# Twin-Wire Pulsed Tandem Gas Metal Arc Welding of API X80 Steel Linepipe

Authors: Wenhao Wu; Ming Zhao; Haiyan Wang; Yanxia Zhang; Tong Wu
Journal: International Journal of Corrosion
 (2018)

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## Abstract

Twin-Wire Pulsed Tandem Gas Metal Arc Welding process with high welding production efficiency was used to join the girth weld seam of API X80 steel linepipe of 18.4 mm wall thickness and 1422 mm diameter. The macrostructure, microstructure, hardness, and electrochemical corrosion behavior of welded joints were studied. Effects of temperature and Cl− concentration on the corrosion behavior of base metal and weld metal were investigated. Results show that the welded joint has good morphology, mechanical properties, and corrosion resistance. The corrosion resistance of both the base metal and the weld metal decreases with increasing temperature or Cl− concentration. In the solution with high Cl− concentration, the base metal and weld metal are more susceptible to pitting. The corrosion resistance of the weld metal is slightly lower than that of the base metal.


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## Body

## 1. Introduction

At present, API X80 pipeline steel offering super high strength and high toughness is widely used in the petrochemical industry [1]. This steel is also used extensively in the pipeline construction of West-East Gas Pipeline Projects in China [2]. Welding is a key process of long-distance oil and gas pipeline construction, which utilizes up to ~20% of the total investment [3]. However, the recent increase in the strength of pipeline steel necessitates a thicker wall of pipeline, which results in poor weldability [4, 5]. Therefore, welding of the ultrahigh strength pipeline steel is becoming an intricate task and needs urgent attention.In the pipeline construction, high weld quality and high production efficiency are two essential requirements. However, these requirements are hardly fulfilled in the welding of girth weld seam of API X80 steel pipe using conventional gas metal arc welding (GMAW) process with single-wire and multilayer [6]. In GMAW, an increase in welding speed alone is unable to meet the required weld quality while an increase in heat input alone causes degradation of weld mechanical properties although it reduces the number of weld passes and increases the welding efficiency. Fortunately, the multiwire Pulsed Tandem Gas Metal Arc Welding (PT-GMAW) process has the potential to overcome the above problems while also meeting both aforesaid requirements [7–9]. Therefore, PT-GMAW is a candidate welding process for application in the pipeline construction.In practice, the welded linepipes are buried into soil for transporting oil or gas [10]. The pipeline in service encounters two different kinds of corrosive environments, the complex soil on the outer surface and the solution containing H2S, Cl−, HCO3-, and so on in the inner surface [11–13]. Published studies have shown that corrosion is one of the main causes of pipeline failure [14, 15]. Therefore, a welded pipeline is immediately subjected to anticorrosion treatment. It is well known that the corrosion resistance is the key factor to ensure the safe operation of long-distance oil and gas pipelines [16]. However, the microstructure and composition of the welded joints are severely inhomogeneous, and this inhomogeneity is coupled with the welding residual stress. Thus, the welded joint becomes the weakest part of the pipeline with respect to the corrosion resistance [17, 18]. Therefore, the study of welding technology and corrosion resistance of longitudinal or circumferential welds of high strength and high toughness steel pipelines is one of the current hotspots.In this study, twin-wire PT-GMAW of API X80 pipeline steel has been introduced. The quality and performance of welded linepipes are evaluated and optimized through analysis of macrostructure, microstructure, mechanical properties, and corrosion behavior of the base metal and weld metal. The effects of external soil temperature and concentration of internal corrosive solution on the corrosion behavior of the base metal and weld metal are explored. This work is expected to hold significant theoretical and practical importance in the petrochemical industry.


## 2. Materials and Methods

### 2.1. Welding Experiment

#### 2.1.1. Chemical Composition and Properties of API X80

API X80 steel linepipes, each with diameter 1422 mm and wall thickness 18.4 mm, were used in this welding experiment. The chemical compositions and mechanical properties of the above steel are given in Tables1 and 2, respectively.Table 1
Chemical compositions of API X80 (wt%).
C Mn Si P S Mo Ni Cr Cu V Nb Ti Fe 0.05 1.75 0.22 0.011 0.002 0.010 0.023 0.166 0.117 0.004 0.046 0.017 BalanceTable 2
Mechanical properties of API X80 (20°C).
Parameter Value Yield strengthRp0.2/MPa ≥550 Tensile strengthRm/MPa ≥620 ElongationA/% ≥20 Average absorbed energy CVN/J ≥70


#### 2.1.2. Groove of Girth Weld Seam

Two circular pipes were girth-welded together. Machining parameters of the double-V groove are shown in Figure1. The angles of the 1st and the 2nd V-grooves are ~60° and ~80°, respectively. In order to strike the welding arc easily and reduce the amount of deposited metal, the gap was made as narrow as possible.Figure 1
Schematic of the double-V groove (unit: mm).


