Influence of Nitrogen Content on the Corrosion Behavior of Powder Metallurgy Nickel-Free Austenitic Stainless Steel

Yu, Weili; Du, Changhai; Shen, Hongren; He, Hao; Yu, Yong; Li, Yimin; Luo, Fenghua

doi:https://doi.org/10.1155/2021/7808070

Advances in Materials Science and Engineering

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Research Article | Open Access

Volume 2021 | Article ID 7808070 | https://doi.org/10.1155/2021/7808070

Influence of Nitrogen Content on the Corrosion Behavior of Powder Metallurgy Nickel-Free Austenitic Stainless Steel

Weili Yu,¹Changhai Du,¹Hongren Shen,¹Hao He,²Yong Yu,³Yimin Li,¹and Fenghua Luo¹

Academic Editor: Antonio Riveiro

Received05 Aug 2021

Accepted05 Oct 2021

Published14 Oct 2021

Abstract

Herein, powder metallurgy gas-solid nitriding was used to prepare a high-nitrogen Ni-free austenitic stainless steel with more than 1.0 wt.% N. Study of the microstructures and corrosion resistances of the as-prepared samples revealed that the corrosion weight loss, size, number of corrosion pits, and corrosion depth decreased as the N content increased from 1.19 to 1.37 wt.%. The self-corrosion current densities of the alloys were determined from their potentiodynamic polarization curves. The changes in the capacitive arc radius as demonstrated by the Nyquist curves were consistent with the conclusions of the immersion corrosion analysis; that is, a high N content leads to a high corrosion resistance.

1. Introduction

Owing to its excellent comprehensive performance, high-N Ni-free austenitic stainless steel (HNNS) has a wide range of applications, such as medicine, shipbuilding, petroleum, nuclear power, and automobile industries [1]. Compared with Cr-Ni austenitic stainless steel, HNNS contains high Mn and N contents and an extremely low Ni content [2]. SS304 does not contain Mo and is prone to pitting corrosion in an environment with Cl. Meanwhile, SS316 contains Mo, which increases the compactness and adhesion strength of the passivation film, thereby effectively improving the corrosion resistance against Cl ions. However, the content of Ni, which is more expensive than Mn and N, in SS304 (8–10.5%) is lower than that in SS316 (10–14%). Thus, the cost of HNNS is lower than that of Ni-containing stainless steel. Furthermore, with N as the austenite phase-forming element of stainless steel, its addition can improve the mechanical properties and corrosion resistance of stainless steel. N can also stabilize the austenite phase and significantly improve the mechanical properties and corrosion resistance of stainless steel [3, 4]. HNNS avoids potential problems related to Ni allergy [5–7].

The main methods of preparing HNNS are high-pressure N₂ gas smelting [8–10] and atmospheric pressure smelting [2, 11]. However, both these methods have their disadvantages. For instance, high-pressure gas atomization in the high-pressure smelting method uses high-pressure N₂ as the atomizing gas to atomize the melt into powder [9]. Rapid solidification can ensure that N₂ in the molten metal will not precipitate during the quenching process. In addition, this considerably increases the N content in the steel powder and can prepare high-N steel (>1.0 wt.%) [9]; however, this also poses issues, such as high-pressure N₂ safety hazards [9], high cost [12], use of complex equipment [13], and difficult operation [14]. Meanwhile, in the atmospheric smelting method, solid powder nitriding can be used to complete the nitriding of the solid powder at low pressures and temperatures [11]. The solubility of N in the austenite phase with a high Cr content is significantly higher than that in the liquid phase; therefore, solid powder nitriding can avoid defects, such as uneven N content and pore formation in the general casting and production of high-N steel. In addition, the atmospheric pressure smelting method has the advantages of low cost [8] and low risk [15]. However, only medium-to-low-N smelted stainless steel with a low N content can be achieved by this method [16].

