula (A).

[数２]
（θ／２）−２０°≦γ≦９０°−β ・・・ （Ａ） [Equation 2]
(Θ / 2) −20 ° ≦ γ ≦ 90 ° −β (A)

溶接条件は、溶接速度を２００〜７００ｍｍ／分、溶接電流を２００〜４５０Ａ、アーク電圧を２０〜４５Ｖ、チップ母材間距離Ｌを１５〜３５ｍｍとすることが好ましい。また、溶接ワイヤ４には、フラックスの充填率、成分組成及び破断強度が特定の範囲にあるフラックス入りワイヤを使用することが好ましい。   The welding conditions are preferably a welding speed of 200 to 700 mm / min, a welding current of 200 to 450 A, an arc voltage of 20 to 45 V, and a tip base metal distance L of 15 to 35 mm. Moreover, it is preferable to use the flux-cored wire in which the filling rate of a flux, a component composition, and breaking strength are in a specific range for the welding wire 4.

次に、本実施形態のガスシールドアーク溶接方法における各種条件設定の理由について説明する。   Next, the reason for setting various conditions in the gas shielded arc welding method of the present embodiment will be described.

［電極ワイヤ４の直径Ｄ：１．２〜１．６ｍｍ］
溶接に用いる電極ワイヤ４の直径Ｄが細過ぎると、具体的にワイヤ径Ｄが１．２ｍｍ未満の場合、アークが広がりにくく、溶接ビードが疲労強度に不利な凸の形状にやりやすい。一方、電極ワイヤ４の直径Ｄが太過ぎると、具体的にはワイヤ径Ｄが１．６を超えると、ワイヤの送給性が低下する。よって、本実施形態のガスシールドアーク溶接方法では、直径Ｄが１．２〜１．６ｍｍの電極ワイヤを使用する。 [Diameter D of electrode wire 4: 1.2 to 1.6 mm]
If the diameter D of the electrode wire 4 used for welding is too thin, when the wire diameter D is specifically less than 1.2 mm, the arc is difficult to spread, and the weld bead tends to have a convex shape that is disadvantageous in fatigue strength. On the other hand, if the diameter D of the electrode wire 4 is too large, specifically, if the wire diameter D exceeds 1.6, the wire feedability decreases. Therefore, in the gas shielded arc welding method of this embodiment, an electrode wire having a diameter D of 1.2 to 1.6 mm is used.

［下板１と立板２とがなす角度θ：９０〜１３０°］
下板１と立板２とがなす角度θは、安全性の観点から、種々の強度計算により算出された値であり、現在一般に採用されている規準などに基づいている。本発明は、橋梁鋼床板などの溶接構造物への適用を前提としているため、従来の設計規準に従い、下板１と立板２とがなす角度θは９０〜１３０°とした。 [An angle θ between the lower plate 1 and the standing plate 2: 90 to 130 °]
The angle θ formed by the lower plate 1 and the upright plate 2 is a value calculated by various strength calculations from the viewpoint of safety, and is based on a standard that is generally adopted at present. Since the present invention is premised on application to a welded structure such as a bridge steel floor plate, the angle θ between the lower plate 1 and the upright plate 2 is set to 90 to 130 ° according to the conventional design standard.

なお、本発明は、下板１と立板２とがなす角度θが９０〜１３０°を前提としているため、角度θを９０°未満にして溶接した場合、その他の条件を満たしても、良好なビード形状や溶け込み形状は得られない。また、角度θを１３０°超にして溶接した場合も、十分な脚長が得られず、良好なビード形状は得られない。   In the present invention, since the angle θ formed by the lower plate 1 and the upright plate 2 is premised on 90 to 130 °, when the angle θ is less than 90 ° and welding is performed, it is satisfactory even if other conditions are satisfied. Neither bead shape nor penetration shape can be obtained. Also, when welding is performed with the angle θ exceeding 130 °, a sufficient leg length cannot be obtained, and a good bead shape cannot be obtained.

［トーチ３の溶接方向における傾斜角度α：−１０〜２０°］
一般的に、図２Ａに示すように、溶接方向におけるトーチ３の傾斜角度αがプラスであれば前進角、図２Ｂに示すように傾斜角度αがマイナスであれば後退角という。そして、前進角が大きくなるに従い、ビード幅は広くなるが、溶け込みは浅くなる。一方、後退角が大きくなると、溶け込みは深くなるが、ビード幅が狭くなり、母材とのなじみが劣化する。 [Inclination angle α in the welding direction of the torch 3: −10 to 20 °]
In general, as shown in FIG. 2A, if the inclination angle α of the torch 3 in the welding direction is positive, it is called a forward angle, and if the inclination angle α is negative as shown in FIG. And as the advance angle increases, the bead width increases, but the penetration becomes shallower. On the other hand, when the receding angle is increased, the penetration becomes deeper, but the bead width is reduced and the compatibility with the base material is deteriorated.

具体的には、トーチ３の溶接方向における傾斜角度αが−１０°よりも小さくなると、即ち、後退角が１０°よりも大きくなると、母材とのなじみが劣化し、良好な溶接ビードが得られなくなる。また、トーチ３の溶接方向における傾斜角度αが２０°を超えると、即ち、前進角が２０°よりも大きくなると、溶込みを立板（リブ材）の８割以上にすることができなくなる。よって、本実施形態のガスシールドアーク溶接方法では、トーチ３の溶接方向における傾斜角度αを−１０〜２０°とする。   Specifically, when the inclination angle α in the welding direction of the torch 3 is smaller than −10 °, that is, when the receding angle is larger than 10 °, the familiarity with the base material is deteriorated and a good weld bead is obtained. It becomes impossible. Further, when the inclination angle α in the welding direction of the torch 3 exceeds 20 °, that is, when the advance angle becomes larger than 20 °, the penetration cannot be made 80% or more of the standing plate (rib material). Therefore, in the gas shielded arc welding method of the present embodiment, the inclination angle α in the welding direction of the torch 3 is set to −10 to 20 °.

［下板１の水平方向に対する傾斜角度β：１０〜５０°］
溶接ビード形状を良好にするために、水平方向に対して下板１を傾斜させて溶接することがある。本発明は、下板１を傾斜させて溶接することを前提にしており、下板１の水平方向に対する傾斜角度βが１０°未満の場合、その他の条件を満たしたとしても、本発明の効果が得られず、良好な溶接ビードが得られない。一方、下板１は、傾斜が大きくなるに従い溶け込みが深くなる傾向があり、その傾斜角度βを５０°よりも大きくすると、溶接金属が立板（リブ材）を貫通する虞がある。よって、本実施形態のガスシールドアーク溶接方法では、下板１の水平方向に対する傾斜角度βを１０〜５０°とする。 [Inclination angle β of the lower plate 1 with respect to the horizontal direction: 10 to 50 °]
In order to improve the weld bead shape, the lower plate 1 may be inclined and welded with respect to the horizontal direction. The present invention is based on the premise that the lower plate 1 is inclined and welded, and when the inclination angle β with respect to the horizontal direction of the lower plate 1 is less than 10 °, even if other conditions are satisfied, the effects of the present invention are achieved. Cannot be obtained, and a good weld bead cannot be obtained. On the other hand, the lower plate 1 tends to deepen as the inclination increases, and if the inclination angle β is larger than 50 °, the weld metal may penetrate the standing plate (rib material). Therefore, in the gas shield arc welding method of the present embodiment, the inclination angle β of the lower plate 1 with respect to the horizontal direction is set to 10 to 50 °.

［トーチ３と下板１とがなす角度γ：（θ／２）−２０°≦γ≦９０°−β］
ビード形状と溶け込みを両立するためには、トーチ３と下板１とがなす角度γと、下板１と立板２とがなす角度θと、下板１の水平方向に対する傾斜角度βとの関係が重要となる。具体的には、トーチ３と下板１とがなす角度γが、（θ／２）−２０°よりも小さいと、溶接金属が下板１に寄り過ぎて、ビード形状が劣化する。一方、トーチ３と下板１とがなす角度γが、９０°−βよりも大きくなると、溶け込みが浅くなり、溶込みを立板（リブ材）の８割以上にすることが難しくなる。よって、本実施形態のガスシールドアーク溶接方法では、トーチ３と下板１とがなす角度γは、上記数式（Ａ）に示す範囲、即ち、｛（θ／２）−２０°｝以上かつ（９０°−β）以下とする。 [An angle γ between the torch 3 and the lower plate 1: (θ / 2) −20 ° ≦ γ ≦ 90 ° −β)
In order to achieve both bead shape and penetration, an angle γ formed by the torch 3 and the lower plate 1, an angle θ formed by the lower plate 1 and the standing plate 2, and an inclination angle β of the lower plate 1 with respect to the horizontal direction Relationships are important. Specifically, if the angle γ formed by the torch 3 and the lower plate 1 is smaller than (θ / 2) −20 °, the weld metal is too close to the lower plate 1 and the bead shape is deteriorated. On the other hand, when the angle γ formed by the torch 3 and the lower plate 1 is larger than 90 ° −β, the penetration becomes shallow, and it becomes difficult to make the penetration 80% or more of the standing plate (rib material). Therefore, in the gas shielded arc welding method of the present embodiment, the angle γ formed by the torch 3 and the lower plate 1 is in the range shown in the above formula (A), that is, {(θ / 2) −20 °} or more and ( 90 ° −β) or less.

［溶接速度：２００〜７００ｍｍ／分］
溶接速度が２００ｍｍ／分未満の場合、入熱が高すぎて、溶接金属が立板（リブ材）を貫通する虞があり、更に、溶接金属が多くなって、垂れビードになりやすい。一方、溶接速度が７００ｍｍ／分を超えると、溶け込みを立板（リブ材）の板厚の８割以上にすることができないことがある。このため、溶接速度は、２００〜７００ｍｍ／分とすることが好ましい。 [Welding speed: 200 to 700 mm / min]
When the welding speed is less than 200 mm / min, the heat input is too high, and there is a possibility that the weld metal penetrates the standing plate (rib material). On the other hand, if the welding speed exceeds 700 mm / min, the penetration may not be 80% or more of the plate thickness of the standing plate (rib material). For this reason, it is preferable that a welding speed shall be 200-700 mm / min.

［溶接電流：２００〜４５０Ａ］
適正な溶接電流の範囲は、電極ワイヤ４の直径Ｄによって異なるが、例えば直径Ｄが１．２ｍｍのワイヤを使用する場合、溶接電流を２００Ａ未満にすると、溶け込みが立板（リブ材）の板厚の８割以上になりにくい。また、直径Ｄが１．６ｍｍのワイヤを使用する場合、溶接電流が４５０Ａを超えると、溶接金属が立板（リブ材）を貫通する虞がある。このため、電極ワイヤ４の直径Ｄが１．２〜１．６ｍｍの範囲においては、溶接電流は２００〜４５０Ａの範囲にすることが好ましい。 [Welding current: 200 to 450 A]
The range of the appropriate welding current varies depending on the diameter D of the electrode wire 4. For example, when a wire having a diameter D of 1.2 mm is used, if the welding current is less than 200 A, the penetration is a vertical plate (rib material). It is hard to become more than 80% of thickness. Further, when a wire having a diameter D of 1.6 mm is used, if the welding current exceeds 450 A, the weld metal may penetrate the standing plate (rib material). For this reason, when the diameter D of the electrode wire 4 is in the range of 1.2 to 1.6 mm, the welding current is preferably in the range of 200 to 450A.