#### 2.1.3. Welding Parameters

Twin-wire PT-GMAW was used to weld the API X80 steel line pipes. The welding setup consisted of two sets of wire feeding systems (one leading the other), two pulsed MIG 500 power sources, and a series of controlling equipment. The shielding gas, composed of 80% Argon and 20% CO2, was combined with a flux cored wire to generate the slag and gas protection. For this, a flux-cored wire AWS A 5.29 E81T8-Ni2 with diameter of 2.0 mm was used as the welding consumable. Welding parameters used in the process were optimized to improve the weld quality and are listed in Table 3. The welding process comprised five passes: one root pass, that is, the first layer of the girth weld seam, followed by one hot pass, that is, the second layer of the girth weld seam, and three subsequent passes, that is, 2 filler passes and 1 cap pass. The root pass and the hot pass were made by depositing the leading wire and trailing wire, respectively, while the other three passes were made by depositing two wires of the PT-GMAW. Preheating and interpass temperatures were strictly controlled in the range of 100°C~150°C.Table 3
Welding parameters.
Welding pass Welding currentI/A Arc voltageU/V Velocityv/m·min−1 Root 240 27 0.8 Hot 240 27 0.5 1st filler Leading wire 210 28 0.3 Trailing wire 190 30 2nd filler Leading wire 210 28 0.3 Trailing wire 190 30 Cap Leading wire 210 28 0.3 Trailing wire 190 30


### 2.2. Hardness Test

According to ASTM E92, the macro-Vickers hardness test was performed with a constant force of 10 kgf. The maximum deviation of the hardness measurements HV10 was ±3%. Details to the location of the tested paths are illustrated in Figure2.Figure 2
Schematic of tested paths for Vickers hardness.


### 2.3. Electrochemical Corrosion Test

#### 2.3.1. Corrosion Specimen

For electrochemical corrosion test, rectangular specimens were taken from both the weld metal and base metal. Each specimen was of dimensions (10 mm)L  ×  (10 mm)W  ×  (3 mm)T. Using a soldering iron, a somewhat oversized electrical copper wire was soldered onto the back of each specimen. Then, all the specimens were mounted on silica gel, grinded using emery papers, and polished to mirror finish. Finally, the polished specimens were cleaned with acetone and alcohol and dried with a hair dryer.


#### 2.3.2. Corrosion Solutions

Two types of solutions were used for the analysis of corrosion behavior of the welded linepipe because the interior and exterior surfaces of the linepipes experience two different types of corrosive environments. The corrosive solution used for the interior surface was an aqueous mixture of 0.5 mol Na2CO3 and 1 mol NaHCO3 with pH 9.4 while that for the exterior surface was a Korla soil simulated solution [19] with the compositions shown in Table 4 and pH 8.4 at room temperature. These solutions were prepared from pure chemical reagents and deionized water. For a given surface, that is, either interior or exterior, similar solution was used for the base metal and weld metal.Table 4
Composition of the Korla soil simulated solution (g/L).
NaHCO3 KCl Na2SO4 CaCl2 NaCl MgCl2·6H2O 0.1462 0.2156 2.5276 0.2442 3.1703 0.6699


#### 2.3.3. Test Equipment and Procedure

An electrochemical workstation comprising three electrodes was used as the corrosion test equipment. In this equipment, saturated calomel electrode and carbon rod were chosen as the reference and auxiliary electrodes, respectively, while the specimen was used as the working electrode. After stabilizing the open circuit potential of the setup, electrochemical impedance spectroscopy (EIS) and polarization (potentiodynamic scanning) experiments were conducted within a frequency range 10−2–105 Hz and scanning potential range −1.5–1.2 V. The scanning rate adopted was 1 mV/s in the higher-pH solution and 0.5 mV/s in the Korla soil simulated solution. Most of the corrosion tests were carried out at room temperature (20°C) except for those aimed to investigate the influence of temperature on the corrosion behavior. In the latter case, tests were carried out also at temperatures 40°C and 60°C. For each testing condition, at least 3 parallel tests were performed. All the measured values of the potential were relative to the saturated calomel electrode, and the test results were reproducible.


## 2.1. Welding Experiment

### 2.1.1. Chemical Composition and Properties of API X80

API X80 steel linepipes, each with diameter 1422 mm and wall thickness 18.4 mm, were used in this welding experiment. The chemical compositions and mechanical properties of the above steel are given in Tables1 and 2, respectively.Table 1
Chemical compositions of API X80 (wt%).
C Mn Si P S Mo Ni Cr Cu V Nb Ti Fe 0.05 1.75 0.22 0.011 0.002 0.010 0.023 0.166 0.117 0.004 0.046 0.017 BalanceTable 2
Mechanical properties of API X80 (20°C).
Parameter Value Yield strengthRp0.2/MPa ≥550 Tensile strengthRm/MPa ≥620 ElongationA/% ≥20 Average absorbed energy CVN/J ≥70


### 2.1.2. Groove of Girth Weld Seam

Two circular pipes were girth-welded together. Machining parameters of the double-V groove are shown in Figure1. The angles of the 1st and the 2nd V-grooves are ~60° and ~80°, respectively. In order to strike the welding arc easily and reduce the amount of deposited metal, the gap was made as narrow as possible.Figure 1
Schematic of the double-V groove (unit: mm).


### 2.1.3. Welding Parameters

Twin-wire PT-GMAW was used to weld the API X80 steel line pipes. The welding setup consisted of two sets of wire feeding systems (one leading the other), two pulsed MIG 500 power sources, and a series of controlling equipment. The shielding gas, composed of 80% Argon and 20% CO2, was combined with a flux cored wire to generate the slag and gas protection. For this, a flux-cored wire AWS A 5.29 E81T8-Ni2 with diameter of 2.0 mm was used as the welding consumable. Welding parameters used in the process were optimized to improve the weld quality and are listed in Table 3. The welding process comprised five passes: one root pass, that is, the first layer of the girth weld seam, followed by one hot pass, that is, the second layer of the girth weld seam, and three subsequent passes, that is, 2 filler passes and 1 cap pass. The root pass and the hot pass were made by depositing the leading wire and trailing wire, respectively, while the other three passes were made by depositing two wires of the PT-GMAW. Preheating and interpass temperatures were strictly controlled in the range of 100°C~150°C.Table 3
Welding parameters.
Welding pass Welding currentI/A Arc voltageU/V Velocityv/m·min−1 Root 240 27 0.8 Hot 240 27 0.5 1st filler Leading wire 210 28 0.3 Trailing wire 190 30 2nd filler Leading wire 210 28 0.3 Trailing wire 190 30 Cap Leading wire 210 28 0.3 Trailing wire 190 30