The N content in stainless steel has solid-solution strengthening effects, which can accelerate the repassivation of the metal surface and effectively inhibit local corrosion in an environment containing Cl⁻, such as seawater [17–20]. Ahila et al. [17] showed that a considerable number of N atoms aggregates at the boundary between the metal and passivation film. N₂ can effectively induce the reformation of the passivation film, thereby inhibiting the occurrence of pitting corrosion. The pitting resistance of HNNS can be measured by the pitting resistance equivalent numbers (PRENs, PREN = wt.% [Cr] + 3.3 wt.% [Mo] + 30 wt.% [N]) [18]. When the material has a high proportion of N, its PREN is higher, and its pitting resistance is stronger. Simultaneously, the addition of N hinders the nucleation and growth of Cr-rich carbides, thereby preventing the reduction of Cr content in the grain boundaries and improving the resistance of stainless steel to intergranular corrosion [21, 22]. N can enhance the anticorrosion effects of Cr and Mo to form a layer on the steel surface that is more resistant to local corrosion, inhibit the excessive passivation of the steel surface, and slow down the dissolution of Cr, Mo, and other elements of austenitic stainless steel [23].

Several studies have reported [24, 25] the influence of N content on the corrosion resistance of stainless steel. Austenitic stainless steels with N contents of 0.14 and 0.19 wt.% were prepared using a high N₂ gas pressure melting method, and they exhibited corrosion rates of 1.86 × 10⁻⁵ and 1.57 × 10⁻⁵ g mm⁻² h⁻¹, respectively, in a 6% FeCl₃ solution (25 ± 1°C, 144 h). This indicates that a low corrosion rate, which corresponds to a high N content, leads to a high corrosion resistance [24]. Exfoliation corrosion experiments were conducted in a previous study using the sulfuric acid-flow Fe method [25]. Austenitic stainless steels with N contents of 0.59 and 0.31 wt.% were immersed in a 6.8 mol L⁻¹ H₂SO₄ + 0.1 mol L⁻¹ Fe₂(SO₄) solution (25°C, 24 h). After immersion, several corrosion grooves appeared along the grain boundary on the surface of austenitic stainless steel with 0.31 wt.% N. The grooves stretched deeply into the matrix, which resulted in the grains peeling off the matrix body significantly. Under the same conditions, only a few particles peeled off the surface of austenitic stainless steel with 0.59 wt.% N. Hence, N improved the exfoliation corrosion resistance of stainless steel.

Ni plating on the surface of stainless steel can improve its surface conditions and resist the entry of Cl⁻, thereby improving its corrosion resistance, expanding its scope of application, and prolonging its service life. However, compared with the conventional stainless steel Ni coating, there are several limitations to the application of Ni plating to HNNS for improving the corrosion resistance. The matrix surface of HNNS is prone to defects, such as inclusions and dislocations. These defects alter the uniformity, increase the fragility of the passivation film, and increase the inflow of the Cl⁻ ions through the defects, thereby damaging the passivation film.

Few studies have evaluated the effects of N contents higher than 1.0 wt.% on the corrosion resistance of Ni-free austenitic stainless steels. In this study, gas-solid nitriding and powder metallurgy were used to prepare HNNS with higher density and N content (>1.0 wt.%) than those of N austenitic stainless steel obtained by high N₂ gas pressure melting. The effects of the difference in N contents on the microstructure and corrosion resistance of HNNS were examined. The corrosion mechanism was analyzed based on uniform and pitting corrosion.

2. Materials and Methods

In this study, 0Cr17Mn11Mo3N grade stainless steel powder provided by Hunan Hengji Powder Technology Co., Ltd. was used. Its chemical composition is shown in Table 1, and the powder morphology is shown in Figure 1.

The stainless steel powder was mixed with a binder (paraffin wax) and cold mold pressing was performed at 400 MPa. The sample size was 11 mm × 8 mm × 2.8 mm. Nitriding and sintering were performed in a low-pressure sintering furnace (SJL-200L, Shanghai Jujing Precision Instrument Manufacturing Co., Ltd.). The temperature was increased to 600°C with an initial vacuum pressure of less than 0.1 Pa. Thereafter, the temperature was maintained at 600°C for 1 h. Under a constant temperature, the N₂ gas pressure was increased to 20 kPa. Subsequently, the temperature was increased to 1280°C at a rate of 3°C·min⁻¹, and the N₂ gas pressure was simultaneously increased to 80 kPa. The temperature and N₂ gas pressure were then maintained for 2 h during the completion of the nitriding treatment. After the nitriding treatment, the furnace was cooled to 1100°C. Vacuum denitrification was then performed at 1100°C, and the temperature was sustained for different lengths of time to provide steels with different N contents. The vacuum denitrification treatment times were 1, 2, and 3 h under a vacuum pressure of less than 0.1 Pa. The three sintered steels were then cooled to below 100°C inside the furnace.