［アーク電圧：２０〜４５Ｖ］
アーク電圧が２０Ｖ未満の場合、アークの広がりが小さくなり、ビード形状が凸になりやすく、更に、電極ワイヤ４が母材（下板１、立板２）に突っ込み、安定な溶接ビードが得られにくい。一方、アーク電圧が４５Ｖを超えると、アーク長が長くなって、溶け込みが浅くなる傾向があり、更に、大気が溶接金属に巻き込まれて、ガス欠陥が発生しやすい。このため、アーク電圧は２０〜４５Ｖの範囲にすることが好ましい。 [Arc voltage: 20-45V]
When the arc voltage is less than 20V, the spread of the arc becomes small, the bead shape tends to be convex, and the electrode wire 4 thrusts into the base material (the lower plate 1 and the upright plate 2), and a stable weld bead is obtained. Hateful. On the other hand, when the arc voltage exceeds 45 V, the arc length becomes long and the penetration tends to be shallow, and further, the atmosphere is caught in the weld metal, and gas defects are likely to occur. For this reason, it is preferable that the arc voltage is in the range of 20 to 45V.

［チップ母材間距離Ｌ：１５〜３５ｍｍ］
チップ母材間距離Ｌが１５ｍｍよりも短いと、シールドガス排出用のノズルと母材（下板１、立板２）とが干渉しないようにトーチ３を配置することが難しくなり、更に、溶接中に発生したスパッタがノズル先端に付着して、シールドガスの流れが低下しやすくなる。一方、チップ母材間距離Ｌが３５ｍｍよりも長いと、溶接中のトーチ振動などによって、安定なビード形状が得られにくくなり、更に、大気が溶接金属に巻き込まれて、ガス欠陥が発生しやすくなる。このため、チップ母材間距離Ｌは１５〜３５ｍｍとすることが好ましい。 [Distance between base materials L: 15 to 35 mm]
If the distance L between the tip base materials is shorter than 15 mm, it becomes difficult to dispose the torch 3 so that the shield gas discharge nozzle and the base materials (lower plate 1 and upright plate 2) do not interfere with each other. Spatter generated inside adheres to the tip of the nozzle, and the flow of shield gas tends to decrease. On the other hand, if the distance L between the tip base materials is longer than 35 mm, it becomes difficult to obtain a stable bead shape due to torch vibration during welding, and further, the atmosphere is caught in the weld metal and gas defects are likely to occur. Become. For this reason, it is preferable that the distance L between chip | tip base materials shall be 15-35 mm.

［電極ワイヤ４の種類：フラックス入りワイヤ］
本実施形態のガスシールドアーク溶接方法に用いる電極ワイヤ４は、消耗電極として用いられる溶接材料であればその種類は特に限定されるものではないが、鋼製外皮にフラックスが充填されたフラックス入りワイヤを用いることが好ましい。特に、フラックスの充填率が１０〜２０質量％であり、ワイヤ全質量あたり、Ｃ：０．０１〜０．１０質量％、Ｓｉ：０．５〜１．５質量％、Ｍｎ：１．５〜３．５質量％、Ｍｇ及びＡｌのうち少なくとも１種：合計で０．１〜２．０質量％、ＴｉＯ２：１．５〜６．０質量％、Ｎａ化合物、Ｋ化合物、及びＬｉ化合物のうち少なくとも１種の化合物：合計で０．０５〜０．４質量％、Ａｌ２Ｏ３、ＺｒＯ２及びＳｉＯ２のうち少なくとも１種の酸化物：ＴｉＯ２との合計で２〜８質量％、Ｆｅ：８６質量％以上を含有し、Ｍｎ含有量（質量％）とＳｉ含有量（質量％）との比（Ｍｎ／Ｓｉ）が１．５〜５．５である組成を有するフラックス入りワイヤが好ましい。 [Type of electrode wire 4: flux-cored wire]
The electrode wire 4 used in the gas shielded arc welding method of the present embodiment is not particularly limited as long as it is a welding material used as a consumable electrode, but a flux-cored wire in which a steel outer shell is filled with a flux. Is preferably used. In particular, the flux filling rate is 10 to 20% by mass, and C: 0.01 to 0.10% by mass, Si: 0.5 to 1.5% by mass, Mn: 1.5 to 1.5% by mass based on the total mass of the wire. 3.5 wt%, Mg and at least one of Al: 0.1 to 2.0 mass% in total, TiO 2: of 1.5-6.0 mass%, Na compounds, K compound, and Li compounds Among them, at least one compound: 0.05 to 0.4 mass% in total, at least one oxide of Al 2 O 3 , ZrO 2 and SiO 2 : 2 to 8 mass% in total with TiO 2 , A flux-cored wire containing Fe: 86% by mass or more and having a composition in which the ratio of Mn content (% by mass) to Si content (% by mass) (Mn / Si) is 1.5 to 5.5. preferable.

＜フラックス充填率：１０〜２０質量％＞
フラックス充填率が１０質量％未満の場合、溶接ビードを覆うスラグの量が少なくなり、良好なビード形状が得られないことがある。一方、フラックス充填率が２０質量％を超えると、溶着金属中の酸素量が高くなり、衝撃性能が劣化することがある。このため、フラックス入りワイヤのフラックス充填率は、１０〜２０質量％であることが好ましい。 <Flux filling ratio: 10 to 20% by mass>
When the flux filling rate is less than 10% by mass, the amount of slag covering the weld bead decreases, and a good bead shape may not be obtained. On the other hand, when the flux filling rate exceeds 20% by mass, the amount of oxygen in the weld metal increases, and the impact performance may be deteriorated. For this reason, it is preferable that the flux filling rate of a flux cored wire is 10-20 mass%.

＜Ｃ：０．０１〜０．１０質量％＞
Ｃは、焼き入れ元素として知られている。一般的に溶接金属のミクロ組織は細かいほど衝撃性能が高い。細かいミクロ組織を有する溶接金属を得るには、０．０１質量％以上のＣ添加が有効な手段である。一方、Ｃは固溶強化元素でもあるので、０．１０質量％以上を添加すると溶接金属の強度が上昇しすぎて、衝撃性能は逆に低下する。このため、フラックス入りワイヤのＣ含有量は、ワイヤ全質量あたり、０．０１〜０．１０質量％であることが好ましい。 <C: 0.01 to 0.10% by mass>
C is known as a quenching element. In general, the finer the microstructure of the weld metal, the higher the impact performance. In order to obtain a weld metal having a fine microstructure, addition of 0.01% by mass or more of C is an effective means. On the other hand, since C is also a solid solution strengthening element, when 0.10 mass% or more is added, the strength of the weld metal increases excessively, and the impact performance decreases conversely. For this reason, it is preferable that C content of a flux cored wire is 0.01-0.10 mass% per wire total mass.

＜Ｓｉ：０．５〜１．５質量％＞
Ｓｉは、脱酸元素として必須な元素であるが、多量に添加すると、溶接金属の強度が上昇しすぎて、衝撃性能が劣化する。具体的には、ワイヤ全質量あたりのＳｉ量が、０．５質量％未満の場合、脱酸が不十分となり、ガス欠陥が発生しやすくなり、更に、ビード形状が劣化する場合もある。一方、Ｓｉを、ワイヤ全質量あたり１．５質量％を超えて添加すると、溶接金属の衝撃性能が低下して、健全な溶接継手が得られないことがある。このため、フラックス入りワイヤのＳｉ含有量は、ワイヤ全質量あたり、０．５〜１．５質量％であることが好ましい。なお、ここでいうＳｉには、酸化物の形態で添加されるＳｉは含まない。 <Si: 0.5 to 1.5% by mass>
Si is an essential element as a deoxidizing element. However, if it is added in a large amount, the strength of the weld metal is excessively increased and the impact performance is deteriorated. Specifically, when the amount of Si per total mass of the wire is less than 0.5% by mass, deoxidation becomes insufficient, gas defects are likely to occur, and the bead shape may be further deteriorated. On the other hand, when Si is added in excess of 1.5% by mass with respect to the total mass of the wire, the impact performance of the weld metal is lowered, and a sound welded joint may not be obtained. For this reason, it is preferable that Si content of a flux cored wire is 0.5-1.5 mass% per wire total mass. In addition, Si added here does not include Si added in the form of an oxide.

＜Ｍｎ：１．５〜３．５質量％＞
Ｍｎは、脱酸及び溶接金属の衝撃性能の確保の目的で添加する。一方、Ｍｎを多量に添加すると、溶接金属の強度が上昇しすぎて、母材（下板１、立板２）との間で強度の差が大きくなり、溶接継手の疲労強度が低下しやすくなり、更に、水素割れも発生しやすくなる。具体的には、ワイヤ全質量あたりのＭｎ量が１．５質量％未満の場合、溶接金属の衝撃性能が不十分になることがあり、また、Ｍｎを、ワイヤ全質量あたり３．５質量％を超えて添加すると、溶接金属の強度が高くなりすぎることがある。このため、フラックス入りワイヤのＭｎ含有量は、ワイヤ全質量あたり、１．５〜３．５質量％であることが好ましい。 <Mn: 1.5 to 3.5% by mass>
Mn is added for the purpose of deoxidation and ensuring the impact performance of the weld metal. On the other hand, if Mn is added in a large amount, the strength of the weld metal increases too much, and the difference in strength between the base metal (lower plate 1 and upright plate 2) increases, and the fatigue strength of the welded joint tends to decrease. Furthermore, hydrogen cracking is likely to occur. Specifically, when the amount of Mn per total mass of the wire is less than 1.5% by mass, the impact performance of the weld metal may be insufficient, and Mn may be 3.5% by mass per total mass of the wire. If it is added in excess of, the strength of the weld metal may become too high. For this reason, it is preferable that Mn content of a flux cored wire is 1.5-3.5 mass% per wire total mass.

＜Ｍｇ及びＡｌ：合計で０．１〜２．０質量％＞
Ｍｇ及びＡｌは、強脱酸剤として添加する。溶接金属中の酸素量は、衝撃性能に大きく影響する。そこで、衝撃性能を確保するためには、ＭｇやＡｌを添加して、溶接金属の酸素量を低減させる必要がある。ただし、Ｍｇ及びＡｌの総含有量がワイヤ全質量あたり０．１質量％未満の場合、脱酸効果が十分に得られない。一方、Ｍｇ及びＡｌの総含有量がワイヤ全質量あたり２．０質量％を超えると、溶接作業性が劣化する。このため、フラックス入りワイヤは、Ｍｇ及びＡｌのいずれか一方又は両方を、ワイヤ全質量あたり、合計で０．１〜２．０質量％含有していることが好ましい。 <Mg and Al: 0.1 to 2.0% by mass in total>
Mg and Al are added as strong deoxidizers. The amount of oxygen in the weld metal greatly affects the impact performance. Therefore, in order to ensure impact performance, it is necessary to add Mg or Al to reduce the oxygen content of the weld metal. However, when the total content of Mg and Al is less than 0.1% by mass with respect to the total mass of the wire, the deoxidation effect cannot be sufficiently obtained. On the other hand, when the total content of Mg and Al exceeds 2.0 mass% per the total mass of the wire, welding workability deteriorates. For this reason, it is preferable that the flux-cored wire contains either one or both of Mg and Al in a total amount of 0.1 to 2.0% by mass with respect to the total mass of the wire.

