Research Article | Open Access
Mehmet Emin Arıkan, Rafet Arıkan, Mustafa Doruk, "Determination of Susceptibility to Intergranular Corrosion of UNS 31803 Type Duplex Stainless Steel by Electrochemical Reactivation Method: A Comparative Study", International Journal of Corrosion, vol. 2012, Article ID 478508, 14 pages, 2012. https://doi.org/10.1155/2012/478508
Determination of Susceptibility to Intergranular Corrosion of UNS 31803 Type Duplex Stainless Steel by Electrochemical Reactivation Method: A Comparative Study
In the present study as in our previous studies (Arikan and Doruk, 2008 and Arikan et al., 2012), similar specimens taken from a hot rolled cylindrical duplex stainless steel (DSS) bar with 22% Cr grade were solution annealed at 1050°C and then aged at 800∘C from 100 to 31622 min for sensitization treatment. Double loop electrochemical potentiodynamic reactivation and standard weight loss immersion acid tests were conducted. The solution annealed samples were found unsensitized. The samples aged for 100 min were less sensitized whereas samples aged for 316 min and more time were sensitized. The degree of sensitization (DOS) can be attributed to higher contribution of chromium and molybdenum depleted areas that result from intermetallic phases. However, especially the samples aged from 3162 to 31622 min have revealed chromium replenishment. Consequently, the degree of sensitization was lowered in comparison to the results obtained in previous studies.
Generally, duplex stainless steels (DSS) are Fe-Cr-Ni alloys having an approximately volumetric fraction of 50% ferrite and 50% austenite in their microstructures. Their main feature is that they compromise favorable corrosion resistance of austenitic stainless steels with good mechanical properties [1–4].
However, duplex stainless steels are susceptible to the precipitation of some phases that affect both the corrosion and the mechanical properties. These phases may be formed during the solidification of the alloy or in subsequent heat treatments or plastic deformation processes or even due to ageing processes during its use, causing a marked effect upon the workability and the useful life of the material . One of the possible phases to be formed is the sigma phase (), a hard and brittle intermetallic compound, rich in Cr and Mo, which is formed from ferrite . This phase has deleterious effect upon both mechanical and the corrosion properties .
In most of the duplex stainless steels sigma phase is formed between 600°C and 950°C and its precipitation becomes faster between 700°C and 900°C. The embrittlement of some alloys due to the sigma phase precipitation may occur in very short times, of the order of 3 min [7–9].
Brandi and Padilha  and Maehara et al.  found the sigma phase precipitation in duplex stainless steels that as the amount of sigma phase increases the amount of ferrite decreases, until its total consumption. According to this result it was concluded that the sigma phase is formed from the ferrite. The proposed mechanism for this formation [10, 11] is the eutectoid decomposition of ferrite according to the reaction where is the so called secondary austenite. The nucleation rate [12–14] and the kinetics  of this reaction have been studied extensively. It is well known that the controlling step is the nucleation rate. The growth of sigma phase causes a decrease in chromium and molybdenum content of the neighboring ferrite, which becomes unstable and transforms into austenite. This austenite, in turn, is rich in chromium and molybdenum and has a lower content of nickel if compared with the neighboring ferrite. These changes in chemical composition promote the formation of an additional sigma phase. The overall result is the coprecipitation of secondary austenite and sigma.
Additional phases found in duplex stainless steels can include chi (), laves (), and . The nucleation sites for and phases are grain boundaries, incoherent twin boundaries, and dislocations.
Duplex stainless steels are susceptible to sensitization due to the precipitation of additional phases when heated in a temperature range of 600–950°C. These phases have a reverse effect on the corrosion and mechanical properties [16, 17]. A substantial depletion of Cr and Mo due to a copious precipitation of and phases results in a decrease of the corrosion properties .
The harmful effect of sigma phase has been of great concern in welded duplex stainless steels, because during this heating and cooling process, the sigma phase is formed in the heat affected zones (HAZ) [19–21]. Leaks in pipelines produced with this type of steel were reported to occur in these zones .