The three sintered steels underwent solid-solution treatment in a quartz tube furnace (SG-GS1700, Shanghai Shinbae Industrial Co., Ltd.) at 1200°C for 2 h under an Ar gas atmosphere. Following the completion of the temperature holding time, the quartz tube was clamped, broken immediately, and quenched in water. A wire-cut electric discharge machine (TZT27-DK7725, POSITTEC) was used to cut along the longitudinal section of the sintered steel to obtain a sample with a width of 1 mm. All parts of the sintered steels were powdered after cleaning the surface oxide layer. The N contents of the sintered steels were determined from the aforementioned powders using an O₂, N₂, and H₂ analyzer (TCH-600, LECO). The N contents of the steels subjected to denitrification treatment for 1, 2, and 3 h were measured to be 1.19, 1.28, and 1.37 wt.%, respectively.

X-ray diffraction (XRD; D8 Advance, Bruker) was used to determine the phase composition of the sintered alloy denitrified at 1100°C for 2 h and those of the three solid-solution alloys with different N contents. The sample used for the test was a block with dimensions of 11 mm × 2.8 mm × 2 mm. The following parameters were used for the analysis: step length = 0.02°, dwell time = 6 s, and scanning angle = 30–85°. The sample position and measured area were moved immediately below the light barrier.

The material test sample was cut using wire-cut electrical discharge machining. The sample was then polished with sandpaper (320#, 600#, 800#, 1000#, 1200#, and 2000#) and was subjected to metallographic polishing (2.5, 1.5, and 0.5 μm) until a mirror-like and scratch-free surface was achieved. An aqueous solution of FeCl₂ and HCl acid was used as the etching agent (concentration ratio: 5 g FeCl₃ + 50 mL HCl + 100 mL H₂O). Depending on the state of the sample, the corrosion time was varied from 5 to 60 s. An optical microscope (DM2700 M, Leica) was used to observe and analyze the corroded samples.

A uniform corrosion experiment was conducted in accordance with the GB/T 17897–2016 standard using 100 g analytical pure iron trichloride (FeCl₃·6H₂O), which meets the requirements of HG/T 3474. FeCl₃·6H₂O was dissolved in 900 mL distilled water and a 6% FeCl₃ soaking solution was prepared. The sample was polished step-by-step with 320#−2000# sandpaper. Before soaking, the sample was ultrasonically cleaned with distilled water, acetone, and anhydrous alcohol and dried. The 6% FeCl₃ solution was used for soaking. The ratio of the sample surface area to volume of the soaking solution was 1 cm²:20 mL, the soaking temperature was 55 ± 1°C, and the soaking time was 72 h. Following the immersion, a solution of 50 mL HNO₃ + 100 mL HF + 350 mL H₂O was used at 25°C to heat the sample for 10 min to remove the corrosion products deposited on its surface. Then, ultrasonic cleaning was continued with absolute ethanol for 10 min. The sample was subsequently dried at 60°C for 8 h. The mass of the sample before and after immersion was weighed using an analytical balance (AE124, Sunny Hengping) with a precision reading of 0.1 mg. The corrosion rate of the sample was calculated according to the following equation:where W_front is the mass of the sample before soaking (g), W_rear is the mass of the sample after soaking (g), S is the surface area of the sample before soaking (mm²), and t is the soaking time (h).