## 2.1.1. Chemical Composition and Properties of API X80

API X80 steel linepipes, each with diameter 1422 mm and wall thickness 18.4 mm, were used in this welding experiment. The chemical compositions and mechanical properties of the above steel are given in Tables1 and 2, respectively.Table 1
Chemical compositions of API X80 (wt%).
C Mn Si P S Mo Ni Cr Cu V Nb Ti Fe 0.05 1.75 0.22 0.011 0.002 0.010 0.023 0.166 0.117 0.004 0.046 0.017 BalanceTable 2
Mechanical properties of API X80 (20°C).
Parameter Value Yield strengthRp0.2/MPa ≥550 Tensile strengthRm/MPa ≥620 ElongationA/% ≥20 Average absorbed energy CVN/J ≥70


## 2.1.2. Groove of Girth Weld Seam

Two circular pipes were girth-welded together. Machining parameters of the double-V groove are shown in Figure1. The angles of the 1st and the 2nd V-grooves are ~60° and ~80°, respectively. In order to strike the welding arc easily and reduce the amount of deposited metal, the gap was made as narrow as possible.Figure 1
Schematic of the double-V groove (unit: mm).


## 2.1.3. Welding Parameters

Twin-wire PT-GMAW was used to weld the API X80 steel line pipes. The welding setup consisted of two sets of wire feeding systems (one leading the other), two pulsed MIG 500 power sources, and a series of controlling equipment. The shielding gas, composed of 80% Argon and 20% CO2, was combined with a flux cored wire to generate the slag and gas protection. For this, a flux-cored wire AWS A 5.29 E81T8-Ni2 with diameter of 2.0 mm was used as the welding consumable. Welding parameters used in the process were optimized to improve the weld quality and are listed in Table 3. The welding process comprised five passes: one root pass, that is, the first layer of the girth weld seam, followed by one hot pass, that is, the second layer of the girth weld seam, and three subsequent passes, that is, 2 filler passes and 1 cap pass. The root pass and the hot pass were made by depositing the leading wire and trailing wire, respectively, while the other three passes were made by depositing two wires of the PT-GMAW. Preheating and interpass temperatures were strictly controlled in the range of 100°C~150°C.Table 3
Welding parameters.
Welding pass Welding currentI/A Arc voltageU/V Velocityv/m·min−1 Root 240 27 0.8 Hot 240 27 0.5 1st filler Leading wire 210 28 0.3 Trailing wire 190 30 2nd filler Leading wire 210 28 0.3 Trailing wire 190 30 Cap Leading wire 210 28 0.3 Trailing wire 190 30


## 2.2. Hardness Test

According to ASTM E92, the macro-Vickers hardness test was performed with a constant force of 10 kgf. The maximum deviation of the hardness measurements HV10 was ±3%. Details to the location of the tested paths are illustrated in Figure2.Figure 2
Schematic of tested paths for Vickers hardness.


## 2.3. Electrochemical Corrosion Test

### 2.3.1. Corrosion Specimen

For electrochemical corrosion test, rectangular specimens were taken from both the weld metal and base metal. Each specimen was of dimensions (10 mm)L  ×  (10 mm)W  ×  (3 mm)T. Using a soldering iron, a somewhat oversized electrical copper wire was soldered onto the back of each specimen. Then, all the specimens were mounted on silica gel, grinded using emery papers, and polished to mirror finish. Finally, the polished specimens were cleaned with acetone and alcohol and dried with a hair dryer.


### 2.3.2. Corrosion Solutions

Two types of solutions were used for the analysis of corrosion behavior of the welded linepipe because the interior and exterior surfaces of the linepipes experience two different types of corrosive environments. The corrosive solution used for the interior surface was an aqueous mixture of 0.5 mol Na2CO3 and 1 mol NaHCO3 with pH 9.4 while that for the exterior surface was a Korla soil simulated solution [19] with the compositions shown in Table 4 and pH 8.4 at room temperature. These solutions were prepared from pure chemical reagents and deionized water. For a given surface, that is, either interior or exterior, similar solution was used for the base metal and weld metal.Table 4
Composition of the Korla soil simulated solution (g/L).
NaHCO3 KCl Na2SO4 CaCl2 NaCl MgCl2·6H2O 0.1462 0.2156 2.5276 0.2442 3.1703 0.6699


### 2.3.3. Test Equipment and Procedure

An electrochemical workstation comprising three electrodes was used as the corrosion test equipment. In this equipment, saturated calomel electrode and carbon rod were chosen as the reference and auxiliary electrodes, respectively, while the specimen was used as the working electrode. After stabilizing the open circuit potential of the setup, electrochemical impedance spectroscopy (EIS) and polarization (potentiodynamic scanning) experiments were conducted within a frequency range 10−2–105 Hz and scanning potential range −1.5–1.2 V. The scanning rate adopted was 1 mV/s in the higher-pH solution and 0.5 mV/s in the Korla soil simulated solution. Most of the corrosion tests were carried out at room temperature (20°C) except for those aimed to investigate the influence of temperature on the corrosion behavior. In the latter case, tests were carried out also at temperatures 40°C and 60°C. For each testing condition, at least 3 parallel tests were performed. All the measured values of the potential were relative to the saturated calomel electrode, and the test results were reproducible.


## 2.3.1. Corrosion Specimen

For electrochemical corrosion test, rectangular specimens were taken from both the weld metal and base metal. Each specimen was of dimensions (10 mm)L  ×  (10 mm)W  ×  (3 mm)T. Using a soldering iron, a somewhat oversized electrical copper wire was soldered onto the back of each specimen. Then, all the specimens were mounted on silica gel, grinded using emery papers, and polished to mirror finish. Finally, the polished specimens were cleaned with acetone and alcohol and dried with a hair dryer.


