Figure 3 shows the morphology and composition of inclusions in Inconel 690 alloy. The inclusions generally exhibit well-defined geometries, including triangular and square shapes, with sizes ranging from a few micrometers. Figure 3A and B show TiN-coated MgO and Al₂O₃ inclusions, approximately 2-5 μm in size. EDS analysis confirms that the core regions are predominantly MgO and Al₂O₃, partially encapsulated by TiN. Additionally, Figure 3C depicts TiN inclusions, often near-square or irregular in shape. Ti, an essential element in Inconel 690 alloy, enhances its oxidation resistance and stress corrosion cracking resistance. Despite trace concentrations of Ti and N, the low formation energy of TiN favors its formation during solidification. MgO and Al₂O₃, as impurities introduced from refractory materials during smelting, are high-melting-point compounds. During solidification, TiN inclusions nucleate on MgO and Al₂O₃, with additional homogeneous nucleation of TiN also occurring^[40].

Figure 4 illustrates the evolution of inclusions as initiation sites for pitting. In Figure 4B, microcracks are observed between the inclusions and the matrix, representing initial pit sites. As corrosion progresses, Figure 4D shows preferential dissolution along the inclusions, with more pronounced corrosion around these regions. Over time, the inclusions gradually dissolve and eventually disappear, as shown in Figure 4F. The primary mechanism of pitting in Inconel 690 alloy is generally associated with the breakdown of the protective passive film and the subsequent formation of localized corrosive environments. Although the passive film was not directly characterized in the present study, extensive previous studies have demonstrated that chloride ions can induce local degradation of passive films on nickel-based alloys, thereby triggering pit initiation and localized dissolution^[41,42]. Therefore, the role of passive film breakdown discussed in this work is interpreted based on established corrosion mechanisms reported in the literature rather than direct microscopic characterization of the passive film. Inclusions such as TiN, MgO, and Al₂O₃ serve as preferential sites for pitting development due to three main factors: electrochemical heterogeneity, passive film breakdown, and stress concentration^[43-45].

Previous studies have shown that corrosion preferentially initiates in the vicinity of oxide inclusions or inclusion-matrix interfaces, indicating that MgO-containing inclusions can markedly increase the susceptibility to localized corrosion and pitting behavior^[46]. Firstly, a potential difference exists between the inclusions and the matrix. TiN, a hard and electrochemically stable compound, exhibits a higher potential than the surrounding Ni and Cr matrix elements, making it cathodic relative to the matrix in corrosive environments. This galvanic coupling accelerates localized dissolution of the matrix around the inclusions, leading to pit initiation. Secondly, the Cr₂O₃-based passive film commonly reported to protect the alloy surface can be locally compromised or inhomogeneous at inclusion sites, allowing corrosive media to penetrate and initiate pitting. Thirdly, the mismatch in thermal expansion coefficients between MgO inclusions and the metallic matrix may lead to local stress concentration at the inclusion-matrix interface under thermal cycling or service conditions. Such stress concentration can potentially promote interfacial damage or microstructural defects, which may provide preferential pathways for the ingress of corrosive agents, thereby further accelerating pitting development.

Figure 5 shows that pits formed on the surface of Inconel 690 alloy, which are commonly associated with passive film breakdown, typically appear as shallow depressions, several micrometers in diameter, with disc-like morphologies and no inclusions present within them. This observation indicates that passive film breakdown not only originate at the inclusion-matrix interface. Instead, discontinuities in the passive film may also develop at non-inclusion sites, where localized damage facilitates the adsorption of Cl^-, and initiates pitting. Such breakdown is often associated with minor surface defects, including grain boundaries or compositionally heterogeneous regions. At these sites, Cl^- preferentially adsorb at defects in the passive film, replacing hydroxyl groups and forming soluble chlorides. This substitution reaction further degrades the protective film, exposing the underlying matrix and driving localized anodic dissolution that gives rise to pits. Direct characterization of the passive film (e.g., XPS or TEM analysis) is beyond the scope of the present study and will be considered in future investigations. Moreover, the presence of Cl^- lowers the corrosion potential and increases current density, thereby accelerating pit initiation and propagation.

During the experiments, it was observed that most of the disc-shaped pits formed by passive film breakdown on the surface of Inconel 690 alloy exhibited limited growth at 70 °C. To further investigate this phenomenon, the experimental conditions were adjusted to enhance the likelihood of pit development. Specifically, the corrosion temperature was increased to 90 °C, as elevated temperatures promote passive film breakdown, thereby facilitating the investigation of pit evolution at non-inclusion sites.