For the electrochemical experiment, CHI750 electrochemical workstation was used (Shanghai Chenhua Instrument Co., Ltd.). The electrochemical test sample (working electrode) was sealed with epoxy resin to achieve an exposed area of 0.25 cm². Before the test, the sample was polished and washed with deionized water. The electrochemical test was carried out using a three-electrode system with a Pt electrode as the auxiliary electrode and a saturated calomel electrode (SCE) as the reference electrode. The potentials used in this study were relative to the reference electrode. After soaking the working electrode for 3 min, an electrochemical impedance spectroscopy (EIS) test was performed. The electrochemical test solution was a 3.5 mass% NaCl solution saturated at room temperature. The scanning rate of the polarization curve was 0.002 mV s⁻¹, and the corrosion potential and corrosion current density of the sample were estimated using the Tafel extrapolation method. The EIS measurement frequency range was 10⁵–10⁻² Hz. The equivalent circuit in ZSimpWin software was selected to fit the impedance data to obtain the relevant charge transfer resistance and other parameters.

The corrosion morphology of the sample surface was observed and analyzed using scanning electron microscopy (FEG 250, Quanta). After immersion and corrosion, the sample was ground according to the metallographic sample preparation method, and the corrosion depth of the sample was directly analyzed using an optical microscope.

3. Results

Figure 2 shows the metallographic structure and XRD pattern of the sintered alloy denitrified at 1100°C for 2 h. Figure 2(a) shows that the sintered alloy was divided into three layers from the surface toward the center. The inner layer had single equiaxed grains; the middle layer had the structure of a grain boundary network or granular precipitated phases; and the outermost layer had several lamellar structures similar to pearlite colonies (ferrite/cementite lamellar) [26, 27]. Cr₂N and CrN peaks were observed in the XRD pattern shown in Figure 2(b), suggesting that the precipitates in Figure 2(a) were Cr₂N and CrN [28, 29]. Cr₂N commonly forms in stainless steel with high N content through discontinuous solubilization [30]. Therefore, during the nitriding and sintering processes, the surface layer of the sintered alloy had a relatively high N content. First, Cr₂N and CrN discontinuously precipitated along the grain boundaries, grew into grains, and precipitated in a cellular shape, which was then arranged in a parallel lamellar shape that covered the entire grain. The N content of the intermediate layer was reduced, and Cr₂N and CrN were discontinuously precipitated in the form of short rods at the grain boundaries. There is insufficient N content in the sintered body because of Cr₂N precipitation. The nitriding and sintering processes employed in this study resulted in a structure with inhomogeneous N distribution. Hence, solution treatment was required to impart homogeneity to the alloy microstructure.

(a)

(b)

Figure 3 shows the metallographic structure and XRD pattern of the alloy after the solution treatment at 1200°C. The N content of the three alloys shown in Figure 3 was determined to be 1.19, 1.28, and 1.37 wt.%. After the solution treatment, the samples with different N contents were identified to be austenite with relatively straight grain boundaries. There were no differences observed in their grain sizes or nitride precipitation on their grain boundaries; however, a small number of twins and pores were found. The sample with 1.19 wt.% N had the smallest number of pores (25) and smallest pores among the three samples (Figure 3(a)). The pore sizes of the sample with 1.28 wt.% N (Figure 3(b)) were similar to those of the sample with 1.19 wt.% N; however, there are more pores (36) for the former. The sample with 1.37 wt.% N (Figure 3(c)) exhibited larger pores and a higher number of pores (49) than those of the other two samples. These pores were mainly distributed at the intersections of the grain boundaries. Hence, these results show that an increase in the N content tended to increase the number of pores. A matrix with more pores, which are mostly open holes, results in poor corrosion resistance of the matrix [31]. Figure 3(d) shows the XRD pattern of the solid-solution alloy. When the N content was high, the matrix was in the austenite phase. Owing to the high N content of the matrix, a small amount of Cr₂N existed.

(a)

(b)

(c)

(d)

Samples with different N contents were immersed in a 55°C 6% FeCl₃ solution for 72 h, and the weight loss of the samples before and after immersion was determined. The corrosion rate change rule is shown in Table 2. After the solution treatment at 1200°C, the corrosion rate of the matrix decreased with an increase in the N content.