＜ＴｉＯ２：１．５〜６．０質量％＞
ＴｉＯ２は、スラグ発生剤及びアーク安定剤として添加する。しかしながら、ＴｉＯ２含有量が、ワイヤ全質量あたり１．５質量％未満の場合、溶接ビード表面を覆うスラグ量が少なくなり、ビード形状が劣化することがある。一方、ＴｉＯ２含有量が、ワイヤ全質量あたり６．０質量％を超えると、溶着金属中の酸素量が増加して、衝撃性能が低下することがある。このため、フラックス入りワイヤのＴｉＯ２含有量は、ワイヤ全質量あたり、１．５〜６．０質量％であることが好ましい。 <TiO 2: 1.5~6.0 mass%>
TiO 2 is added as a slag generator and arc stabilizer. However, when the TiO 2 content is less than 1.5% by mass with respect to the total mass of the wire, the amount of slag covering the surface of the weld bead decreases, and the bead shape may be deteriorated. On the other hand, if the TiO 2 content exceeds 6.0% by mass with respect to the total mass of the wire, the amount of oxygen in the weld metal increases and the impact performance may be lowered. Therefore, TiO 2 content of the flux cored wire, the wire the total mass per is preferably 1.5 to 6.0 wt%.

＜Ｎａ化合物、Ｋ化合物及びＬｉ化合物：合計で０．０５〜０．４質量％＞
Ｎａ、Ｋ及びＬｉなどのアルカリ金属を含む化合物は、アーク安定剤として作用する。このため、フラックス入りワイヤには、Ｎａ化合物、Ｋ化合物及びＬｉ化合物のうち、少なくとも１種が添加されていることが好ましい。ただし、Ｎａ化合物、Ｋ化合物及びＬｉ化合物の総含有量が、ワイヤ全質量あたり０．０５質量％未満の場合、十分な効果が得られず、アークが不安定となり、良好なビード形状が得られないことがある。 <Na compound, K compound and Li compound: 0.05 to 0.4 mass% in total>
Compounds containing alkali metals such as Na, K and Li act as arc stabilizers. For this reason, it is preferable that at least one of Na compound, K compound and Li compound is added to the flux-cored wire. However, when the total content of the Na compound, K compound and Li compound is less than 0.05 mass% per total mass of the wire, sufficient effects cannot be obtained, the arc becomes unstable, and a good bead shape is obtained. There may not be.

一方、これらのアルカリ金属化合物の総含有量が、ワイヤ全質量あたり０．４質量％を超えても、アークを安定させる効果は変わらず、却ってワイヤが吸湿したり、溶接金属の拡散性水素が高くなって、低温割れが発生しやすくなる。このため、フラックス入りワイヤは、Ｎａ化合物、Ｋ化合物及びＬｉ化合物のうち少なくとも１種の化合物を、ワイヤ全質量あたり、合計で０．０５〜０．４質量％含有していることが好ましい。   On the other hand, even if the total content of these alkali metal compounds exceeds 0.4% by mass per the total mass of the wire, the effect of stabilizing the arc is not changed, but the wire absorbs moisture or the diffusible hydrogen of the weld metal It becomes high and it becomes easy to generate cold cracks. For this reason, it is preferable that the flux-cored wire contains 0.05 to 0.4 mass% in total of at least one compound of Na compound, K compound and Li compound per total mass of the wire.

＜Ａｌ２Ｏ３、ＺｒＯ２及びＳｉＯ２：ＴｉＯ２との合計で２〜８質量％＞
Ａｌ２Ｏ３、ＺｒＯ２及びＳｉＯ２はスラグ発生剤であり、溶接ビードを得るのに不可欠な成分であり、フラックス入りワイヤには、これらのうち少なくとも１種の酸化物が添加されていることが好ましい。なお、前述したように、ＴｉＯ２もスラグ発生剤として作用する。そこで、Ａｌ２Ｏ３、ＺｒＯ２及びＳｉＯ２については、ＴｉＯ２との合計量で規定する。 <Al 2 O 3, ZrO 2 and SiO 2: 2 to 8% by weight, the total of TiO 2>
Al 2 O 3 , ZrO 2 and SiO 2 are slag generators and are indispensable components for obtaining a weld bead, and at least one of these oxides is added to the flux-cored wire. Is preferred. As described above, TiO 2 also acts as a slag generator. Therefore, Al 2 O 3 , ZrO 2 and SiO 2 are defined by the total amount with TiO 2 .

具体的には、Ａｌ２Ｏ３、ＺｒＯ２及びＳｉＯ２の総含有量が、ＴｉＯ２との合計で、ワイヤ全質量あたり２質量％未満の場合、溶接ビード表面を覆うスラグ量が少なくなり、ビード形状が劣化することがある。一方、Ａｌ２Ｏ３、ＺｒＯ２及びＳｉＯ２の総含有量が、ＴｉＯ２との合計で、ワイヤ全質量あたり８質量％を超えると、溶着金属中の酸素量が増加して、衝撃性能が低下することがある。このため、フラックス入りワイヤは、Ａｌ２Ｏ３、ＺｒＯ２及びＳｉＯ２のうち少なくとも１種の酸化物を、ＴｉＯ２との合計で、ワイヤ全質量あたり、２〜８質量％含有していることが好ましい。 Specifically, when the total content of Al 2 O 3 , ZrO 2 and SiO 2 is less than 2% by mass with respect to the total mass of the wire with TiO 2 , the amount of slag covering the weld bead surface is reduced, The bead shape may deteriorate. On the other hand, if the total content of Al 2 O 3 , ZrO 2 and SiO 2 exceeds 8% by mass with respect to the total mass of the wire with TiO 2 , the amount of oxygen in the weld metal increases, and impact performance is reduced. May decrease. Thus, flux cored wire, the Al 2 O 3, at least one oxide of ZrO 2 and SiO 2, the sum of the TiO 2, the total wire mass per to contain 2-8 wt% Is preferred.

＜Ｍｎ／Ｓｉ：１．５〜５．５＞
Ｓｉ及びＭｎは、いずれも脱酸元素として添加されるが、これらの元素の添加比率によっては、ビード形状や溶接金属の衝撃性能に影響を及ぼすことがある。具体的には、ワイヤ全質量あたりのＭｎ含有量（質量％）とＳｉ含有量（質量％）の比（＝ＭＮ／Ｓｉ）が１．５未満の場合、十分な衝撃性能が得られないことがあり、また、Ｍｎ／Ｓｉが５．５を超えると、良好なビード形状が得られないことがある。このため、このため、フラックス入りワイヤにおけるＭｎ含有量（質量％）とＳｉ含有量（質量％）の比（＝ＭＮ／Ｓｉ）は、１．５〜５．５であることが好ましい。 <Mn / Si: 1.5 to 5.5>
Si and Mn are both added as deoxidizing elements. Depending on the addition ratio of these elements, the bead shape and the impact performance of the weld metal may be affected. Specifically, when the ratio of Mn content (mass%) to Si content (mass%) per total mass of wire (= MN / Si) is less than 1.5, sufficient impact performance cannot be obtained. In addition, if Mn / Si exceeds 5.5, a good bead shape may not be obtained. For this reason, it is preferable that ratio (= MN / Si) of Mn content (mass%) and Si content (mass%) in a flux cored wire is 1.5-5.5.

＜Ｎｉ及びＭｏ：合計で０．１〜３．０質量％＞
本実施形態のガスシールドアーク溶接方法で使用されるフラックス入りワイヤは、前述した各成分に加えて、ＮｉやＭｏなどの合金元素を含有していてもよい。各種合金成分のうち、Ｎｉ及びＭｏは、例えば−４０℃における低温靭性や、５９０ＭＰａ以上の高強度の溶接金属を得る場合は必要な合金元素であるため、必要に応じて添加される。なお、Ｎｉ及びＭｏは、両方が添加されていてもよいが、少なくとも一方が添加されていれば、溶接金属の強度向上の効果が得られる。 <Ni and Mo: 0.1 to 3.0% by mass in total>
The flux-cored wire used in the gas shielded arc welding method of the present embodiment may contain alloy elements such as Ni and Mo in addition to the components described above. Among various alloy components, Ni and Mo are necessary alloy elements when obtaining a low-temperature toughness at −40 ° C. or a high-strength weld metal of 590 MPa or more, for example, and are added as necessary. Both Ni and Mo may be added, but if at least one of them is added, the effect of improving the strength of the weld metal can be obtained.

ただし、Ｎｉ及びＭｏの総含有量が、ワイヤ全質量あたり０．１質量％未満の場合、前述した添加効果が得られない。一方、Ｎｉ及びＭｏの総含有量が、ワイヤ全質量あたり３．０質量％を超えると、溶接金属の強度が高くなりすぎる。よって、フラックス入りワイヤにＮｉ及びＭｏを添加する場合は、その総含有量を、ワイヤ全質量あたり０．１〜３．０質量％とすることが好ましい。   However, when the total content of Ni and Mo is less than 0.1% by mass with respect to the total mass of the wire, the above-described addition effect cannot be obtained. On the other hand, if the total content of Ni and Mo exceeds 3.0% by mass with respect to the total mass of the wire, the strength of the weld metal becomes too high. Therefore, when adding Ni and Mo to a flux-cored wire, the total content is preferably 0.1 to 3.0% by mass with respect to the total mass of the wire.

＜Ｆｅ：８６質量％以上＞
Ｆｅ源としては、鋼板外皮、フラックスに添加される鉄粉やＦｅ合金などが挙げられる。Ｆｅ含有量が、ワイヤ質量あたり８６％未満の場合、ワイヤの溶着速度が遅くなり、所定のビード形状が得られにくくなる。よって、Ｆｅ含有量は、ワイヤ質量あたり、８６質量％以上とすることが好ましい。 <Fe: 86% by mass or more>
Examples of the Fe source include a steel sheet outer shell, iron powder added to the flux, and an Fe alloy. When the Fe content is less than 86% per wire mass, the welding speed of the wire becomes slow, and it becomes difficult to obtain a predetermined bead shape. Therefore, the Fe content is preferably 86% by mass or more per wire mass.

＜不可避的不純物＞
本実施形態のガスシールドアーク溶接方法で使用されるフラックス入りワイヤの成分組成における残部は、不可避的不純物である。本実施形態で使用するフラックス入りワイヤにおける不可避的不純物としては、Ｂ及びＢ化合物、ＲＥＭ（希土類元素）、Ｐ、Ｓ、Ａｌ、Ａｌ２Ｏ３、Ｃｒ、Ｎｂ、Ｖ、Ｃｕ、Ｔｉ、Ｍｇ、Ｃａ及びＮなどが挙げられる。 <Inevitable impurities>
The remainder in the component composition of the flux-cored wire used in the gas shielded arc welding method of this embodiment is an inevitable impurity. Inevitable impurities in the flux-cored wire used in the present embodiment include B and B compounds, REM (rare earth element), P, S, Al, Al 2 O 3 , Cr, Nb, V, Cu, Ti, Mg, Ca, N, etc. are mentioned.

＜製造方法＞
フラックス入りワイヤの製造方法は、特に限定されるものではないが、例えば、以下に示す方法で製造することができる。先ず、外皮を構成する鋼帯を、長手方向に送りながら成形ロールにより成形し、Ｕ字状のオープン管にする。次に、フラックスが所定の化学組成となるように、酸化物と、金属又は合金と、Ｆｅ粉などを所要量配合し、これを外皮に充填した後、断面が円形になるように加工する。その後、冷間引き抜き加工により伸線し、例えば１．２〜１．６ｍｍのワイヤ径とする。なお、冷間加工途中に加工硬化したワイヤを軟化させるために、焼鈍を施してもよい。 <Manufacturing method>
Although the manufacturing method of a flux cored wire is not specifically limited, For example, it can manufacture with the method shown below. First, a steel strip constituting the outer skin is formed by a forming roll while being sent in the longitudinal direction, and a U-shaped open tube is formed. Next, required amounts of oxide, metal or alloy, Fe powder, and the like are blended so that the flux has a predetermined chemical composition, and this is filled in the outer shell, and then processed so that the cross section becomes circular. Thereafter, the wire is drawn by cold drawing to have a wire diameter of, for example, 1.2 to 1.6 mm. In order to soften the work-hardened wire during the cold working, annealing may be performed.