According to Truman and Pirt  this effect is a consequence of Cr and Mo content decrease in the matrix phase because the sigma phase is considerably richer in these elements than either the ferrite or austenite. Adhe et al.  proposed that this decrease is confined to regions adjacent to sigma phase. Wilms et al. , on the other hand, observed that the localized corrosion starts next to the sigma phase in the newly formed secondary austenite.
Although the sigma phase has been considered extremely harmful to the corrosion resistance of the DSSs, the available information about it is limited. Thus, it was decided to undertake an investigation of the influence of ageing treatments on the sensitization of the DSS.
There are several test methods for determining the sensitization to intergranular corrosion. Weight loss acid test was first standardized and the test procedure was presented in ASTM A262-91 . Corrosion rate is determined by measuring the weight loss of the sample. Another test method of measuring the susceptibility to intergranular corrosion involves electrochemical reactivation of the steel samples as defined in ASTM G108-94 . This reactivation process is named as electrochemical potentiodynamic reactivation (EPR) and has been developed in single loop (SLEPR) or in double loop (DLEPR) types. The latter was first used for austenitic stainless steels. The best advantage of this technique is that it obtains a quantitative value of the degree of sensitization (DOS) instead of solely qualitative appreciation as metallographic etchings. The EPR test provides the degree of sensitization of the material which is proportional to the amount of chromium depleted areas adjacent to the chromium rich phases.
In this study, DLEPR was applied for the determination of the degree of sensitization of duplex stainless steel type UNS S31803 with 22% Cr grade. It is designated by X2CrNiMo 22-5-3 with the trade name SAF2205. The summary of technical literature related to austenitic-ferritic duplex stainless steels shows that test solution for DLEPR often consists of sulfuric acid (H2SO4) solution with the addition of KSCN as depassivator.
The purpose of the present study was to investigate intergranular corrosion behavior of DSS in relation to the influence of the microstructure produced by different heat treatments. This is performed by solution annealing at 1050°C and ageing at 800°C from 100 to 31622 min in order to provide different microstructure and sensitization levels. Electrochemical measurements were used to determine the degree of sensitization (DOS) to intergranular corrosion. Light optical microscopy (LOM) was used to identify the different phases that form in bulk material after the heat treatments. X-ray diffraction (XRD) technique and energy dispersive spectroscopy (EDS) analysis were used for studying microstructural evolution. Surfaces obtained after the DLEPR test and the weight loss immersion test were also observed to check the attacked locations and the relationship with the chromium depleted areas.
Similar works were performed by Arikan and Doruk  and Arikan et al.  on the same type duplex stainless steel aged at 650°C and 725°C, respectively, for various periods of time. The results are compared in Section 3.
2. Experimental Method
The same experimental methodology as in our previous studies was applied for the present work. The procedure was given briefly as follows.
The material used was a commercial type hot rolled bar of UNS S31803 duplex stainless steel (DSS) (trade name SAF2205). The chemical composition of the steel is given in Table 1.
The specimens were all solution heat treated at 1050°C for 1 hour and then quenched in water, followed by ageing heat treatments at 800°C from 100 to 31622 minutes and water quenching.
For metallographic examination, they were etched in NaOH solution as described in ASTM A923-03 . The solution for etching was prepared by adding 40 g of reagent grade sodium hydroxide to 100 g of distilled water. The polished specimens were electrolytically etched at 2 volts for 20 seconds at room temperature. It colors the phases in duplex stainless steel such as austenite in white, ferrite in light brown, sigma in dark brown, and carbides in black.
The weight loss test was done according to ASTM A923-03 Test Method C standard. For this, the test solution is prepared by dissolving 100 g of reagent-grade ferric chloride, FeCl3-6H2O, in 900 mL of distilled water (approximately 6% FeCl3 by weight). The solution is filtered through glass wool or filter paper to remove insoluble particles. The pH of the test solution shall be adjusted to approximately 1.3 prior to beginning the test by the addition of HCl or NaOH, as required.