Figure 4 shows the surface morphologies of the solution-treated alloys after their immersion in a 6% FeCl₃ solution at 55°C for 72 h. Under the same corrosive environment, pitting corrosion occurred on the surfaces of all three HNNS samples. Because of the high immersion temperature, the corrosion pits on the substrate surface were small and spherical with a shape similar to that of the fish scales. The fish-scale pits formed on the surface of the HNNS sample with 1.19 wt.% N (Figure 4(a)) were larger and deeper than those formed on the surfaces of the other two HNNS samples. When the N content was increased from 1.19 to 1.28 wt.% (Figure 4(b)), the size and depth of the pits on the corroded surface decreased. When the N content was further increased to 1.37 wt.% (Figure 4(c)), the corrosion surface became smooth and the size and depth of the pits on the corroded surface decreased. The size and depth of the corrosion pits of a substrate can characterize its corrosion resistance. At the same solid-solution temperature, an increase in the N content of the substrate decreased the diameter of the pits formed on the surface of HNNS after corrosion; thus, the corrosion surface no longer showed fish-scale pits. In other words, the resistance of the matrix improved with an increase in the N content.

(a)

(b)

(c)

Figure 5 shows the corrosion depth of the solution-treated alloy immersed in 6% FeCl₃ solution at 55°C for 72 h. The solution-treated alloys with the N contents of 1.19, 1.28, and 1.37 wt.% showed immersion corrosion depths of 178.29, 145.39, and 118.01 μm, respectively. As the N content increased, the corrosion depth decreased and the corrosion resistance of HNNS improved, which is consistent with the immersion weight loss results summarized in Table 2.

(a)

(b)

(c)

Figure 6 shows the potentiodynamic polarization curve of HNNS in 3.5% NaCl solution. The corresponding electrochemical parameters are listed in Table 3. Figure 6 shows the presence of a passivation zone in the polarization curve, with its range varying with the N content. As the N content increased from 1.19 to 1.37 wt.%, the passivation zone of HNNS widened, the polarization curve gradually moved upward, and the corrosion potential increased. As shown in Table 3, as the N content increased from 1.19 to 1.37 wt.%, the corrosion current density of HNNS in 3.5% NaCl solution decreased from 5.96 × 10⁻⁷ to 3.14 × 10⁻⁷ A cm⁻², and the corrosion potential increased from −0.469 to −0.377 V. Thus, with increasing N content, the corrosion current density of HNNS decreased and the corrosion potential increased.

The corrosion potential (E_corr) of a material can be used to characterize its corrosion resistance ability, where large E_corr values correspond to strong corrosion resistance. The corrosion current density (I_corr) reflects the corrosion rate, where low I_corr values correspond to slow corrosion rates, which indicate strong corrosion resistance [32]. Wu et al. [33] studied the potentiodynamic polarization curves of N-containing stainless steel with different N contents (0.66–0.82 wt.%) in 3.5% NaCl solution, in which the highest corrosion potential was obtained from the sample with 0.82 wt.% N. Thus, the higher the N content of HNNS, the stronger is its corrosion resistance. The changing law is consistent with the findings of this study.

Figure 7 shows the Nyquist curves of the HNNS samples in a 3.5% NaCl solution. In the Nyquist diagram, the capacitive arc radius can be used to characterize the corrosion resistance of the material. A large capacitive arc radius leads to a stable passivation film formed on the surface of a sample, which endows the alloying element with a high dissolution and strong corrosion resistance [34]. EIS measurements carried out under the passivation potential revealed that HNNS with 1.37 wt.% N showed the largest capacitive arc radius, whereas HNNS with 1.19 wt.% N showed the smallest capacitive arc radius, among all the samples examined in this study. The corrosion resistance of the samples with different N contents was ordered as follows: 1.37 wt.% > 1.28 wt.% > 1.19 wt.%. These changes are consistent with the findings of the potentiodynamic polarization curve.