## 2.3.2. Corrosion Solutions

Two types of solutions were used for the analysis of corrosion behavior of the welded linepipe because the interior and exterior surfaces of the linepipes experience two different types of corrosive environments. The corrosive solution used for the interior surface was an aqueous mixture of 0.5 mol Na2CO3 and 1 mol NaHCO3 with pH 9.4 while that for the exterior surface was a Korla soil simulated solution [19] with the compositions shown in Table 4 and pH 8.4 at room temperature. These solutions were prepared from pure chemical reagents and deionized water. For a given surface, that is, either interior or exterior, similar solution was used for the base metal and weld metal.Table 4
Composition of the Korla soil simulated solution (g/L).
NaHCO3 KCl Na2SO4 CaCl2 NaCl MgCl2·6H2O 0.1462 0.2156 2.5276 0.2442 3.1703 0.6699


## 2.3.3. Test Equipment and Procedure

An electrochemical workstation comprising three electrodes was used as the corrosion test equipment. In this equipment, saturated calomel electrode and carbon rod were chosen as the reference and auxiliary electrodes, respectively, while the specimen was used as the working electrode. After stabilizing the open circuit potential of the setup, electrochemical impedance spectroscopy (EIS) and polarization (potentiodynamic scanning) experiments were conducted within a frequency range 10−2–105 Hz and scanning potential range −1.5–1.2 V. The scanning rate adopted was 1 mV/s in the higher-pH solution and 0.5 mV/s in the Korla soil simulated solution. Most of the corrosion tests were carried out at room temperature (20°C) except for those aimed to investigate the influence of temperature on the corrosion behavior. In the latter case, tests were carried out also at temperatures 40°C and 60°C. For each testing condition, at least 3 parallel tests were performed. All the measured values of the potential were relative to the saturated calomel electrode, and the test results were reproducible.


## 3. Results and Discussion

### 3.1. Weld Morphology

#### 3.1.1. Macrograph of Welded Joint

Macrograph of the twin-wire PT-GMA welded API X80 steel linepipe joint is shown in Figure3. It can be found that the double-V groove is filled completely by the five deposited layers. Comparing to the conventional welding process widely used in the West-East Gas Pipeline Project in China [6], Referred to Figure 4, it indicates that the welding efficiency of the girth weld seam has been improved significantly using the twin-wire PT-GMAW.Figure 3
Macrograph of the PT-GMAW joint with 5 layers.Figure 4
Macrograph of welding species of the combined girth-welded joint with 7 layers [6].


#### 3.1.2. Microstructure of Welded Joint

Microstructures of the base metal (BM), weld metal (WM), and heat affected zone (HAZ) are shown in Figure4a through c, respectively. The BM microstructure (Figure 5(a)) comprises acicular ferrite (AF) and polygonal ferrite (PF). Grains within the BM are very fine and uniformly distributed. The microstructure of WM (Figure 5(b)) also constitutes the AF and PF and refined grains although the refinement is relatively less as compared to that within the BM. In addition, a significant amount of grain interlocking can be observed within the WM. The grain interlocking is of great significance to ensure the performance of welded joint. The HAZ microstructure (Figure 5(c)) constitutes a large amount of granular bainites (GB), a relatively small amount of lath-shaped bainites (LB) and randomly distributed martensite-austenite constituents (M-A). The grains within the HAZ are much coarser than those in the BM and WM. These coarse grains give rise to higher microstructure inhomogeneity and, thus, may deteriorate the performance of the welded joint.Figure 5
Microstructure of welded joint within (a) BM (×500), (b) WM (×1000), and (c) HAZ (×1000).
(a) (b) (c)


### 3.2. Hardness of Welded Joint

Figures6(a)–6(d) show the macro-hardness profiles of the root pass, hot pass, filling layer, and cap layer, respectively. Almost on every studied layer, average value of macro-hardness is the minimum in the HAZ and varies in the following order: HAZ < WM < BM. The average macro-hardness in the BM is slightly higher than that in the WM because the grains within the BM are relatively fine and more uniformly distributed, as observed in Figure 5. The hardness of the cap layer is slightly lower than the other layers. The reason is that the former layer had been heat treated by the latter, making the microstructure of the previous layer better to improve its hardness.Figure 6
Macro hardness of welded joint within (a) root pass, (b) hot pass, (c) filling layer, and (d) cap layer.
(a) (b) (c) (d)