The corrosion rate is calculated in accordance with the weight loss and total surface area. Unless otherwise specified, the calculated corrosion rate shall not exceed 10 mdd. The corrosion rate is calculated in accordance with the following: corrosion rate (mdd) = weight loss (mg)/(specimen area (dm2) × time (days)). Tests are performed using FeCl3 solution with a volume of 20 mL/cm2 at °C for 24 hours.
The chemical composition and the profile line analysis of the phases were carried out by EDS with SEM. The presence of different phases was also identified by X-ray diffraction patterns by means of Rigaku diffractometer with Cu radiation.
The susceptibility of the aged DSS to intergranular corrosion was evaluated using DLEPR test according to ASTM G108 standard . The test was performed according to the recommendations of Majidi and Streicher [30, 31]. The standard solution is modified to suit duplex stainless steels and consisted of 2 M H2SO4 + 0.5 M NaCl + 0.01 M KSCN at °C . The test cell consisted of a 1 litre flask with necks for electrodes. A cylindrical working electrode was centrally located and two counter electrodes were placed next to specimen to improve the current distribution. The specimen was mounted according to Stern-Makrides arrangement .
The potential was scanned with a rate of 15 V/hour in the anodic direction from below the to +250 mV (SCE) in middle of the passive region and then scanned back to the . The scanning direction was then reversed and hence two loops are generated. The peak activation current () and the peak reactivation current () were measured during the forward and backward scans, respectively. The degree of sensitization (DOS) was thus measured as the ratio of the maximum current densities, × 100 [30, 31].
The activation or critical current density () or () is proportional to the corrosion rate of a metal. The rate of corrosion rises rapidly in the activation range up to the activation peak current density. The potential corresponding to this is called activation peak potential or passivation potential . If the potential is raised further, the anodic current will drop to a lower value called passivation current density (), and then it will remain constant over a wide potential range. This is the passive range in which a thin invisible film of oxide covers the metal surface. This protective film acts as a barrier between the metal and its environment and reduces the rate of dissolution.
During the anodic sweep, the entire surface is active and contributes to the peak current. Nevertheless, during the reactivation sweep, only the sensitized regions contribute to the passive-active transition. The unsensitized specimens show a small and result in a small ratio. On the other hand, in heavily sensitized specimens, approaches resulting in a high ratio.
3. Results and Discussion
3.1. Metallographic Examination
The optical micrographs obtained by etching with NaOH reagent are given in Figures 1 and 2. Figure 1 represents the microstructure of solution annealed parent alloy in which white phase is austenite () and the dark phase is ferrite (). The volume fractions of and were 54 and 46%, respectively. The microstructure does not reveal any visible precipitates of other phases.
To study the influence of the microstructure on degree of sensitization (DOS), the specimens were aged at 800°C for times 100, 316, 1000, 3162, 10000, and 31622 min. The ageing heat treatments induced a marked change in the ferrite/austenite ratio caused by the transformation , as given by (1). The nucleation rate [13, 32] and the growth kinetics of this reaction have been studied extensively . It is well known that the controlling step is the nucleation rate. One of the possible phases to be formed is the sigma phase which is rich in Cr and Mo.
For specimens aged at 800°C, microstructural changes are shown in Figures 2(a)–2(f). For ageing 100 min, small precipitates of sigma phase appear at and boundaries. Incoherent twin boundaries and dislocations inside the ferrite matrix may also be the nucleation sites for precipitation . The precipitations of -phase was first encountered after ageing for 100 min and became more massive with ageing time. Nucleation and growth of σ-phase are thermally activated processes involving diffusion. Therefore, temperature will have a significant effect on the kinetics of the transformation. After 316 min, a lot of sigma precipitates had developed at , and inside the ferrite phase as shown in Figures 2(b)–2(f). Longer ageing treatment leads to the increase and coarsening of the σ phase in an irregular shape.