The Nyquist plots of the samples were numerically fitted using the equivalent circuit shown in Figure 8, where R_sol represents the resistance of the electrolyte, R₁ represents the resistance of the pores in the film, R_ct represents the resistance of the passivation film, Q represents the pseudocapacitance of the film, and C is the double electric layer capacitance [35]. Table 4 lists the main electrochemical parameters obtained after fitting the EIS equivalent circuit. At the same solid-solution temperature, as the N content of HNNS increased from 1.19 to 1.37 wt.%, its R_ct increased from 1.51 × 10⁵ to 2.91 × 10⁵ Ω cm² (Table 4).

The structure of the sintered HNNS was not uniform, and nitride precipitates were present on its surface. The N content of HNNS was found to influence its reaction with Cr, in which a high N content accelerated the reaction. First, the discontinuous precipitations at the grain boundary appeared as round dots or short rods that precipitated to form crystal cells and finally arranged into parallel layers to form a lamellar shape. Following the solution treatment at 1200°C, the matrix entered the homogeneous austenite phase. After immersion in 6% FeCl₃ solution at 55°C for 72 h, the alloys with different N contents experienced mass loss and corrosion pits appeared on their surfaces. As the N content increased, the size and number of the corrosion pits on the surface of the substrate decreased, and the corrosion depth decreased. The potentiodynamic polarization curves and EIS results demonstrated that alloys with high N content exhibited high corrosion potentials, low current densities, and large capacitive reactance arc radii. Accordingly, HNNS with 1.37 wt.% N exhibited the highest corrosion resistance among all three HNNS samples investigated in this study.

4. Discussion

Increasing the N content is a highly effective approach for improving the corrosion resistance of austenitic stainless steel [36, 37]. Figure 9 shows the corrosion diagram of HNNS. In the initial stage of corrosion, Fe in the matrix easily oxidizes because of H⁺ produced by hydrolysis in the solution, generating soluble Fe²⁺ ions. Fe²⁺ further hydrolyzes to form Fe(OH)₂, which easily reacts with [O] in the passivation film to form a metal hydroxide, FeOOH (equations (2)–(4)).

(a)

(b)

(c)

These equations show that a large amount of H⁺ may exist on the surface of the sample, particularly inside the corrosion pits, which aggravates the corrosion. When a large amount of [N] is dissolved in the matrix, [N] reacts with water to generate OH⁻ (equation (5)), which can neutralize the H⁺ generated in reaction (4) and inhibit the acidification of the solution in the corrosion hole:

When the content of [N] in the matrix increases, as shown in Figure 9(b), more [N] is consumed in reaction (4), which consequently produces more OH⁻, reduces the H⁺ concentration in the corrosion hole, and inhibits the continued corrosion of the matrix. This also prevents the increased size and depth of the corrosion pits. Cr23Ni4Mo2N is an austenitic stainless steel with 1.0 wt.% N. When its [N] content is dissolved, [N] in NH⁴⁺ is stabilized [20]. When the [N] content in the matrix further increases, [N] can directly produce NH⁴⁺ by reacting with H⁺ hydrolyzed in the solution, as shown in reaction (6). Accordingly, at high N contents, the solid-solution [N] reacts with H⁺ before it reacts with other elements, such as Fe (Figure 9(c)). The reaction prevents the dissolution of the metal matrix and corrosion pits on the surface of the matrix, reduces the number of overall corrosion pits of the sample, and enhances the corrosion resistance of the sample:

The above analysis is based on the acid consumption theory [16]. Increasing N content can also be attributed to the surface enrichment [38, 39] and synergy [40, 41] theories. Considering the surface enrichment theory, a small amount of Cr₂N is present in the sample after solid solution due to the high N content of the matrix. During the passivation process, Cr₂N is enriched on the surface of the passivation film, and its N element reacts with water to generate NH₃ and NH⁴⁺ along with a small amount of NO₃⁻. As shown in reaction (7), the generated NO₃⁻ can inhibit the surface of the etch pits through repassivation, which can stabilize the passivation film and prevent pit growth [32, 33]:

When the N content of the substrate increases, the Cr₂N content of the sample increases. The amount of NO₃⁻ generated by the reaction also increases, which improves the ability of the sample to stabilize its passivation film and enhances its resistance to metal dissolution after its passivation film is destroyed. This results in an enhancement of the corrosion resistance of the sample.