### 3.3. Corrosion Behavior of Welded Joint

#### 3.3.1. Analysis of Corrosion Resistance

The polarization curves and EIS results of the BM and WM in the high pH solution are shown in Figures7(a) and 7(b), respectively. It can be observed that both the BM and the WM are markedly passivated. From Figure 7(a), it is apparent that the self-corrosion current density and the corrosion potential of BM are 13.201 μA·cm−2 and −0.862 V, respectively, while those values for the WM are 16.657 μA·cm−2 and −0.877 V, respectively. Therefore, the WM has a more negative corrosion potential than the BM. This indicates that the WM is more likely to be corroded than the BM. That is to say, the corrosion resistance of WM is lower than that of BM in the high pH solution. Moreover, the capacitive reactance arcs of the WM and BM (Figure 7(b)) are located in the first quadrant. This observation suggests that the reaction resistance of the BM is higher than that of the WM. This further indicates that the corrosion rate of BM is lower than that of the WM in the high pH solution.Figure 7
Results of electrochemical corrosion test of BM and WM in the high pH solution. (a) Polarization curves and (b) EIS.
(a) (b)The results of EIS were fitted using the equivalent circuitRs(Qf(Rf(QdlRct)). In the circuit, Rs is the solution resistance, Qf is the capacitance of the corrosion product film, Rf is the resistance of the corrosion products at the electrode surface, Qdl is the double layer capacitance, and Rct is the polarization resistance. In general, the greater is the value of Rct, the harder is the feasibility of electrode reaction and, hence, the better is the corrosion resistance of the material [20]. Rct of the BM and the WM are 33380 Ω·cm2 and 10380 Ω·cm2, respectively. It can be seen that the polarization resistance of the WM is much smaller than that of the BM, which indicates that the charge on the WM is easier to transfer; that is, the corrosion resistance of the WM is poorer than the BM. This assertion is consistent with that obtained from the observations from the polarization curves in Figure 7(a).The polarization curves of the BM and WM in the Korla soil simulated solution, shown in Figure8(a), are similar to each other. No passivation phenomena can be observed at their anodes, and only the active zones are corroded. The self-corrosion current density and corrosion potential of the BM are 39.537 μA·cm−2 and −0.688 V, respectively, and those of the WM are 41.602 μA·cm−2 and −0.769 V, respectively. The marginal increase in the negative value of corrosion potential of BM indicates that its corrosion resistance is slightly higher than that of the WM in the Korla soil simulated solution.Figure 8
Results of electrochemical corrosion test of BM and WM in the Korla soil simulated solution. (a) Polarization curves and (b) EIS.
(a) (b)The results of EIS in Figure8(b) show that the capacitive reactance arc of the BM is greater than that of the WM. This indicates that BM exhibits a greater reaction resistance and, hence, a lower corrosion rate. The results of EIS were fitted with the equivalent circuit Rs(QdlRct) [21]. The fitted results are shown in Table 5. From the data in Table 5, it can be found that the charge transfer resistance of the BM is greater than that of the WM. Therefore, the corrosion resistance of BM is better than that of WM. This assertion is consistent with that obtained from the analysis of polarization curves.Table 5
Fitted results of EIS in the Korla soil simulated solution.
Solution resistanceRs (Ω·cm2) Double layer capacitanceQdl (Ω−1·cm−2·Sn) Diffusion indexndl Polarization resistanceRct (Ω·cm2) BM 19.29 4.9637 × 10 - 4 0.620 1524 WM 23.61 8.2786 × 10 - 4 0.754 766.4


#### 3.3.2. Influence of Temperature

The effect of temperature of the Korla soil simulated solution on the corrosion resistance of BM and WM is shown in Figures9(a) and 9(b), respectively. With increase in temperature, the polarization curves of both the BM and the WM have shifted downwards, indicating a decrease in the self-corrosion potential of BM and WM. In other words, the corrosion tendencies as well as the corrosion current densities of both the BM and the WM have increased. These are clear indications of increase in the corrosion rate. Therefore, it can be asserted that the corrosion resistance of the BM and the WM decreases with increasing temperature.Figure 9
Influence of temperature on the polarization curve of (a) BM and (b) WM.
(a) (b)Figure10 shows the results of EIS of BM and WM at different temperatures of the Korla soil simulated solution. An apparent decrease in the diameter of the capacitance arc can be observed with the increase in temperature. This indicates a decrease in the resistance of electrode to chemical reaction or an easier corrosion reaction because of a decrease in the corrosion resistance of both the BM and WM. Moreover, the corrosion resistance of the BM is found to be better than that of the WM at all the temperatures under consideration. The above observations are consistent with those from the polarization curves.Figure 10
Influence of temperature on EIS profiles of (a) BM and (b) WM.
(a) (b)


#### 3.3.3. Influence of Cl− Concentration

In order to study the effect of Cl− concentration on the corrosion resistance of BM and WM, 0.5 wt%, 1.5 wt%, 2.5 wt%, and 3.5 wt% NaCl solutions were added to the high pH solution. The polarization curves of BM and WM at 20°C are shown in Figure 11. No pitting has been found in the BM and WM with the addition of 0.5 wt% NaCl solution. However, with a further increase of Cl− concentration in the high pH solution, that is, with the addition of 1.5 to 3.5 wt% NaCl solutions, significant pitting of BM and WM has been observed, as evident in the macroscopic morphologies of BM and WM in Figure 12. From Figure 11, it is clear that both the pitting potential and the passivation potential decrease with increasing Cl− concentration. This indicates a relatively easy path for the formation and growth of pit on the surface or a higher susceptibility to pitting. It can be inferred that increase in Cl− concentration results in an increase in the corrosion current density and decrease in the corrosion potential and corrosion resistance of both BM and WM.Figure 11
Influence of Cl− concentration on polarization curves of (a) BM and (b) WM.
(a) (b)Figure 12
Macroscopic morphology of specimens of (a) BM and (b) WM, immersed in 3.5% NaCl solution for 7 days.
(a) (b)Figure13 shows the effect of Cl− concentration on the EIS of BM and WM. With the increase in Cl− concentration, the capacitance arc and the polarization resistance gradually decrease, indicating a gradual decrease in corrosion resistance. This result is consistent with those obtained from the polarization curve.Figure 13
Influence of Cl− concentration on EIS profiles of (a) BM and (b) WM.
(a) (b)


## 3.1. Weld Morphology

### 3.1.1. Macrograph of Welded Joint

Macrograph of the twin-wire PT-GMA welded API X80 steel linepipe joint is shown in Figure3. It can be found that the double-V groove is filled completely by the five deposited layers. Comparing to the conventional welding process widely used in the West-East Gas Pipeline Project in China [6], Referred to Figure 4, it indicates that the welding efficiency of the girth weld seam has been improved significantly using the twin-wire PT-GMAW.Figure 3
Macrograph of the PT-GMAW joint with 5 layers.Figure 4
Macrograph of welding species of the combined girth-welded joint with 7 layers [6].