3.2. Phase Volume Fraction by Light Optical Microscopy
Microanalysis reveals that the solution annealed material consists of ferrite and austenite phases. The main microstructural change during ageing is the formation of σ-phase and secondary austenite () from the ferrite phase due to the eutectoid reaction (1). The amounts of phases were estimated by measuring the fractions of colored area on polished and etched specimens by light optical microscopy (Leica DMI 5000 M metal microscopy). The measured volume fractions of ferrite, austenite, and sigma phases for different ageing times are given in Table 2 and Figure 3. Since the ferrite transforms into and , the ferrite phase disappears in short time (1000 min). The total austenite is considered as the sum of the primary and secondary austenite () and increases to the value of 55% in 1000 min.
During the early stages of the transformation, sigma forms preferentially at the and grain boundaries and inside the -grain and grows into the ferrite phase via a transformation mechanism involving diffusion. Because both nucleation and diffusional growth of are thermally activated processes, the ageing time and temperature will have a significant effect on the kinetics of the transformation. The time at which sigma was first observed was 100 min at 800°C.
3.3. Weight Loss Test Results
The susceptibility to intergranular corrosion is given by the loss of weight due to the dissolution of chromium depleted areas and is expressed as the rate of weight loss in mg per sq·dm per day (mdd). The results of standard weight loss immersion test are given in Table 3 and plotted in Figure 4. Since the calculated corrosion rate does not exceed 10 mdd, the test results are acceptable. The first step of the evaluation of tested specimens was visual and microscopic examination. The degree of sensitization was given by the loss of weight due to the dissolution of chromium depleted areas and is expressed as the rate of weight loss in mdd. The corrosion rate is quite high for 100 min and increases rapidly up to 1000 min and then slows down and even a slight decrease is observed for 3162 and 10000 min of ageing and then increases again slightly by the end of 31622 min. Moreover, the lower chromium and molybdenum content is not the only factor responsible for the increase in the rate of corrosion. The neighborhood of more noble phases (sigma phase) will enhance the anodic dissolution of secondary austenite extensively.
The surfaces of the corroded specimens were examined using LOM. The localized attack in black points is initiated in the secondary austenite phase adjacent to the sigma phase as shown in Figure 5. The austenite and the sigma phases resist the ferric chloride solution more than the ferrite and the secondary austenite. Once a pit is formed it rapidly propagates within the initial ferrite region. As a result, it is observed that the sigma and austenite phases are almost intact, while the secondary austenite () and some iron rich ferrite phases are attacked.
3.4. EDS Analysis of Phases
The precipitation of the intermetallic sigma phase is accomplished by the formation of secondary austenite (). As the sigma phase grows, chromium and molybdenum are enriched in these precipitates and, simultaneously, nickel diffuses into the ferrite. The enrichment of -stabilizing elements (such as Ni) in the ferrite and the loss of ferrite stabilizing elements (such as Cr and Mo) lead to an unstable ferrite transforming into secondary austenite depleted in chromium and molybdenum .
SEM image and profile line analysis of the sample aged at 800°C for 316 min is given in Figure 6. The sigma phase appears black, the ferrite dark gray, and the primary austenite light gray. A bright region around the sigma phase is likely secondary austenite. The EDS measurements of Cr, Mo, Ni, Mn, and Fe content of the , , , and phases are given in Table 4. The relative concentrations of major alloy elements across the secondary precipitates are measured by the line scanning as shown in Figure 6.
The phases have different chemical composition. The results indicate that the phase was partitioned in Cr and Mo where the secondary austenite is depleted in Cr and Mo. For instance samples aged at 800°C for 316 and 31622 min show depletion of chromium in secondary austenite from 26.32% to 20.26% and 20.23%, respectively, and a nearly total loss of molybdenum. Chromium content of the sigma phase reaches to 30.76% and 35.21%, respectively.