［破断強度：３００〜９００ＭＰａ］
電極ワイヤ４の破断強度は、送給性に大きな影響を及ぼす。具体的には、電極ワイヤ４の破断強度が３００ＭＰａ未満の場合、ワイヤが座屈しやすく、安定して送給することができないことがある。一方、電極ワイヤの破断強度が９００ＭＰａを超えると、ライナとの接触が強くなり、摩擦抵抗が高くなりすぎて、送給性が低下することがある。このため、電極ワイヤ４の破断強度は、３００〜９００ＭＰａであることが好ましい。なお、ここでいう破断強度は、ＪＩＳ Ｚ ２２４１に規定される方法により測定した値である。 [Break strength: 300 to 900 MPa]
The breaking strength of the electrode wire 4 greatly affects the feedability. Specifically, when the breaking strength of the electrode wire 4 is less than 300 MPa, the wire is likely to buckle and cannot be stably fed. On the other hand, when the breaking strength of the electrode wire exceeds 900 MPa, the contact with the liner becomes strong, the frictional resistance becomes too high, and the feedability may be lowered. For this reason, it is preferable that the breaking strength of the electrode wire 4 is 300-900 MPa. In addition, the breaking strength here is the value measured by the method prescribed | regulated to JISZ2241.

以上詳述したように、本実施形態のガスシールドアーク溶接方法は、水平方向に対して下板を傾けて、特定条件ですみ肉溶接しているため、下板とＵリブや縦リブとのすみ肉溶接において、溶込みは立板（リブ材）の板厚の８割以上でかつ完全溶込みにはならず、更に、アンダーカットフリーで滑らかな溶接ビードが得られる。その結果、適度な溶け込みを有し、溶接ビードが良好なすみ肉溶接継手が得られる。   As described above in detail, the gas shield arc welding method of the present embodiment tilts the lower plate with respect to the horizontal direction and fillet welds under specific conditions. In fillet welding, the penetration is not less than 80% of the thickness of the standing plate (rib material) and does not become complete penetration, and a smooth weld bead can be obtained that is free of undercut. As a result, a fillet welded joint having an appropriate penetration and a good weld bead is obtained.

以下、本発明の実施例及び比較例を挙げて、本発明の効果について具体的に説明する。本実施例においては、下板（材質：ＪＩＳ Ｇ ３１０６ ＳＭ４９０Ａ、サイズ：厚さ１６ｍｍ、幅１００ｍｍ、長さ７５０ｍｍ）と、立板（材質：ＪＩＳ Ｇ ３１０６ ＳＭ４９０Ａ、サイズ：厚さ９ｍｍ、幅１００ｍｍ、長さ７５０ｍｍ）を、下記表１に示す組成で、フラックス充填率が１５．０質量％、破断強度が６５０ＭＰａのフラックス入りワイヤを使用し、その他の条件を変えて片側すみ肉ガスシールドアーク溶接を行い、溶け込み及び溶接ビードなどを評価した。   Hereinafter, the effects of the present invention will be specifically described with reference to Examples and Comparative Examples of the present invention. In this embodiment, a lower plate (material: JIS G 3106 SM490A, size: thickness 16 mm, width 100 mm, length 750 mm) and a vertical plate (material: JIS G 3106 SM490A, size: thickness 9 mm, width 100 mm, 750 mm in length) with a composition shown in Table 1 below, using a flux-cored wire with a flux filling rate of 15.0 mass% and a breaking strength of 650 MPa, and changing the other conditions, one-side fillet gas shielded arc welding was performed. And the penetration and weld bead were evaluated.

［評価基準］
図３Ａ〜Ｃは溶け込み及びビード形状の判断基準例を示す顕微鏡写真であり、図３Ａ及びＣは不良の例を示し、図３Ｂは良好の例を示す。溶け込み形状の評価は、図３Ａに示すように溶込みが立板（リブ材）の板厚の８割未満の場合又は図３Ｃに示すように溶け込みが立板（リブ材）貫通していた場合を不良（×）、図３Ｂに示すように、溶込みが（リブ材）の板厚の８割以上でかつ完全溶込みでなかった場合を良好（○）、更に溶け込みが（リブ材）の板厚の８．５〜９．５割であった場合を優良（◎）とした。また、ビード形状の評価は、アンダーカットが発生した場合を不良（×）、アンダーカットが発生しなかった場合を良好（○）、更に、凸形状にならず滑らかなビードであった場合を優良（◎）とした。 [Evaluation criteria]
3A to C are micrographs showing examples of criteria for determining the penetration and bead shape, FIGS. 3A and 3C show examples of defects, and FIG. 3B shows a good example. The penetration shape is evaluated when the penetration is less than 80% of the thickness of the standing plate (rib material) as shown in FIG. 3A or when the penetration penetrates the standing plate (rib material) as shown in FIG. 3C. 3 (B), as shown in FIG. 3B, when the penetration was 80% or more of the (rib material) thickness and was not complete penetration (○), the penetration was further (rib material). The case where it was 8.5 to 9.5% of the plate thickness was judged as excellent (◎). In addition, the bead shape is evaluated as poor (×) when undercut occurs, good (○) when undercut does not occur, and excellent when the bead is smooth and not convex. (◎).

＜第１実施例＞
先ず、直径Ｄが異なる複数の電極ワイヤを使用し、それ以外の条件は同じにして溶接を行った。この第１実施例では、ビード形状及び溶け込み形状と併せて、ワイヤ送給性についても評価した。ワイヤ送給性の評価は、所定のワイヤ送給速度（無負荷の場合に相当）の８割未満の速度しか出なかった場合を不良（×）、８割以上が出た場合を良好（○）、更に、所定のワイヤ送給速度の９割以上が出た場合は優良（◎）とした。 <First embodiment>
First, a plurality of electrode wires having different diameters D were used, and welding was performed under the same conditions. In the first embodiment, the wire feedability was also evaluated together with the bead shape and the penetration shape. Evaluation of wire feedability is good when the wire feed speed is less than 80% of the predetermined wire feed speed (corresponding to no load) (x), and when 80% or more is good (○ ) Furthermore, when 90% or more of the predetermined wire feeding speed was obtained, it was judged as excellent (◎).

上記表２に示す比較例１，２は、ワイヤ径Ｄが本発明の範囲よりも太い場合の例であり、ワイヤ送給がスムーズではなく、その結果ビード形状も不良であった。また、比較例６，７は、ワイヤ径Ｄが本発明の範囲よりも細い場合の例であり、電極ワイヤが溶接中に座屈しやすく、ワイヤ送給性も低下し、良好なビードが得られなかった。これに対して、実施例３〜５は、ビード形状、溶け込み形状及びワイヤ送給性のいずれもが良好であった。   Comparative Examples 1 and 2 shown in Table 2 above are examples in which the wire diameter D is thicker than the range of the present invention, and the wire feeding was not smooth, and as a result, the bead shape was also poor. Further, Comparative Examples 6 and 7 are examples in which the wire diameter D is thinner than the range of the present invention, and the electrode wire is likely to buckle during welding, the wire feedability is reduced, and a good bead is obtained. There wasn't. On the other hand, in Examples 3 to 5, all of the bead shape, the penetration shape, and the wire feeding property were good.

＜第２実施例＞
第２実施例では、電極ワイヤの溶接方向における傾斜角度αを変えて、それ以外の条件は同じにして溶接を行い、ビード形状及び溶け込み形状を評価した。各種条件及び評価結果を下記表３にまとめて示す。 <Second embodiment>
In the second example, the bead shape and the penetration shape were evaluated by changing the inclination angle α in the welding direction of the electrode wire and performing the welding under the same other conditions. Various conditions and evaluation results are summarized in Table 3 below.

上記表３に示す比較例８は電極ワイヤの後退角が大きすぎて、ビード形状及び溶け込み形状が劣化した。また、比較例１３は、前進角が大きすぎて、ビード形状は良好であったが、溶け込みが浅くなり、立板（リブ材）板厚の８割に満たなかった。これに対して、実施例９〜１２は、ビード形状及び溶け込み形状共に良好であった。   In Comparative Example 8 shown in Table 3 above, the receding angle of the electrode wire was too large, and the bead shape and the penetration shape deteriorated. In Comparative Example 13, the advancing angle was too large and the bead shape was good, but the penetration was shallow, and it was less than 80% of the standing plate (rib material) plate thickness. On the other hand, Example 9-12 was favorable in bead shape and penetration shape.

＜第３実施例＞
第３実施例では、下板と立板とがなす角度θを変えて、それ以外の条件は同じにして溶接を行い、ビード形状及び溶け込み形状を評価した。各種条件及び評価結果を下記表４にまとめて示す。 <Third embodiment>
In the third example, the bead shape and the penetration shape were evaluated by changing the angle θ formed by the lower plate and the upright plate and performing the welding under the same other conditions. Various conditions and evaluation results are summarized in Table 4 below.

上記表４に示す比較例１４は、下板と立板とがなす角度θが本発明の範囲よりも小さかったため、ビード形状及び溶け込み形状とも不良であった。また、比較例１８は、下板と立板とがなす角度θが本発明の範囲よりも大きかったため、溶け込み形状は良好であったが、十分な脚長が得られず、良好なビード形状は得られなかった。これに対して、実施例１５〜１７は、ビード形状及び溶け込み形状共に良好であった。   In Comparative Example 14 shown in Table 4 above, since the angle θ formed by the lower plate and the upright plate was smaller than the range of the present invention, both the bead shape and the penetration shape were poor. Further, in Comparative Example 18, since the angle θ formed by the lower plate and the upright plate was larger than the range of the present invention, the penetration shape was good, but a sufficient leg length was not obtained and a good bead shape was obtained. I couldn't. On the other hand, in Examples 15 to 17, both the bead shape and the penetration shape were good.

＜第４実施例＞
第４実施例では、下板の水平方向に対する傾斜角度βを変えて、それ以外の条件は同じにして溶接を行い、ビード形状及び溶け込み形状を評価した。各種条件及び評価結果を下記表５にまとめて示す。 <Fourth embodiment>
In the fourth example, the bead shape and the penetration shape were evaluated by changing the inclination angle β with respect to the horizontal direction of the lower plate and performing welding under the same other conditions. Various conditions and evaluation results are summarized in Table 5 below.

上記表５に示す比較例１９は、傾斜角度βが本発明の範囲よりも小さいため、良好なビード形状及び溶け込み形状が得られなかった。また、比較例２３は、傾斜角度βが本発明の範囲よりも大きいため、図３Ｃに示すように、溶接金属が立板（リブ材）を貫通してしまった。これに対して、実施例２０〜２２は、ビード形状及び溶け込み形状共に良好であった。   In Comparative Example 19 shown in Table 5 above, since the inclination angle β was smaller than the range of the present invention, a good bead shape and penetration shape could not be obtained. In Comparative Example 23, since the inclination angle β is larger than the range of the present invention, as shown in FIG. 3C, the weld metal has penetrated the standing plate (rib material). On the other hand, in Examples 20 to 22, both the bead shape and the penetration shape were good.