### 3.1.2. Microstructure of Welded Joint

Microstructures of the base metal (BM), weld metal (WM), and heat affected zone (HAZ) are shown in Figure4a through c, respectively. The BM microstructure (Figure 5(a)) comprises acicular ferrite (AF) and polygonal ferrite (PF). Grains within the BM are very fine and uniformly distributed. The microstructure of WM (Figure 5(b)) also constitutes the AF and PF and refined grains although the refinement is relatively less as compared to that within the BM. In addition, a significant amount of grain interlocking can be observed within the WM. The grain interlocking is of great significance to ensure the performance of welded joint. The HAZ microstructure (Figure 5(c)) constitutes a large amount of granular bainites (GB), a relatively small amount of lath-shaped bainites (LB) and randomly distributed martensite-austenite constituents (M-A). The grains within the HAZ are much coarser than those in the BM and WM. These coarse grains give rise to higher microstructure inhomogeneity and, thus, may deteriorate the performance of the welded joint.Figure 5
Microstructure of welded joint within (a) BM (×500), (b) WM (×1000), and (c) HAZ (×1000).
(a) (b) (c)


## 3.1.1. Macrograph of Welded Joint

Macrograph of the twin-wire PT-GMA welded API X80 steel linepipe joint is shown in Figure3. It can be found that the double-V groove is filled completely by the five deposited layers. Comparing to the conventional welding process widely used in the West-East Gas Pipeline Project in China [6], Referred to Figure 4, it indicates that the welding efficiency of the girth weld seam has been improved significantly using the twin-wire PT-GMAW.Figure 3
Macrograph of the PT-GMAW joint with 5 layers.Figure 4
Macrograph of welding species of the combined girth-welded joint with 7 layers [6].


## 3.1.2. Microstructure of Welded Joint

Microstructures of the base metal (BM), weld metal (WM), and heat affected zone (HAZ) are shown in Figure4a through c, respectively. The BM microstructure (Figure 5(a)) comprises acicular ferrite (AF) and polygonal ferrite (PF). Grains within the BM are very fine and uniformly distributed. The microstructure of WM (Figure 5(b)) also constitutes the AF and PF and refined grains although the refinement is relatively less as compared to that within the BM. In addition, a significant amount of grain interlocking can be observed within the WM. The grain interlocking is of great significance to ensure the performance of welded joint. The HAZ microstructure (Figure 5(c)) constitutes a large amount of granular bainites (GB), a relatively small amount of lath-shaped bainites (LB) and randomly distributed martensite-austenite constituents (M-A). The grains within the HAZ are much coarser than those in the BM and WM. These coarse grains give rise to higher microstructure inhomogeneity and, thus, may deteriorate the performance of the welded joint.Figure 5
Microstructure of welded joint within (a) BM (×500), (b) WM (×1000), and (c) HAZ (×1000).
(a) (b) (c)


## 3.2. Hardness of Welded Joint

Figures6(a)–6(d) show the macro-hardness profiles of the root pass, hot pass, filling layer, and cap layer, respectively. Almost on every studied layer, average value of macro-hardness is the minimum in the HAZ and varies in the following order: HAZ < WM < BM. The average macro-hardness in the BM is slightly higher than that in the WM because the grains within the BM are relatively fine and more uniformly distributed, as observed in Figure 5. The hardness of the cap layer is slightly lower than the other layers. The reason is that the former layer had been heat treated by the latter, making the microstructure of the previous layer better to improve its hardness.Figure 6
Macro hardness of welded joint within (a) root pass, (b) hot pass, (c) filling layer, and (d) cap layer.
(a) (b) (c) (d)


## 3.3. Corrosion Behavior of Welded Joint

### 3.3.1. Analysis of Corrosion Resistance

The polarization curves and EIS results of the BM and WM in the high pH solution are shown in Figures7(a) and 7(b), respectively. It can be observed that both the BM and the WM are markedly passivated. From Figure 7(a), it is apparent that the self-corrosion current density and the corrosion potential of BM are 13.201 μA·cm−2 and −0.862 V, respectively, while those values for the WM are 16.657 μA·cm−2 and −0.877 V, respectively. Therefore, the WM has a more negative corrosion potential than the BM. This indicates that the WM is more likely to be corroded than the BM. That is to say, the corrosion resistance of WM is lower than that of BM in the high pH solution. Moreover, the capacitive reactance arcs of the WM and BM (Figure 7(b)) are located in the first quadrant. This observation suggests that the reaction resistance of the BM is higher than that of the WM. This further indicates that the corrosion rate of BM is lower than that of the WM in the high pH solution.Figure 7
Results of electrochemical corrosion test of BM and WM in the high pH solution. (a) Polarization curves and (b) EIS.
(a) (b)The results of EIS were fitted using the equivalent circuitRs(Qf(Rf(QdlRct)). In the circuit, Rs is the solution resistance, Qf is the capacitance of the corrosion product film, Rf is the resistance of the corrosion products at the electrode surface, Qdl is the double layer capacitance, and Rct is the polarization resistance. In general, the greater is the value of Rct, the harder is the feasibility of electrode reaction and, hence, the better is the corrosion resistance of the material [20]. Rct of the BM and the WM are 33380 Ω·cm2 and 10380 Ω·cm2, respectively. It can be seen that the polarization resistance of the WM is much smaller than that of the BM, which indicates that the charge on the WM is easier to transfer; that is, the corrosion resistance of the WM is poorer than the BM. This assertion is consistent with that obtained from the observations from the polarization curves in Figure 7(a).The polarization curves of the BM and WM in the Korla soil simulated solution, shown in Figure8(a), are similar to each other. No passivation phenomena can be observed at their anodes, and only the active zones are corroded. The self-corrosion current density and corrosion potential of the BM are 39.537 μA·cm−2 and −0.688 V, respectively, and those of the WM are 41.602 μA·cm−2 and −0.769 V, respectively. The marginal increase in the negative value of corrosion potential of BM indicates that its corrosion resistance is slightly higher than that of the WM in the Korla soil simulated solution.Figure 8
Results of electrochemical corrosion test of BM and WM in the Korla soil simulated solution. (a) Polarization curves and (b) EIS.
(a) (b)The results of EIS in Figure8(b) show that the capacitive reactance arc of the BM is greater than that of the WM. This indicates that BM exhibits a greater reaction resistance and, hence, a lower corrosion rate. The results of EIS were fitted with the equivalent circuit Rs(QdlRct) [21]. The fitted results are shown in Table 5. From the data in Table 5, it can be found that the charge transfer resistance of the BM is greater than that of the WM. Therefore, the corrosion resistance of BM is better than that of WM. This assertion is consistent with that obtained from the analysis of polarization curves.Table 5
Fitted results of EIS in the Korla soil simulated solution.
Solution resistanceRs (Ω·cm2) Double layer capacitanceQdl (Ω−1·cm−2·Sn) Diffusion indexndl Polarization resistanceRct (Ω·cm2) BM 19.29 4.9637 × 10 - 4 0.620 1524 WM 23.61 8.2786 × 10 - 4 0.754 766.4