3.5. X-Ray Diffraction Pattern
The results of the X-ray diffraction analysis consist of a series of diffraction patterns given in Figure 7. The diffraction pattern of the solution annealed parent alloy presents ferrite and austenite phase peaks only. Samples aged at 800°C for different ageing times show the peaks of phases developed.
Although the precipitations at grain boundaries are evident for 100 min of ageing as shown in light optical micrograph of Figure 2(a), the X-ray spectra of the sample does not reveal any sigma peak. This may be attributed, as given in Table 2, to the low volume fraction of the sigma phase (4.6%).
Samples aged at 800°C show sigma peaks first in 316 min of ageing. With increased holding time, the intensity of sigma peaks increases as the volume fraction of sigma phase increases (Table 2) and also additional sigma peaks appear. After 1000 min of ageing, one of the ferrite phase peaks decreases to nearly zero but the other peak does not disappear; it overlaps with a sigma phase peak. After longer periods of time such as 10000 min, the treatments promote the transformation of ferrite phase. This results in a noticeable decrease in the intensity of the and an increase of peaks. The decrease of the ferrite peak intensity indicates that the major fraction of ferrite is transformed into sigma. Consequently, several sigma peaks are observed. All the changes observed in the diffraction peak intensity correlate well with the changes in volume fraction of each phase during the isothermal hold as given in Table 2.
3.6. DLEPR Results
Figure 7 shows the polarization curves for samples in solution annealed and aged condition. The curve obtained from the solution annealed sample is treated as a reference and compared with the others. The activation peak current density of the reference curve is 23.13 mA/cm2 and the corresponding activation peak potential () or passivation potential () is −212.78 mV with respect to saturated calomel reference electrode (SCE). This peak reaches a maximum and then fall to a low passive current density () of 0.001448 mA/cm2 before reaching the chosen reverse potential of +250 mV. The sample is thus passivated in a wide range between −212.78 mV and +250 mV. In this passive range, a thin invisible film of oxide may cover the metal surface. The protective film acts as a barrier between the metal and its environment and reduces its rate of dissolution. And hence, the ratio is very low (0.027634%). This may be considered as unsensitized material (Table 5).
From the sample aged for 100 min, few sigma phase precipitates were observed optically (Figure 2(a)). The amount is determined by volume fraction which is very small, about 4.6%, (Table 2). Therefore, the diffraction pattern does not reveal any evidence of the phase. Consequently, the sample presents very small reactivation current (Table 5), and hence the ratio is 1.99% and, accordingly, the corrosion rates become 2.06075 mdd (Table 3). This means a slight chromium depletion resulting in a less sensitization.
After ageing for 316 min, the formation of a massive sigma phase nucleation at the boundaries and within the ferrite grains was observed (Figure 2(b)). The XRD curves (Figure 7) reveal this evidence because of the significant amount of the phase (22%) (Table 2). Next to the -phase, the secondary austenite () forms from the decomposition of ferrite into and (Table 2). Dissolution of the secondary austenite results in greater weight loss (4.39 mdd) (Table 3) and, accordingly, a high ratio of (17.61%) (Table 5). This means that the sample has been quite sensitized.
The degree of sensitization (DOS) is also given by the loss of weight due to the dissolution of chromium depleted areas. The results are given in Table 3 and plotted in Figure 4. When aged at 800°C, the corrosion rate is low for 100 min but increases up to 1000 min and then slows down and even a slight decrease is observed for 3162 and 10000 min of ageing. Then, it increases again slightly by the end of 31622 min.
The DOS values exhibit a similar trend. For instance, the aged samples mainly for longer ageing treatment such as 1000, 3162, 10000, and 31622 min led to coarsening of the sigma phase and slowed the corrosion rate to 4.99, 4.64, 4.80, and 5.09 mdd, respectively, and the corresponding current density ratios () or DOS values are given as 31.67, 15.08, 61.01, and 36.82%, respectively. These values are lower than those obtained at 725°C. Higher ageing temperature such as 800°C promotes a redistribution of chromium in depleted zones . In other words, it causes the replenishment of the secondary austenite by chromium diffusion from the chromium rich ferrite phase and from the interior of the austenite. As a result, prolonged ageing at 800°C causes a decrease in DOS and hence a decrease in corrosion rate in comparing with the results of lower ageing temperatures such as 725 and 625°C.