＜第５実施例＞
第５実施例では、電極ワイヤと下板とがなす角度γを変えて、それ以外の条件は同じにして溶接を行い、ビード形状及び溶け込み形状を評価した。各種条件及び評価結果を下記表６にまとめて示す。 <Fifth embodiment>
In the fifth example, the bead shape and the penetration shape were evaluated by changing the angle γ formed by the electrode wire and the lower plate and performing the welding under the same other conditions. Various conditions and evaluation results are summarized in Table 6 below.

上記表６に示す比較例２４は、角度γが本発明の範囲よりも小さいため、立板の脚長が小さくなり、ビード形状が劣化し、更に、完全溶け込みとなった。また、比較例２８は、角度γが本発明の範囲よりも大きいため、良好なビード形状が得られず、また、溶け込みも立板（リブ材）の板厚の８割未満であった。これに対して、実施例２５〜２７は、ビード形状及び溶け込み形状共に良好であった。   In Comparative Example 24 shown in Table 6 above, since the angle γ was smaller than the range of the present invention, the leg length of the upright plate was reduced, the bead shape was deteriorated, and further, the penetration was complete. In Comparative Example 28, since the angle γ was larger than the range of the present invention, a good bead shape was not obtained, and the penetration was less than 80% of the thickness of the standing plate (rib material). On the other hand, in Examples 25 to 27, both the bead shape and the penetration shape were good.

＜第６実施例＞
第６実施例では、溶接速度を変えて、それ以外の条件は同じにして溶接を行い、ビード形状及び溶け込み形状を評価した。各種条件及び評価結果を下記表７にまとめて示す。なお、下記表７に示すＮｏ．２９〜３４は、いずれも本発明の範囲内の実施例である。 <Sixth embodiment>
In the sixth example, welding was performed under the same conditions except that the welding speed was changed, and the bead shape and the penetration shape were evaluated. Various conditions and evaluation results are summarized in Table 7 below. In addition, No. shown in Table 7 below. 29 to 34 are all examples within the scope of the present invention.

上記表７に示すように、実施例３０〜３３は、溶接速度を２００〜７００ｍｍ／分の範囲にしているため、ビード形状及び溶け込み形状共に優れていた。一方、実施例２９は、溶接速度が遅めであったため、溶接金属が多くなり、ビード形状がやや垂れ気味であった。また、実施例３４は、溶接速度が速かったため、溶け込みが立板（リブ材）の板厚の８割ぎりぎりとなり、余裕がなかった。   As shown in Table 7 above, Examples 30 to 33 were excellent in both bead shape and penetration shape because the welding speed was in the range of 200 to 700 mm / min. On the other hand, in Example 29, since the welding speed was slow, the amount of weld metal increased, and the bead shape was slightly drooping. Further, in Example 34, since the welding speed was high, the penetration was just below 80% of the thickness of the standing plate (rib material), and there was no margin.

＜第７実施例＞
第７実施例では、溶接電流を変えて、それ以外の条件は同じにして溶接を行い、ビード形状及び溶け込み形状を評価した。各種条件及び評価結果を下記表８にまとめて示す。なお、下記表８に示すＮｏ．３５〜４０は、いずれも本発明の範囲内の実施例である。 <Seventh embodiment>
In the seventh example, welding was performed under the same conditions except that the welding current was changed, and the bead shape and the penetration shape were evaluated. Various conditions and evaluation results are summarized in Table 8 below. In addition, No. shown in Table 8 below. 35 to 40 are all examples within the scope of the present invention.

上記表８に示すように、実施例３６〜３９は、溶接電流が２００〜４５０Ａであったため、ビード形状及び溶け込み形状共に優れていた。一方、実施例３５は、溶接電流が低かったため、溶け込みが立板（リブ材）の板厚の８割ぎりぎりとなり、余裕がなかった。また、実施例４０は、溶接電流が高めであったため、ビード形状がやや垂れ気味であった。   As shown in Table 8 above, Examples 36 to 39 were excellent in both the bead shape and the penetration shape because the welding current was 200 to 450 A. On the other hand, in Example 35, since the welding current was low, the penetration was just below 80% of the thickness of the standing plate (rib material), and there was no room. Further, in Example 40, since the welding current was high, the bead shape was slightly drooping.

＜第８実施例＞
第８実施例では、アーク電圧を変えて、それ以外の条件は同じにして溶接を行い、ビード形状及び溶け込み形状を評価した。各種条件及び評価結果を下記表９にまとめて示す。なお、下記表９に示すＮｏ．４１〜４６は、いずれも本発明の範囲内の実施例である。 <Eighth embodiment>
In the eighth example, welding was performed under the same conditions except that the arc voltage was changed, and the bead shape and the penetration shape were evaluated. Various conditions and evaluation results are summarized in Table 9 below. In addition, No. shown in Table 9 below. 41 to 46 are all examples within the scope of the present invention.

上記表９に示すように、実施例４２〜４５は、アーク電圧が２０〜４５Ｖであったため、ビード形状及び溶け込み形状共に優れていた。一方、実施例４１は、アーク電圧が低かったため、ビード形状がやや凸形状であった。また、実施例４６は、本アーク電圧が高めであったため、アーク長が長くなり、溶け込みが立板（リブ材）の板厚の８割ぎりぎりとなり、余裕がなかった。   As shown in Table 9 above, Examples 42 to 45 had excellent bead shape and penetration shape because the arc voltage was 20 to 45 V. On the other hand, in Example 41, since the arc voltage was low, the bead shape was slightly convex. In Example 46, the arc voltage was high, so the arc length was long, and the penetration was just below 80% of the plate thickness of the standing plate (rib material), so there was no room.

＜第９実施例＞
第９実施例では、チップ母材間距離を変えて、それ以外の条件は同じにして溶接を行い、ビード形状及び溶け込み形状を評価した。各種条件及び評価結果を下記表１０にまとめて示す。なお、下記表１０に示すＮｏ．４７〜５１は、いずれも本発明の範囲内の実施例である。 <Ninth embodiment>
In the ninth example, welding was performed under the same conditions except that the distance between the tip base materials was changed, and the bead shape and the penetration shape were evaluated. Various conditions and evaluation results are summarized in Table 10 below. In addition, No. shown in Table 10 below. 47 to 51 are all examples within the scope of the present invention.

上記表１０に示すように、チップ母材間距離を１５〜３５ｍｍにした実施例４８〜５０は、ビード形状及び溶け込み形状共に優れていた。一方、実施例４７は、チップ母材間距離が短かったため、ノズルとリブ材との干渉を避けるために、溶接トーチの下板に対する角度（γ）を小さくする必要があった。このため、溶接金属がやや下板に寄っており、ビード形状及び溶け込み形状がやや不安定であった。また、実施例５１は、チップ母材間の距離が長かったため、溶接中の振動などにより、ビード形状がやや不安定であった。   As shown in Table 10 above, Examples 48 to 50 in which the distance between the chip base materials was 15 to 35 mm were excellent in both the bead shape and the penetration shape. On the other hand, in Example 47, since the distance between the tip base materials was short, it was necessary to reduce the angle (γ) with respect to the lower plate of the welding torch in order to avoid interference between the nozzle and the rib material. For this reason, the weld metal is slightly closer to the lower plate, and the bead shape and the penetration shape are somewhat unstable. Further, in Example 51, since the distance between the tip base materials was long, the bead shape was slightly unstable due to vibration during welding or the like.

＜第１０実施例＞
第１０実施例では、フラックス充填率が異なるフラックス入りワイヤを使用し、下記表１１に示す溶接条件で溶接を行い、溶接金属の衝撃性能及びビード形状を評価した。 <Tenth embodiment>
In the tenth example, flux-cored wires having different flux filling rates were used, and welding was performed under the welding conditions shown in Table 11 below, and the impact performance and bead shape of the weld metal were evaluated.

本実施例で用いた各フラックス入りワイヤのフラックス充填率、成分組成及びワイヤの破断強度を、下記表１２に示す。なお、下記表１２に示すＮｏ．５２〜５６のフラックス入りワイヤは、いずれも本発明の範囲内の実施例である。また、各ワイヤの破断強度は、各試験材から、ＪＩＳ Ｚ ２２４１ ２号に対応した試験片を作製し、ＪＩＳ Ｚ ２２４１に準拠した方法で測定した値であり、以下の実施例においても同様である。   Table 12 below shows the flux filling rate, component composition, and breaking strength of each flux-cored wire used in this example. In addition, No. shown in Table 12 below. 52 to 56 flux cored wires are all examples within the scope of the present invention. Moreover, the breaking strength of each wire is a value measured by a method in accordance with JIS Z 2241 by preparing a test piece corresponding to JIS Z 2241 2 from each test material, and the same applies to the following examples. is there.

また、下記表１３に各フラックス入りワイヤの評価結果を示す。なお、下記表１３に示す溶接金属の衝撃性能の評価は、各サンプルについて、ＪＩＳ Ｚ ３３１３に準拠して、−２０℃における吸収エネルギーを３回測定し、その平均値が４７Ｊ未満の場合を不良（×）、４７Ｊ以上の場合を良好（○）、更に、６０Ｊ以上の場合を優良（◎）とした。   Table 13 below shows the evaluation results of each flux-cored wire. In addition, evaluation of the impact performance of the weld metal shown in the following Table 13 is based on JIS Z 3313, and the absorbed energy at −20 ° C. is measured three times for each sample, and the average value is less than 47 J. (X), the case of 47J or more was judged as good (◯), and the case of 60J or more was judged as excellent (◎).

上記表１３に示すように、フラックス充填率が１０〜２０質量％のフラックス入りワイヤを用いた実施例５３〜５５は、溶接金属の衝撃性能が高く及びビード形状も優れていた。一方、実施例５２は、フラックスの充填率が低かったため、ビード形状がやや垂れ気味であった。また、実施例５６は、フラックス充填率が高かったため、衝撃性能が４７Ｊ以上ではあったが、６０Ｊには届かなかった。   As shown in Table 13 above, Examples 53 to 55 using flux-cored wires with a flux filling rate of 10 to 20% by mass had high weld metal impact performance and excellent bead shape. On the other hand, in Example 52, since the filling rate of the flux was low, the bead shape was slightly drooping. Further, in Example 56, since the flux filling rate was high, the impact performance was 47 J or more, but it did not reach 60 J.

＜第１１実施例＞
第１１実施例では、Ｃ含有量が異なるフラックス入りワイヤを使用し、上記表１１に示す溶接条件で溶接を行い、溶接金属の衝撃性能及びビード形状を評価した。本実施例で用いた各フラックス入りワイヤのフラックス充填率、成分組成及びワイヤ強度を下記表１４に、評価結果を下記表１５に、それぞれ示す。なお、下記表１４及び表１５に示すＮｏ．５７〜６１のフラックス入りワイヤは、いずれも本発明の範囲内の実施例である。 <Eleventh embodiment>
In the eleventh example, flux-cored wires having different C contents were used, welding was performed under the welding conditions shown in Table 11 above, and the impact performance and bead shape of the weld metal were evaluated. The flux filling rate, component composition, and wire strength of each flux-cored wire used in this example are shown in Table 14 below, and the evaluation results are shown in Table 15 below. In addition, No. shown in the following Table 14 and Table 15. All the flux cored wires 57 to 61 are examples within the scope of the present invention.