According to the synergy theory [40, 41], the pitting equivalent equation (8) shows that an increase of 1 wt.% in the N content of stainless steel is equivalent to an increase of 30 wt.% in its Cr content [18]. Thus, the high N content of a sample results in a strong pitting resistance:

The highest N content of the HNNS samples prepared in this study was 1.37 wt.%. The effect of a further increase in the N content in improving the corrosion resistance of HNNS remains uncertain. In future, HNNS with higher N contents than the current samples will be prepared, and the relationship between its solid-solution N content and corrosion resistance will be investigated.

Compared with traditional austenitic stainless steel, high-N steel prepared by the powder metallurgy gas-solid nitriding method has a higher matrix N content. In SUS 304 stainless steel matrix, the Ni content is 8–11 wt.% without Mo. Meanwhile, the Ni content in SUS 316 stainless steel matrix is 10–14 wt.% with an Mo content of 2–3 wt.%. The high-N steel matrix in this study contains 3.5 wt.% Mo. Compared with SUS304, high-N steel is more resistant to Cl⁻ corrosion. An et al. [42] studied the pitting corrosion resistance of Cr23Mo1N HNNS and 316L stainless steel in Cl⁻-containing solutions. After immersion in the corrosive solution (6% FeCl₃, T = 35°C, t = 7 d), the corrosion rates of HNNS and 316L stainless steel were calculated to be 5.37 × 10⁻³ and 9.07 g m⁻² h⁻¹, respectively. This indicates the strong corrosion resistance of HNNS, that is, its pitting corrosion resistance is better than that of SUS 304 and 316 stainless steel. Therefore, a high N content in the matrix results in strong corrosion resistance.

5. Conclusions

(1)The powder metallurgy gas-solid nitriding method was used to prepare HNNS samples with N contents of >1.0 wt.%. The matrix structure was not uniform, and a nitride layer was formed at the boundary. When the matrix was treated with solid-solution at 1200°C, the structure showed a uniform austenite phase.(2)After immersion in 6% FeCl₃ solution at 55°C for 72 h, the corrosion weight loss rates of the samples with N contents of 1.19, 1.28, and 1.37 wt.% decreased to 1.74 × 10⁻⁵, 1.43 × 10⁻⁵, and 1.11 × 10⁻⁵ g mm⁻² h⁻¹, respectively. The corresponding corrosion depths decreased to 178.29, 145.39, and 118.01 μm, respectively. Therefore, the size and depth of the corrosion pits on the corroded surface decreased with increasing N content.(3)With an increase in the N content of HNNS from 1.19 to 1.37 wt.%, its corrosion current density decreased from 5.96 × 10⁻⁷ to 3.14 × 10⁻⁷ A cm⁻², whereas its capacitive reactance arc radius increased. After the equivalent circuit was employed, the passivation film resistance of the HNNS samples with N contents of 1.19, 1.28, and 1.37 wt.% increased to 1.51 × 10⁵, 2.38 × 10⁵, and 2.91 × 10⁵, respectively.(4)The excellent corrosion resistance of HNNS can be attributed to the presence of a large amount of solid-solution N in the matrix.

Data Availability

The data used to support the findings of this study are available from the corresponding author upon request.

Conflicts of Interest

The authors declare that there are no conflicts of interest regarding the publication of this study.

Acknowledgments

The authors thank Dr. Ning Wu and Dr. Haojun Zhou from Central South University for the informative discussions on the powder metallurgy gas-solid nitriding method and solid-solution treatment process feasibility. Mr. Mingchu Huang and Dr. Chen Wang at Central South University are acknowledged for their assistance with the XRD and OM. The authors are grateful to Mr. Chrisna Mea and Mr. Manoj Aravind from Editage Co. Ltd., Shanghai, China, for scrupulously polishing the English language of the study. The authors are grateful for the financial support from major projects of Changsha Science and Technology Plan (Grant no. kh2003014) and Strategic Emerging Industry Technology Research and Major Technology Achievement Transformation Project of Hunan Province (Grant no. 2019GK4002).

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