### 3.3.2. Influence of Temperature

The effect of temperature of the Korla soil simulated solution on the corrosion resistance of BM and WM is shown in Figures9(a) and 9(b), respectively. With increase in temperature, the polarization curves of both the BM and the WM have shifted downwards, indicating a decrease in the self-corrosion potential of BM and WM. In other words, the corrosion tendencies as well as the corrosion current densities of both the BM and the WM have increased. These are clear indications of increase in the corrosion rate. Therefore, it can be asserted that the corrosion resistance of the BM and the WM decreases with increasing temperature.Figure 9
Influence of temperature on the polarization curve of (a) BM and (b) WM.
(a) (b)Figure10 shows the results of EIS of BM and WM at different temperatures of the Korla soil simulated solution. An apparent decrease in the diameter of the capacitance arc can be observed with the increase in temperature. This indicates a decrease in the resistance of electrode to chemical reaction or an easier corrosion reaction because of a decrease in the corrosion resistance of both the BM and WM. Moreover, the corrosion resistance of the BM is found to be better than that of the WM at all the temperatures under consideration. The above observations are consistent with those from the polarization curves.Figure 10
Influence of temperature on EIS profiles of (a) BM and (b) WM.
(a) (b)


### 3.3.3. Influence of Cl− Concentration

In order to study the effect of Cl− concentration on the corrosion resistance of BM and WM, 0.5 wt%, 1.5 wt%, 2.5 wt%, and 3.5 wt% NaCl solutions were added to the high pH solution. The polarization curves of BM and WM at 20°C are shown in Figure 11. No pitting has been found in the BM and WM with the addition of 0.5 wt% NaCl solution. However, with a further increase of Cl− concentration in the high pH solution, that is, with the addition of 1.5 to 3.5 wt% NaCl solutions, significant pitting of BM and WM has been observed, as evident in the macroscopic morphologies of BM and WM in Figure 12. From Figure 11, it is clear that both the pitting potential and the passivation potential decrease with increasing Cl− concentration. This indicates a relatively easy path for the formation and growth of pit on the surface or a higher susceptibility to pitting. It can be inferred that increase in Cl− concentration results in an increase in the corrosion current density and decrease in the corrosion potential and corrosion resistance of both BM and WM.Figure 11
Influence of Cl− concentration on polarization curves of (a) BM and (b) WM.
(a) (b)Figure 12
Macroscopic morphology of specimens of (a) BM and (b) WM, immersed in 3.5% NaCl solution for 7 days.
(a) (b)Figure13 shows the effect of Cl− concentration on the EIS of BM and WM. With the increase in Cl− concentration, the capacitance arc and the polarization resistance gradually decrease, indicating a gradual decrease in corrosion resistance. This result is consistent with those obtained from the polarization curve.Figure 13
Influence of Cl− concentration on EIS profiles of (a) BM and (b) WM.
(a) (b)