上記表１３に示すように、Ｃ含有量が０．０１〜０．１０質量％のフラックス入りワイヤを用いた実施例５８〜６０は、溶接金属の衝撃性能が高く及びビード形状も優れていた。一方、実施例５７は、Ｃ含有量が少なかったため、溶接金属の組織はやや粗く、衝撃性能が４７Ｊ以上ではあったが、６０Ｊには届かなかった。また、実施例６１は、Ｃ含有量が多めであったため、硬いベーナイト組織になるので、衝撃性能が４７Ｊ以上ではあったが、６０Ｊには届かなかった。   As shown in Table 13 above, Examples 58 to 60 using a flux-cored wire having a C content of 0.01 to 0.10% by mass had high weld metal impact performance and an excellent bead shape. On the other hand, in Example 57, since the C content was small, the structure of the weld metal was slightly rough and the impact performance was 47 J or more, but it did not reach 60 J. Further, in Example 61, since the C content was large, a hard bainite structure was formed, so the impact performance was 47 J or more, but it did not reach 60 J.

＜第１２実施例＞
第１２実施例では、Ｓｉ含有量が異なるフラックス入りワイヤを使用し、上記表１１に示す溶接条件で溶接を行い、溶接金属の衝撃性能及びビード形状を評価した。本実施例で用いた各フラックス入りワイヤのフラックス充填率、成分組成及びワイヤ強度を下記表１６に、評価結果を下記表１７に、それぞれ示す。なお、下記表１６及び表１７に示すＮｏ．６２〜６６のフラックス入りワイヤは、いずれも本発明の範囲内の実施例である。 <Twelfth embodiment>
In the twelfth example, flux-cored wires having different Si contents were used, and welding was performed under the welding conditions shown in Table 11 above, and the impact performance and bead shape of the weld metal were evaluated. The flux filling rate, component composition, and wire strength of each flux-cored wire used in this example are shown in Table 16 below, and the evaluation results are shown in Table 17 below. In addition, No. shown in the following Table 16 and Table 17. 62-66 flux cored wires are all examples within the scope of the present invention.

上記表１７に示すように、Ｓｉ含有量が０．５〜１．５質量％のフラックス入りワイヤを用いた実施例６３〜６５は、溶接金属の衝撃性能が高く及びビード形状も優れていた。一方、実施例６２は、Ｓｉ含有量が少なかったため、ビードの母材とのなじみが若干劣ってた。また、実施例６６は、Ｓｉ含有量が多めであったため、衝撃性能が４７Ｊ以上ではあったが、６０Ｊには届かなかった。   As shown in Table 17 above, Examples 63 to 65 using a flux-cored wire having a Si content of 0.5 to 1.5% by mass had high weld metal impact performance and excellent bead shape. On the other hand, in Example 62, since the Si content was small, the familiarity with the base material of the beads was slightly inferior. In Example 66, since the Si content was large, the impact performance was 47 J or more, but it did not reach 60 J.

＜第１３実施例＞
第１３実施例では、Ｍｎ含有量が異なるフラックス入りワイヤを使用し、上記表１１に示す溶接条件で溶接を行い、溶接金属の衝撃性能及びビード形状を評価した。本実施例で用いた各フラックス入りワイヤのフラックス充填率、成分組成及びワイヤ強度を下記表１８に、評価結果を下記表１９に、それぞれ示す。なお、下記表１８及び表１９に示すＮｏ．６７〜７１のフラックス入りワイヤは、いずれも本発明の範囲内の実施例である。 <Thirteenth embodiment>
In the thirteenth example, flux-cored wires having different Mn contents were used and welding was performed under the welding conditions shown in Table 11 above, and the impact performance and bead shape of the weld metal were evaluated. The flux filling rate, component composition, and wire strength of each flux-cored wire used in this example are shown in Table 18 below, and the evaluation results are shown in Table 19 below. In addition, No. shown in Table 18 and Table 19 below. 67 to 71 flux-cored wires are all examples within the scope of the present invention.

上記表１９に示すように、Ｍｎ含有量が１．５〜３．５質量％のフラックス入りワイヤを用いた実施例６３〜６５は、溶接金属の衝撃性能が高く及びビード形状も優れていた。一方、実施例６２は、Ｍｎ含有量が少なかったため、衝撃性能が４７Ｊ以上ではあったが、６０Ｊには届かなかった。また、実施例６６は、Ｍｎ含有量が多めであったため、溶接金属が高強度化され、衝撃性能が６０Ｊには届かなかった。   As shown in Table 19 above, Examples 63 to 65 using flux-cored wires having a Mn content of 1.5 to 3.5% by mass had high weld metal impact performance and excellent bead shape. On the other hand, in Example 62, since the Mn content was small, the impact performance was 47 J or more, but it did not reach 60 J. In Example 66, since the Mn content was large, the weld metal was strengthened, and the impact performance did not reach 60J.

＜第１４実施例＞
強脱酸剤であるＭｇ若しくはＡｌ又はその両方の含有量が異なるフラックス入りワイヤを使用し、上記表１１に示す溶接条件で溶接を行い、溶接金属の衝撃性能及びビード形状を評価した。本実施例で用いた各フラックス入りワイヤのフラックス充填率、成分組成及びワイヤ強度を下記表２０に、評価結果を下記表２１に、それぞれ示す。なお、下記表２０及び表２１に示すＮｏ．７２〜７６のフラックス入りワイヤは、いずれも本発明の範囲内の実施例である。 <14th embodiment>
Using flux-cored wires having different contents of Mg or Al, which are strong deoxidizers, or both, welding was performed under the welding conditions shown in Table 11 above, and the impact performance and bead shape of the weld metal were evaluated. The flux filling rate, component composition, and wire strength of each flux-cored wire used in this example are shown in Table 20 below, and the evaluation results are shown in Table 21 below. In addition, No. shown in Table 20 and Table 21 below. 72-76 flux cored wires are all examples within the scope of the present invention.

上記表２１に示すように、Ｍｇ及びＡｌの総含有量が０．１〜２．０質量％のフラックス入りワイヤを用いた実施例７３〜７５は、溶接金属の衝撃性能が優れていた。一方、実施例７２は、ＭｇおよびＡｌ含有量が少なかったため、衝撃性能が４７Ｊ以上ではあったが、６０Ｊには届かなかった。また、実施例７６は、ＭｇおよびＡｌ含有量が多めであったため、溶接作業性の劣化に起因したビード形状がやや不安定であった。   As shown in Table 21 above, Examples 73 to 75 using flux-cored wires having a total content of Mg and Al of 0.1 to 2.0 mass% were excellent in impact performance of the weld metal. On the other hand, in Example 72, since the contents of Mg and Al were small, the impact performance was 47 J or more, but it did not reach 60 J. Further, in Example 76, since the contents of Mg and Al were large, the bead shape resulting from the deterioration of welding workability was somewhat unstable.

＜第１５実施例＞
第１５実施例では、ＴｉＯ２含有量が異なるフラックス入りワイヤを使用し、上記表１１に示す溶接条件で溶接を行い、溶接金属の衝撃性能及びビード形状を評価した。本実施例で用いた各フラックス入りワイヤのフラックス充填率、成分組成及びワイヤ強度を下記表２２に、評価結果を下記表２３に、それぞれ示す。なお、下記表２２及び表２３に示すＮｏ．７７〜８１のフラックス入りワイヤは、いずれも本発明の範囲内の実施例である。 <Fifteenth embodiment>
In the fifteenth example, flux-cored wires having different TiO 2 contents were used and welding was performed under the welding conditions shown in Table 11 above, and the impact performance and bead shape of the weld metal were evaluated. The flux filling rate, component composition, and wire strength of each flux-cored wire used in this example are shown in Table 22 below, and the evaluation results are shown in Table 23 below. In addition, No. shown in Table 22 and Table 23 below. 77 to 81 flux-cored wires are all examples within the scope of the present invention.

上記表２３に示すように、ＴｉＯ２含有量が１．５〜６．０質量％のフラックス入りワイヤを用いた実施例７８〜８０は、溶接金属の衝撃性能が高く及びビード形状も優れていた。一方、実施例７７は、ＴｉＯ２含有量が少なかったため、ビード形状がやや不安定であった。また、実施例８１は、ＴｉＯ２含有量が多めであったため、衝撃性能が４７Ｊ以上ではあったが、６０Ｊには届かなかった。 As shown in Table 23, Examples 78 to 80 using a flux-cored wire having a TiO 2 content of 1.5 to 6.0% by mass had high weld metal impact performance and excellent bead shape. . On the other hand, in Example 77, the bead shape was somewhat unstable due to a low TiO 2 content. Further, in Example 81, since the TiO 2 content was large, the impact performance was 47 J or more, but it did not reach 60 J.

＜第１６実施例＞
第１６実施例では、アーク安定剤としてのアルカリ金属の含有量が異なるフラックス入りワイヤを使用し、下記表２４に示す溶接条件で溶接を行い、溶接金属の拡散水素量及びビード形状を評価した。 <Sixteenth embodiment>
In the sixteenth example, flux-cored wires having different alkali metal contents as an arc stabilizer were used, and welding was performed under the welding conditions shown in Table 24 below, and the diffusion hydrogen amount and bead shape of the weld metal were evaluated.

本実施例で用いた各フラックス入りワイヤのフラックス充填率、成分組成及びワイヤ強度を、下記表２５に示す。なお、下記表２５に示すＮｏ．８２〜８７のフラックス入りワイヤは、いずれも本発明の範囲内の実施例である。   Table 25 below shows the flux filling rate, component composition, and wire strength of each flux-cored wire used in this example. In addition, No. shown in Table 25 below. 82 to 87 flux cored wires are all examples within the scope of the present invention.

また、下記表２６に各フラックス入りワイヤの評価結果を示す。なお、下記表２６に示す拡散水素量の評価は、ＪＩＳ Ｚ ３１１８に準拠した方法により行い、その結果、拡散性水素量が８．０ｍｌ／１００ｇを超えていた場合を不良（×）、８．０ｍｌ／１００ｇ以下の場合を良好（○）、更に５．０ｍｌ／１００ｇ以下の場合を優良（◎）とした。   Table 26 below shows the evaluation results of each flux-cored wire. In addition, evaluation of the diffusion hydrogen amount shown in the following Table 26 is performed by a method based on JIS Z 3118. As a result, the case where the amount of diffusible hydrogen exceeds 8.0 ml / 100 g is defective (x). The case of 0 ml / 100 g or less was evaluated as good (◯), and the case of 5.0 ml / 100 g or less was evaluated as excellent (◎).

上記表２６に示すように、Ｎａ化合物、Ｎａ化合物及びＬｉ化合物の総含有量が０．０５〜０．４質量％の範囲内のフラックス入りワイヤを用いた実施例８３〜８６は、溶接金属中の拡散性水素量が低く及びビード形状も優れていた。一方、実施例８２は、Ｎａ化合物、Ｋ化合物及びＬｉ化合物の総含有量が少なかったため、アークがやや不安定になり、ビード形状がやや不安定であった。また、実施例８７は、Ｎａ化合物、Ｋ化合物及びＬｉ化合物の総含有量が多めであったため、ワイヤが吸湿し、拡散性水素量が８．０ｍｌ／１００ｇ以下ではあったが、５．０ｍｌ／１００ｇ以上であった。   As shown in Table 26 above, Examples 83 to 86 using flux-cored wires in which the total content of Na compound, Na compound and Li compound was in the range of 0.05 to 0.4% by mass included in the weld metal The amount of diffusible hydrogen was low and the bead shape was excellent. On the other hand, in Example 82, since the total content of the Na compound, the K compound, and the Li compound was small, the arc was slightly unstable and the bead shape was slightly unstable. In Example 87, the total content of Na compound, K compound and Li compound was higher, so the wire absorbed moisture and the amount of diffusible hydrogen was 8.0 ml / 100 g or less, but 5.0 ml / It was 100 g or more.