When the polarization curves of the samples aged at 800°C from 100 to 31622 min are compared with the reference curve, it is seen that the activation peak current density () increases with increasing ageing times (Table 5). Also, the passive current density () increases from 0.029998 mA/cm2 up to 0.040190 mA/cm2, and the passivation potential () increases from −212.78 mV to −145.65 mV (SCE).
From the results discussed so far, considering weight loss acid test and DLEPR test, it can be concluded that both the sensitization and the corrosion rate have increased with respect to the depletion of chromium and molybdenum in the ferrite region.
Chromium diffusion is much faster in ferrite than in austenite. The chromium concentrates in the neighboring sigma phase  and causes the sigma phase to grow fast within the ferrite region. As a result, the formation of the secondary austenite can degrade the stability of the passive film .
After the DLEPR test, for instance, samples aged for 1000 and 10000 min were slightly polished and examined with LOM (Figures 9(a) and 10(a)) to check the attack locations and the relationship with the chromium depleted areas. Observation of the surface indicates that the sigma and austenite phases are almost intact, while the secondary austenite and some iron rich ferrite phases are attacked. The corroded secondary austenite regions appear in black and the isolated sigma precipitates in white. The only difference is that the amount of corroded area is larger for 10000 min of ageing. Large primary austenite grains remain in white as usual. To distinguish sigma and primary austenite phases in color, the samples were electrolytically etched with NaOH reagent. The sigma phase is colored reddish brown and distinguished from the primary austenite which was not affected from the etchant (Figures 9(b) and 10(b)).
When the DLEPR and acid test samples (Figure 5) are compared, they show similar behavior because the same areas were affected in both cases. In other words the attacks have concentrated at sensitized areas. The appearance of the localized attack after immersion test shows large number of black points clearly. This shows that local corrosion is initiated in the secondary austenite phase as what happened in the DLEPR test samples. Once a pit is formed, it rapidly propagates within the initial ferrite region. After a long time of exposure, the corroded area extended and covered a large area including many sigma and austenite phases. As a result, large cavities were developed. This type of corrosion is known as localized corrosion.
As mentioned before, Arikan and Doruk  and Arikan et al.  presented a study dealing with DLEPR and standard weight loss acid tests for the same type of duplex stainless steel annealed at 1050°C for 1 hour and aged at 650°C and 725°C for the same periods of time. The results are compared in the following paragraphs.
Comparison of the results of micrographs, X-ray, and digital image analysis obtained from samples aged at 650°, 725°, and 800°C, indicates that the minimum time where sigma was first observed is less than 100 min at 800°C, less than 316 min at 725°C, and longer as 1000 min at 650°C. Both DLEPR and acid tests expose continuous chromium depleted zones leading to intergranular corrosion at phase boundaries and local corrosion around sigma phases precipitated inside the ferrite region.
Samples exhibit nearly the same corrosion rates such as 2.42, 2.37, and 2.06 mdd for 3162, 316, and 100 min of ageing at 650, 725, and 800°C, respectively, and then increases rapidly with ageing time.
A similar trend for DOS values was observed, but since ferrite decomposition occurs faster at 800°C, accordingly, sensitization begins in shorter time of ageing than that at 725 and 650°C. This indicates that the DLEPR test provides reasonable results proportional to -phase content.
For ageing at 650°C and 725°C, the sensitization and corrosion rate depend strongly on the extent of chromium and molybdenum depletion. But in the case of 800°C, both the sensitization and corrosion rate are lower due to the replenishment of the secondary austenite by chromium diffusion from the chromium rich ferrite phase and from the interior of the austenite. As a result, the sensitization and corrosion rate depend strongly on the extent of replenishment of the secondary austenite. Accordingly, this causes a decrease in DOS and hence a decrease in susceptibility to intercrystalline corrosion.