## 3.3.1. Analysis of Corrosion Resistance

The polarization curves and EIS results of the BM and WM in the high pH solution are shown in Figures7(a) and 7(b), respectively. It can be observed that both the BM and the WM are markedly passivated. From Figure 7(a), it is apparent that the self-corrosion current density and the corrosion potential of BM are 13.201 μA·cm−2 and −0.862 V, respectively, while those values for the WM are 16.657 μA·cm−2 and −0.877 V, respectively. Therefore, the WM has a more negative corrosion potential than the BM. This indicates that the WM is more likely to be corroded than the BM. That is to say, the corrosion resistance of WM is lower than that of BM in the high pH solution. Moreover, the capacitive reactance arcs of the WM and BM (Figure 7(b)) are located in the first quadrant. This observation suggests that the reaction resistance of the BM is higher than that of the WM. This further indicates that the corrosion rate of BM is lower than that of the WM in the high pH solution.Figure 7
Results of electrochemical corrosion test of BM and WM in the high pH solution. (a) Polarization curves and (b) EIS.
(a) (b)The results of EIS were fitted using the equivalent circuitRs(Qf(Rf(QdlRct)). In the circuit, Rs is the solution resistance, Qf is the capacitance of the corrosion product film, Rf is the resistance of the corrosion products at the electrode surface, Qdl is the double layer capacitance, and Rct is the polarization resistance. In general, the greater is the value of Rct, the harder is the feasibility of electrode reaction and, hence, the better is the corrosion resistance of the material [20]. Rct of the BM and the WM are 33380 Ω·cm2 and 10380 Ω·cm2, respectively. It can be seen that the polarization resistance of the WM is much smaller than that of the BM, which indicates that the charge on the WM is easier to transfer; that is, the corrosion resistance of the WM is poorer than the BM. This assertion is consistent with that obtained from the observations from the polarization curves in Figure 7(a).The polarization curves of the BM and WM in the Korla soil simulated solution, shown in Figure8(a), are similar to each other. No passivation phenomena can be observed at their anodes, and only the active zones are corroded. The self-corrosion current density and corrosion potential of the BM are 39.537 μA·cm−2 and −0.688 V, respectively, and those of the WM are 41.602 μA·cm−2 and −0.769 V, respectively. The marginal increase in the negative value of corrosion potential of BM indicates that its corrosion resistance is slightly higher than that of the WM in the Korla soil simulated solution.Figure 8
Results of electrochemical corrosion test of BM and WM in the Korla soil simulated solution. (a) Polarization curves and (b) EIS.
(a) (b)The results of EIS in Figure8(b) show that the capacitive reactance arc of the BM is greater than that of the WM. This indicates that BM exhibits a greater reaction resistance and, hence, a lower corrosion rate. The results of EIS were fitted with the equivalent circuit Rs(QdlRct) [21]. The fitted results are shown in Table 5. From the data in Table 5, it can be found that the charge transfer resistance of the BM is greater than that of the WM. Therefore, the corrosion resistance of BM is better than that of WM. This assertion is consistent with that obtained from the analysis of polarization curves.Table 5
Fitted results of EIS in the Korla soil simulated solution.
Solution resistanceRs (Ω·cm2) Double layer capacitanceQdl (Ω−1·cm−2·Sn) Diffusion indexndl Polarization resistanceRct (Ω·cm2) BM 19.29 4.9637 × 10 - 4 0.620 1524 WM 23.61 8.2786 × 10 - 4 0.754 766.4


## 3.3.2. Influence of Temperature

The effect of temperature of the Korla soil simulated solution on the corrosion resistance of BM and WM is shown in Figures9(a) and 9(b), respectively. With increase in temperature, the polarization curves of both the BM and the WM have shifted downwards, indicating a decrease in the self-corrosion potential of BM and WM. In other words, the corrosion tendencies as well as the corrosion current densities of both the BM and the WM have increased. These are clear indications of increase in the corrosion rate. Therefore, it can be asserted that the corrosion resistance of the BM and the WM decreases with increasing temperature.Figure 9
Influence of temperature on the polarization curve of (a) BM and (b) WM.
(a) (b)Figure10 shows the results of EIS of BM and WM at different temperatures of the Korla soil simulated solution. An apparent decrease in the diameter of the capacitance arc can be observed with the increase in temperature. This indicates a decrease in the resistance of electrode to chemical reaction or an easier corrosion reaction because of a decrease in the corrosion resistance of both the BM and WM. Moreover, the corrosion resistance of the BM is found to be better than that of the WM at all the temperatures under consideration. The above observations are consistent with those from the polarization curves.Figure 10
Influence of temperature on EIS profiles of (a) BM and (b) WM.
(a) (b)


## 3.3.3. Influence of Cl− Concentration

In order to study the effect of Cl− concentration on the corrosion resistance of BM and WM, 0.5 wt%, 1.5 wt%, 2.5 wt%, and 3.5 wt% NaCl solutions were added to the high pH solution. The polarization curves of BM and WM at 20°C are shown in Figure 11. No pitting has been found in the BM and WM with the addition of 0.5 wt% NaCl solution. However, with a further increase of Cl− concentration in the high pH solution, that is, with the addition of 1.5 to 3.5 wt% NaCl solutions, significant pitting of BM and WM has been observed, as evident in the macroscopic morphologies of BM and WM in Figure 12. From Figure 11, it is clear that both the pitting potential and the passivation potential decrease with increasing Cl− concentration. This indicates a relatively easy path for the formation and growth of pit on the surface or a higher susceptibility to pitting. It can be inferred that increase in Cl− concentration results in an increase in the corrosion current density and decrease in the corrosion potential and corrosion resistance of both BM and WM.Figure 11
Influence of Cl− concentration on polarization curves of (a) BM and (b) WM.
(a) (b)Figure 12
Macroscopic morphology of specimens of (a) BM and (b) WM, immersed in 3.5% NaCl solution for 7 days.
(a) (b)Figure13 shows the effect of Cl− concentration on the EIS of BM and WM. With the increase in Cl− concentration, the capacitance arc and the polarization resistance gradually decrease, indicating a gradual decrease in corrosion resistance. This result is consistent with those obtained from the polarization curve.Figure 13
Influence of Cl− concentration on EIS profiles of (a) BM and (b) WM.
(a) (b)


## 4. Conclusions

(1) Welding of girth weld seam of API X80 steel linepipe with thick wall and large diameter has been conducted successfully using the twin-wire PT-GMAW process. The achieved high welding efficiency makes this process an appropriate choice for the welding of the above structure.(2) With optimized welding parameters, the welded joint exhibits good morphology, mechanical properties, and corrosion resistance. Irrespective of the type of corrosive environment, the corrosion resistance of weld metal is slightly lower than that of the base metal at both the inner and outer surfaces of the API X80 steel linepipe.(3) The corrosion resistance of the base metal and the weld metal is decreased with the increase in temperature or Cl− concentration.



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*Source: 7284246-2018-03-11.xml*