＜第１７実施例＞
第１７実施例では、スラグ発生剤の添加量が異なるフラックス入りワイヤを使用し、上記表１１に示す溶接条件で溶接を行い、溶接金属の衝撃性能及びビード形状を評価した。本実施例で用いた各フラックス入りワイヤのフラックス充填率、成分組成及びワイヤ強度を下記表２７に、評価結果を下記表２８に、それぞれ示す。なお、下記表２７及び表２８に示すＮｏ．８８〜９２のフラックス入りワイヤは、いずれも本発明の範囲内の実施例である。 <Seventeenth embodiment>
In the seventeenth example, flux-cored wires with different amounts of slag generator were used and welding was performed under the welding conditions shown in Table 11 above, and the impact performance and bead shape of the weld metal were evaluated. The flux filling rate, component composition, and wire strength of each flux-cored wire used in this example are shown in Table 27 below, and the evaluation results are shown in Table 28 below. In addition, No. shown in the following Table 27 and Table 28. 88 to 92 flux cored wires are all examples within the scope of the present invention.

上記表２８に示すように、Ａｌ２Ｏ３、ＺｒＯ２、ＳｉＯ２及びＴｉＯ２の総含有量が２〜８質量％であるフラックス入りワイヤを用いた実施例８９〜９１は、溶接金属の衝撃性能が高く及びビード形状も優れていた。一方、実施例８８は、Ａｌ２Ｏ３、ＺｒＯ２、ＳｉＯ２及びＴｉＯ２の総含有量が少なかったため、ビード形状がやや不安定であった。また、実施例９２は、Ａｌ２Ｏ３、ＺｒＯ２、ＳｉＯ２及びＴｉＯ２の総含有量が多かったため、衝撃性能が４７Ｊ以上ではあったが、６０Ｊには届かなかった。 As shown in Table 28 above, Examples 89 to 91 using a flux-cored wire having a total content of Al 2 O 3 , ZrO 2 , SiO 2 and TiO 2 of 2 to 8% by mass are impacts of the weld metal. The performance was high and the bead shape was excellent. On the other hand, in Example 88, since the total content of Al 2 O 3 , ZrO 2 , SiO 2 and TiO 2 was small, the bead shape was slightly unstable. In Example 92, since the total content of Al 2 O 3 , ZrO 2 , SiO 2 and TiO 2 was large, the impact performance was 47 J or more, but it did not reach 60 J.

＜第１８実施例＞
第１８実施例では、Ｆｅ含有量が異なるフラックス入りワイヤを使用し、上記表１１に示す溶接条件で溶接を行い、溶接金属の衝撃性能及びビード形状を評価した。本実施例で用いた各フラックス入りワイヤのフラックス充填率、成分組成及びワイヤ強度を下記表２９に、評価結果を下記表３０に、それぞれ示す。なお、下記表２９及び表３０に示すＮｏ．９３〜９６のフラックス入りワイヤは、いずれも本発明の範囲内の実施例である。 <Eighteenth embodiment>
In 18th Example, the flux cored wire from which Fe content differs was used, and it welded on the welding conditions shown in the said Table 11, and evaluated the impact performance and bead shape of the weld metal. The flux filling rate, component composition, and wire strength of each flux-cored wire used in this example are shown in Table 29 below, and the evaluation results are shown in Table 30 below. In addition, No. shown in the following Table 29 and Table 30. 93 to 96 flux cored wires are all examples within the scope of the present invention.

上記表３０に示すように、Ｆｅ含有量が８６質量％以上のフラックス入りワイヤを用いた実施例９４〜９６は、溶接金属の衝撃性能が高く及びビード形状も優れていた。一方、実施例９３は、Ｆｅ含有量が少なかったため、溶着効率が低く、ビード形状は所定の要求を満足しているが、余裕がなかった。   As shown in Table 30 above, Examples 94 to 96 using a flux-cored wire with an Fe content of 86% by mass or more had high weld metal impact performance and an excellent bead shape. On the other hand, in Example 93, since the Fe content was small, the welding efficiency was low, and the bead shape satisfied a predetermined requirement, but there was no room.

＜第１９実施例＞
第１９実施例では、Ｍｎ／Ｓｉが異なるフラックス入りワイヤを使用し、上記表１１に示す溶接条件で溶接を行い、溶接金属の衝撃性能及びビード形状を評価した。本実施例で用いた各フラックス入りワイヤのフラックス充填率、成分組成及びワイヤ強度を下記表３１に、評価結果を下記表３２に、それぞれ示す。なお、下記表３１及び表３２に示すＮｏ．９７〜１０１のフラックス入りワイヤは、いずれも本発明の範囲内の実施例である。 <Nineteenth embodiment>
In the nineteenth example, flux-cored wires with different Mn / Si were used and welding was performed under the welding conditions shown in Table 11 above, and the impact performance and bead shape of the weld metal were evaluated. The flux filling rate, component composition, and wire strength of each flux-cored wire used in this example are shown in Table 31 below, and the evaluation results are shown in Table 32 below. In addition, No. shown in the following Table 31 and Table 32. 97-101 flux cored wires are all examples within the scope of the present invention.

上記表３２に示すように、Ｍｎ／Ｓｉが１．５〜５．５であるフラックス入りワイヤを用いた実施例９８〜１００は、溶接金属の衝撃性能が高く及びビード形状も優れていた。一方、実施例９７は、Ｍｎ／Ｓｉが低かったため、衝撃性能が４７Ｊ以上ではあったが、６０Ｊには届かなかった。また、実施例１０１は、Ｍｎ／Ｓｉが高かったため、ビードの形状がやや不安定であった。   As shown in Table 32 above, Examples 98 to 100 using flux-cored wires with Mn / Si of 1.5 to 5.5 had high weld metal impact performance and excellent bead shape. On the other hand, in Example 97, since Mn / Si was low, the impact performance was 47 J or more, but it did not reach 60 J. In Example 101, since Mn / Si was high, the bead shape was slightly unstable.

＜第２０実施例＞
第２０実施例では、Ｎｉ及びＭｏの添加量が異なるフラックス入りワイヤを使用し、上記表１１に示す溶接条件で溶接を行い、溶接金属の機械的性質及びビード形状を評価した。本実施例で用いた各フラックス入りワイヤのフラックス充填率、成分組成及びワイヤ強度を、下記表３３に示す。なお、下記表３３に示すＮｏ．１０２〜１０６のフラックス入りワイヤは、いずれも本発明の範囲内の実施例である。 <20th embodiment>
In the twentieth example, flux-cored wires having different amounts of Ni and Mo were used and welding was performed under the welding conditions shown in Table 11 above, and the mechanical properties and bead shape of the weld metal were evaluated. Table 33 below shows the flux filling rate, component composition, and wire strength of each flux-cored wire used in this example. In addition, No. shown in Table 33 below. The flux cored wires 102 to 106 are all examples within the scope of the present invention.

また、下記表３４に各フラックス入りワイヤの評価結果を示す。なお、下記表３４に示す溶接金属の機械的性質は、引張強度及び衝撃性能により評価し、引張強度が５９０ＭＰａ未満又は−４０℃における衝撃性能が４７Ｊ未満の場合は不良（×）、引張強度が５９０ＭＰａ以上かつ−４０℃における衝撃性能が４７Ｊ以上の場合を良好（○）、更に、引張強度が６２０〜６５０ＭＰａかつ−４０℃における衝撃性能が６０Ｊ以上の場合を優良（◎）とした。   Table 34 below shows the evaluation results of each flux-cored wire. The mechanical properties of the weld metal shown in Table 34 below are evaluated based on the tensile strength and impact performance. When the tensile strength is less than 590 MPa or the impact performance at −40 ° C. is less than 47 J, the defect (x) and the tensile strength are The case where the impact performance at 590 MPa or more and −40 ° C. was 47 J or more was good (◯), and the case where the tensile strength at 620 to 650 MPa and the impact performance at −40 ° C. was 60 J or more was judged excellent (◎).

上記表３４に示すように、Ｎｉ及びＭｏの総含有量が０．１〜３．０質量％であるフラックス入りワイヤを用いた実施例１０３〜１０５は、溶接金属の機械的性質及びビード形状共に優れていた。一方、実施例１０２は、Ｎｉ及びＭｏの総含有量が少なかったため、−４０℃における衝撃性能が４７Ｊ以上ではあったが、６０Ｊには届かなかった。また、実施例１０６は、Ｎｉ及びＭｏの総含有量が多かったため、引張強度が６５０ＭＰａを超えた。   As shown in Table 34 above, Examples 103 to 105 using flux-cored wires having a total content of Ni and Mo of 0.1 to 3.0% by mass are both mechanical properties and bead shapes of the weld metal. It was excellent. On the other hand, in Example 102, since the total content of Ni and Mo was small, the impact performance at −40 ° C. was 47 J or more, but it did not reach 60 J. In Example 106, since the total content of Ni and Mo was large, the tensile strength exceeded 650 MPa.

＜第２１実施例＞
第２１実施例では、ワイヤ強度が異なるフラックス入りワイヤを使用し、上記表１１に示す溶接条件で溶接を行い、ワイヤ送給性及びビード形状を評価した。本実施例で用いた各フラックス入りワイヤのフラックス充填率、成分組成及びワイヤ強度を下記表３５に、評価結果を下記表３６に、それぞれ示す。なお、下記表３５及び表３６に示すＮｏ．１０７〜１１１のフラックス入りワイヤは、いずれも本発明の範囲内の実施例である。 <Twenty-first embodiment>
In the twenty-first example, flux-cored wires having different wire strengths were used, welding was performed under the welding conditions shown in Table 11 above, and the wire feedability and bead shape were evaluated. The flux filling rate, component composition, and wire strength of each flux-cored wire used in this example are shown in Table 35 below, and the evaluation results are shown in Table 36 below. In addition, No. shown in Table 35 and Table 36 below. 107 to 111 flux cored wires are all examples within the scope of the present invention.

上記表３６に示すように、破断強度が３００〜９００ＭＰａであるフラックス入りワイヤを用いた実施例１０８〜１１０は、ワイヤ送給性及びビード形状共に優れていた。一方、実施例１０７は、ワイヤの破断強度が低くかったため、ワイヤがややスムーズに送給されず、ビード形状もやや不安定であった。実施例１１１は、ワイヤの破断強度が高過ぎて、ワイヤと送給ライナの摩擦抵抗が高くなり、ワイヤの送給性が極めて良好であるとまでは言えず、ビード形状もやや不安定であった。   As shown in Table 36 above, Examples 108 to 110 using flux-cored wires having break strengths of 300 to 900 MPa were excellent in both wire feedability and bead shape. On the other hand, in Example 107, since the breaking strength of the wire was low, the wire was not fed slightly smoothly and the bead shape was somewhat unstable. In Example 111, the breaking strength of the wire is too high, the frictional resistance between the wire and the feeding liner is high, the wire feeding property is not very good, and the bead shape is somewhat unstable. It was.