Only the solution annealed samples and the samples aged at 650°C for 100 and 316 min and at 725°C for only 100 min are unsensitized. At higher ageing temperature of 800°C, the samples are moderately sensitized even for the ageing time less than 100 min. The corresponding DOS value (1.999%) and the corrosion rate (2.06 mdd) are indicative of less sensitization.
Prolonged ageing between 1000 and 31622 min at 800°C causes a decrease in DOS (31–61%) and hence a decrease in corrosion rate in contrary to 725°C. This may be due to redistribution of chromium in the chromium depleted zones  which is indicative of the replenishment of the secondary austenite by chromium diffusion from the chromium rich ferrite phase and from the interior of the austenite.
3.7. Analysis of Polarization Curves in Reverse Scanning
At the beginning of the reverse scanning, the anodic current density decreases and the anodic curve moves to the left (Figure 8). This is an indication of thickening of the oxide film. On decreasing the potential, the anodic current density is reduced nearly to zero. This is due to the slowing of the anodic dissolution kinetics caused by thickening of the passive film. The sample has thus continued to passivate from through , back to potential . Further reducing the potential, the direction of the current density has changed between and as shown in Figure 11. It shows a loop consisting of cathodic current . The origin of the cathodic current can be attributed to the fact that at potentials between and , the rate of the cathodic reaction is greater than the anodic current density and hence the net current is cathodic over the potential range, (Table 6). If the potential is further reduced on the reverse scan, the direction of the current density changes back and an anodic reactivation loop is generated. This indicates that the oxide has dissolved and metal dissolution reaction has occurred. The development of the reactivation peak current density () can be attributed to metal dissolution. The lowered reactivation peak current density (on the reverse scan) is due to incomplete reactivation of the metal surface.
If no cathodic loop was generated on the reverse scan, the anodic reactivation would begin at a higher potential and would likely reach a high value of in a short time, and thus the metal dissolution would take place.
The same cathodic loop behavior is observed on the reverse scans of polarization curves obtained from the solution annealed and aged samples by DLEPR test (Table 6).
The potential ranges () of samples aged at 800°C from 100 to 31622 min, where the cathodic loops are obtained, are different from that of the solution annealed sample. In general, their reactivation curves look like that of the solution annealed sample. A similar cathodic loop behavior has been observed for all cases but the anodic loops do not resemble that of the solution annealed sample. This indicates that the precipitates developed in the microstructure influence the polarization behavior.
For all cases except for 31622 min the potential ranges () for the cathodic loops change from 0.200 to 0.172 volt and are less than that of the solution annealed sample. However, the formation of the cathodic loop delays the occurrence of the anodic reactivation current loop even for a short time. Then, the direction of the current density changes back quickly and the anodic reactivation current density begins to be generated at a potential of V for ageing 100 min. It then reaches the peak value of A/cm2 with the DOS value of 1.9999% for ageing 100 min.
For the sample aged for 316 min, the potential range (Δ) for the cathodic loop is 0.196398 V. This is lower than the value measured for the solution annealed one. The dissolution of oxide begins at a high potential such as V. After a short delay, the reactivation current density reaches A/cm2. The DOS value is 17.617%.
For the sample aged for 1000 min, the potential range () for the cathodic loop is 0.188347 V. This is lower than the value measured for 316 min of ageing. The V) and V) have been found higher with increasing ageing time. The reactivation peak current density () has reached to 14.189 mA/cm2 corresponding to a high DOS value (31.677%).
For the sample aged for 3162 min, the range of the potential for the cathodic loop is 0.188076 V. This is more or less the same as the value obtained for 1000 min of ageing. But the V) is higher and (= 0.046346 V) is lower than the value obtained for 1000 min of ageing. The reactivation peak current density () has decreased to 6.6807 mA/cm2 corresponding to a low DOS value (15.680%).