１ 下板
２ 立板
３ トーチ
４ 溶接ワイヤ
Ｄ ワイヤ径
Ｌ チップ母材間距離
θ 下板と立板とがなす角度
α 電極ワイヤの傾斜角度
β 下板の傾斜角度
γ 電極ワイヤと下板とがなす角度 DESCRIPTION OF SYMBOLS 1 Lower plate 2 Standing plate 3 Torch 4 Welding wire D Wire diameter L Distance between chip base materials θ Angle between lower plate and vertical plate α Inclination angle of electrode wire β Inclination angle of lower plate γ Electrode wire and lower plate Angle to make

Claims (5)

下板と立板とを片側すみ肉ガスシールドアーク溶接する方法であって、
水平方向に対して前記下板を傾けて、
電極ワイヤの直径Ｄを１．２〜１．６ｍｍ、
前記下板と前記立板とがなす角度θを９０〜１３０°、
溶接トーチの溶接方向における傾斜角度αを−１０〜２０°、
前記下板の水平方向に対する傾斜角度βを１０〜５０°、
前記溶接トーチと前記下板とがなす角度γを下記数式（Ａ）で示す範囲にして、
前記下板と前記立板とのすみ肉部を溶接するガスシールドアーク溶接方法。
（θ／２）−２０°≦γ≦９０°−β ・・・ （Ａ） A method in which a bottom plate and a vertical plate are welded on one side by fillet gas shield arc welding,
Tilt the lower plate with respect to the horizontal direction,
The diameter D of the electrode wire is 1.2 to 1.6 mm,
An angle θ formed by the lower plate and the standing plate is 90 to 130 °,
The inclination angle α in the welding direction of the welding torch is −10 to 20 °,
An inclination angle β with respect to the horizontal direction of the lower plate is 10 to 50 °,
In the range shown the angle γ of the lower plate and the welding torch is formed by the following equation (A), it
A gas shielded arc welding method for welding a fillet portion between the lower plate and the standing plate.
(Θ / 2) −20 ° ≦ γ ≦ 90 ° −β (A) 溶接速度を２００〜７００ｍｍ／分、
溶接電流を２００〜４５０Ａ、
アーク電圧を２０〜４５Ｖ、
チップ母材間距離を１５〜３５ｍｍ、
にする請求項１に記載のガスシールドアーク溶接方法。 Welding speed is 200 to 700 mm / min,
The welding current is 200 to 450 A,
Arc voltage 20-45V,
The distance between the chip base materials is 15 to 35 mm,
The gas shielded arc welding method according to claim 1. 前記電極ワイヤが鋼製外皮にフラックスが充填されたフラックス入りワイヤであり、
前記フラックス入りワイヤは、
前記フラックスの充填率が１０〜２０質量％であり、
ワイヤ全質量あたり、Ｃ：０．０１〜０．１０質量％、Ｓｉ：０．５〜１．５質量％、Ｍｎ：１．５〜３．５質量％、Ｍｇ及びＡｌのうち少なくとも１種：合計で０．１〜２．０質量％、ＴｉＯ２：１．５〜６．０質量％、Ｎａ化合物、Ｋ化合物及びＬｉ化合物のうち少なくとも１種の化合物：合計で０．０５〜０．４質量％、Ａｌ２Ｏ３、ＺｒＯ２及びＳｉＯ２のうち少なくとも１種の酸化物：ＴｉＯ２との合計で２〜８質量％、Ｆｅ：８６質量％以上を含有し、Ｍｎ含有量（質量％）とＳｉ含有量（質量％）との比（Ｍｎ／Ｓｉ）が１．５〜５．５である組成を有する、
請求項１又は２に記載のガスシールドアーク溶接方法。 The electrode wire is a flux-cored wire in which a steel outer sheath is filled with flux,
The flux-cored wire is
The flux filling rate is 10 to 20% by mass,
C: 0.01 to 0.10% by mass, Si: 0.5 to 1.5% by mass, Mn: 1.5 to 3.5% by mass, at least one of Mg and Al, based on the total mass of the wire: 0.1 to 2.0% by mass in total, TiO 2 : 1.5 to 6.0% by mass, at least one compound among Na compound, K compound and Li compound: 0.05 to 0.4 in total 2% to 8% by mass in total with at least one oxide of TiO 2 among mass%, Al 2 O 3 , ZrO 2 and SiO 2 , Fe: 86% by mass or more, Mn content (% by mass ) And the Si content (% by mass) (Mn / Si) has a composition of 1.5 to 5.5,
The gas shielded arc welding method according to claim 1 or 2. 前記フラックス入りワイヤは、更に、Ｎｉ及びＭｏのうち少なくとも１種の元素を、ワイヤ全質量あたり、合計で０．１〜３．０質量％含有する請求項３に記載のガスシールドアーク溶接方法。   4. The gas shielded arc welding method according to claim 3, wherein the flux-cored wire further contains at least one element of Ni and Mo in a total amount of 0.1 to 3.0 mass% per total mass of the wire. 前記電極ワイヤは、破断強度が３００〜９００ＭＰａである請求項１又は２に記載のガスシールドアーク溶接方法。   The gas shielded arc welding method according to claim 1, wherein the electrode wire has a breaking strength of 300 to 900 MPa.
JP2014197531A 2014-09-26 2014-09-26 Gas shield arc welding method Active JP6257489B2 (en)

Priority Applications (2)

Application Number Priority Date Filing Date Title
JP2014197531A JP6257489B2 (en) 2014-09-26 2014-09-26 Gas shield arc welding method
CN201510583561.3A CN105458465B (en) 2014-09-26 2015-09-14 Gas-shielded arc welding method

Applications Claiming Priority (1)

Application Number Priority Date Filing Date Title
JP2014197531A JP6257489B2 (en) 2014-09-26 2014-09-26 Gas shield arc welding method

Publications (2)

Publication Number Publication Date
JP2016068097A JP2016068097A (en) 2016-05-09
JP6257489B2 true JP6257489B2 (en) 2018-01-10

Family

ID=55596862

Family Applications (1)

Application Number Title Priority Date Filing Date
JP2014197531A Active JP6257489B2 (en) 2014-09-26 2014-09-26 Gas shield arc welding method

Country Status (2)

Country Link
JP (1) JP6257489B2 (en)
CN (1) CN105458465B (en)

Families Citing this family (3)

* Cited by examiner, † Cited by third party
Publication number Priority date Publication date Assignee Title
KR101798091B1 (en) * 2017-06-22 2017-11-15 김명기 Welding method having uniform bead
CN107598330B (en) * 2017-10-26 2020-05-01 上海振华重工(集团)股份有限公司 Full penetration welding method for U-shaped rib
CN113649725B (en) * 2021-09-27 2022-10-11 南京航空航天大学 Process method for improving fatigue performance of sheet steel GMAW electric arc welding butt joint

Family Cites Families (12)

* Cited by examiner, † Cited by third party
Publication number Priority date Publication date Assignee Title
JPS5080939A (en) * 1973-11-22 1975-07-01
JP3815600B2 (en) * 2001-09-07 2006-08-30 日鐵住金溶接工業株式会社 One side horizontal fillet gas shielded arc welding method
KR100774155B1 (en) * 2006-10-20 2007-11-07 고려용접봉 주식회사 Flux cored wire for duplex stainless steel and the manufacturing method thereof
JP5104037B2 (en) * 2007-05-24 2012-12-19 Ｊｆｅスチール株式会社 Fillet welding method and fillet welded joint
JP5014189B2 (en) * 2008-02-12 2012-08-29 日鐵住金溶接工業株式会社 Two-electrode fillet gas shielded arc welding method
JP5207933B2 (en) * 2008-11-21 2013-06-12 株式会社神戸製鋼所 Steel strip for flux cored wire with seam and method for manufacturing seamed flux cored wire
JP5103424B2 (en) * 2009-03-03 2012-12-19 日鐵住金溶接工業株式会社 One side horizontal fillet gas shielded arc welding method
CN102275026A (en) * 2010-06-08 2011-12-14 上海振华重工(集团)股份有限公司 Welding process for U-shaped rib of steel bridge panel
JP5325262B2 (en) * 2011-05-20 2013-10-23 三菱重工業株式会社 Welding method, welding apparatus and steel deck
CN102407397A (en) * 2011-09-15 2012-04-11 海波重型工程科技股份有限公司 Construction method for improving fatigue strength of welding joint of orthotropic steel bridge deck
CN102601498B (en) * 2012-03-13 2015-04-22 中铁宝桥集团有限公司 Welding method for U-shaped ribs of orthotropic plate of bridge girder
CN102861970A (en) * 2012-09-27 2013-01-09 中铁山桥集团有限公司 Welding method of orthotropic plate U-shaped rib fillet welding robot and special equipment thereof

Also Published As

Publication number Publication date
CN105458465B (en) 2017-08-25
CN105458465A (en) 2016-04-06
JP2016068097A (en) 2016-05-09

Similar Documents

Publication Publication Date Title
JP5205115B2 (en) MIG flux-cored wire for pure Ar shield gas welding and MIG arc welding method
US11136654B2 (en) Low-manganese gas-shielded flux cored welding electrodes
KR100920550B1 (en) Flux-cored wire for titania-based gas shielded arc welding
JP5005309B2 (en) Gas shielded arc welding flux cored wire for high strength steel
US10562134B2 (en) Flux-cored wire for gas-shielded arc welding
JP6399983B2 (en) Flux-cored wire for gas shielded arc welding
JP4209913B2 (en) Flux-cored wire for gas shielded arc welding
JP2009248137A (en) Flux cored wire for gas-shielded arc welding
JP2008290116A (en) Fillet welded joint and fillet welding method
JP6155810B2 (en) High Ni flux cored wire for gas shielded arc welding
JP5104037B2 (en) Fillet welding method and fillet welded joint
KR102115725B1 (en) Multi-electrode gas-shielded arc one-side welding method
JP6257489B2 (en) Gas shield arc welding method
WO2017013965A1 (en) Wire containing flux for gas shield arc welding
US10569369B2 (en) Wire containing flux for gas shield arc welding
WO2020012925A1 (en) Flux-cored wire for two-phase stainless steel welding, welding method and welding metal
KR102117815B1 (en) Multi-electrode gas-shielded arc one-side welding method
JP2019171473A (en) Flux-cored wire
JP6726008B2 (en) Flux-cored wire for gas shield arc welding
JP4260127B2 (en) Composite wire for submerged arc welding
JP5455422B2 (en) Low hydrogen coated arc welding rod
JP2020015092A (en) Flux-cored wire for welding two-phase stainless steel, welding method and weld metal
JPH09277088A (en) Flux cored wire for gas shielded metal-arc welding
JPH10180488A (en) Flux cored wire for electro gas arc welding
JP7063657B2 (en) Flux-filled wire for gas shielded arc welding

Legal Events

Date Code Title Description
RD04 Notification of resignation of power of attorney

Free format text: JAPANESE INTERMEDIATE CODE: A7424

Effective date: 20160209

A621 Written request for application examination

Free format text: JAPANESE INTERMEDIATE CODE: A621

Effective date: 20160901

A977 Report on retrieval

Free format text: JAPANESE INTERMEDIATE CODE: A971007

Effective date: 20170623

A131 Notification of reasons for refusal

Free format text: JAPANESE INTERMEDIATE CODE: A131

Effective date: 20170704

A521 Written amendment

Free format text: JAPANESE INTERMEDIATE CODE: A523

Effective date: 20170829

TRDD Decision of grant or rejection written
A01 Written decision to grant a patent or to grant a registration (utility model)

Free format text: JAPANESE INTERMEDIATE CODE: A01

Effective date: 20171114

A61 First payment of annual fees (during grant procedure)

Free format text: JAPANESE INTERMEDIATE CODE: A61

Effective date: 20171205

R150 Certificate of patent or registration of utility model

Ref document number: 6257489

Country of ref document: JP

Free format text: JAPANESE INTERMEDIATE CODE: R150