For ageing time of 10000 and 31622 min, cathodic loops on the reverse scan are obtained within a potential range of 0.172446 and 0.205538 V, respectively. And then the anodic reactivation loops suddenly begin to be generated at higher potentials of such as −0.12440 and −0.13465 V, respectively. The reactivation peak current densities () have reached to 35.355 and 25.583 mA/cm2 and the corresponding DOS values are 61.015 and 36.827%, respectively. As seen from Table 6, the and have changed disorderly with increasing ageing time.
For all cases the cathodic loops delay the occurrence of the anodic reactivation loops. The anodic reactivation peak current densities increased constantly until the peak current densities () were reached but they were also found lower than that obtained at 725°C for all ageing times. Since the values depend closely on the dissolution reaction of the phases in the metal, during the reactivation sweep only the chromium depleted areas contribute to the passive-active transition. But at 800°C longer ageing from 1000 to 31622 min causes limited replenishment of the chromium depleted zones. Consequently, this resulted in lower and hence lower DOS values.
The limited replenishment of the chromium depleted zones also caused larger potential range for cathodic loops and the values are also found lower than those obtained at 725°C. This is why the occurrence of the anodic reactivation loops was delayed more.
A similar behavior has been observed for the passive current densities (). The chromium depletion or dissolution of secondary austenite phase () causes the passive current densities to shift to higher current densities as compared to that obtained from the solution annealed sample (Figure 8, Table 5). But the values are lower than the values obtained at 725°C because of the limited replenishment of the chromium depleted zone at 800°C.
First, the effect of isothermal treatment at 800°C on the microstructures and consequent corrosion behavior of a duplex stainless steel UNS S31803 was investigated. Then the results were compared with the previous results obtained from samples aged at 650 and 725°C [27, 28]. The important findings are summarized as follows.(a)The solution annealed sample is unsensitized condition. The structure is free of precipitations, and consequently it presented a very small reactivation current. When aged at 800°C the samples were sensitized even for ageing less than 100 min. The corresponding DOS value (1.999%) and the corrosion rate (2.06 mdd) are indicative of sensitization.(b)Comparison of the results of micrographs, X-ray, and digital image analysis obtained from samples aged at 800°, 725°, and 650°C indicate that the minimum time where sigma was first observed was less than 100 min at 800°C, less than 316 min at 725°C, and as long as 1000 min at 650°C. However, the degree of sensitization increased rapidly with increasing ageing time for all the cases. This can be attributed to a higher contribution of chromium and molybdenum depleted areas resulting in the formation of the intermetallic phases. (c)Prolonged ageing between 1000 and 31622 min at 800°C caused a decrease in DOS (31–61%) and hence a decrease in corrosion rate in contrary to 725°C and 650°C. A possible explanation of this is that it may be due to redistribution of chromium in the chromium depleted zone  which is indicative of the replenishment of the secondary austenite by chromium diffusion from the chromium rich ferrite phase and from the interior of the austenite. (d)For all cases from the observations of the polarization curves it may be concluded that cathodic loops do not affect metal dissolution. They merely delay the occurrence of anodic loops for a short time in a small potential range. These potential ranges () measured over the cathodic loops depend on the protective film thickness, ageing temperature, time, and microstructural changes in the material. Actually, during the anodic sweep, the entire surface is active and contributes to peak current. But, during the reactivation sweep, only the sensitized areas contribute to the passive-active transition. Thus, unsensitized specimen show a small and therefore a small ratio, while in heavily sensitized specimens, approaches , giving a high ratio. Oxide dissolves first and then metal dissolution takes place.
The peak reactivation current density () depends closely on the dissolution reaction in the metal. But higher temperature treatment such as 800°C leads to limited replenishment of the chromium depleted regions (secondary austenite) and hence reduced the amount of sensitized areas. This allowed less dissolution of the secondary austenite phase resulting in lower and hence lower DOS values. This means that the sensitization and corrosion rate depend strongly on the extent of replenishment of the secondary austenite.
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