In situ observations were performed using OM at 1,000 × magnification. As shown in Figure 6A, two inclusions were identified as reference markers in the selected region of interest, enabling continuous tracking of the corrosion evolution. After 1 h of immersion at 90 °C, numerous pits that are typically associated with passive film breakdown appeared in the monitored region, as shown in Figure 6B. However, upon further exposure for 2 h, the majority of these pits did not propagate further, with only a single pit continuing to grow into a larger cavity.

This behavior reflects the metastable nature of pitting growth, wherein pits may evolve along two distinct pathways. In the first case, shallow pits fail to sustain the local accumulation of Cl^-, limiting vertical growth. These pits undergo repassivation and cease to propagate, as seen in the majority of cases in Figure 6. In the second case, a small subset of metastable pits avoids repassivation and transition into steady-state growth. Localized deepening promotes Cl^- accumulation, which in turn accelerates corrosion through a positive feedback mechanism. These pits progressively enlarge and evolve into stable, sustained corrosion sites, as shown in Figure 7.

Figure 8 shows the surface evolution of pits in Inconel 690 alloy with increasing immersion time in 6% FeCl₃ + 0.16% HCl solution at 70 °C. Pits expanded outward from their central initiation sites, during which thin lacy covers formed above them. As growth proceeded, these covers eventually fractured and collapsed. The lacy covers were relatively thin, typically ranging from several to more than ten micrometers in thickness, as shown in Figure 8A. During enlargement, pits expanded radially from the initiation center, maintaining an approximately circular morphology, as shown in Figure 8B.

As illustrated in Figure 9, detachment of the lacy cover in larger pits could even lead to the formation of secondary pits within the interior. The lacy cover functioned as a diffusion barrier during early pit growth, stabilizing the localized environment and facilitating continued propagation. Once the pit reached sufficient depth in the vertical direction, its geometry alone provided an effective diffusion barrier for sustaining the aggressive electrolyte within the cavity. Meanwhile, the lacy cover itself underwent progressive corrosion, developing perforations that gave rise to its characteristic morphology before ultimately collapsing and disappearing as the pit matured^[34].

Figure 10 shows the cross-section of a pit following freezing, extraction, and air-drying. Elemental analysis combined with EDS spectra revealed marked accumulation of Cl within the corrosion product region, together with pronounced enrichment of O and Cr. These findings indicate the formation of sparingly soluble Cr oxides during the corrosion process. In contrast, Ni and Fe were only sporadically distributed. Their corrosion products, primarily chlorides, remained soluble and readily exchanged with the external environment, preventing their accumulation within the pit region.

Cross-sections of pits before and after lacy cover formation were examined, and compositional mapping and line-scan analyses were performed using EDS [Figure 11]. As shown in Figure 11A, in the stage preceding lacy cover formation, only partial Cl enrichment was detected, while other ions remained at relatively low levels inside the pit. By contrast, after the lacy cover developed [Figure 11B], Cl accumulation became more pronounced, accompanied by pronounced enrichment of Cr, whereas Ni and Fe remained sparsely distributed. This difference arises because, without a cover, pits propagated at a relatively low corrosion rate, and dissolved species exchanged freely with the external solution, preventing substantial ionic accumulation^[47]. The minor enrichment of Cr, Ni, and Fe observed in the EDS spectra at this stage likely resulted from the inadvertent intrusion of matrix debris during specimen preparation.

The formation of a lacy cover accelerated the corrosion process, leading to the generation and retention of greater amounts of sparingly soluble Cr oxides. Line-scan analysis further supports this trend: in Figure 11A, the highest peaks of Cl and Fe correspond to FeCl₃, the primary component of the corrosive medium, while a secondary Cl peak coincided with Cr, confirming limited Cr oxide accumulation. In contrast, nearly all Cl peaks in Figure 11B coincided with Cr peaks, indicating that the lacy cover promoted ion retention within the pit and enhanced the accumulation of sparingly soluble Cr oxides, thereby accelerating pit growth.

Figure 12 shows 3D reconstructed morphology of pits during their steady-state growth in 6% FeCl₃ + 0.16% HCl solution at 70 °C. In the early stage of steady-state growth, pits expanded laterally, growing outward from the initiation site while also deepening, but at a slower rate, resulting in a disc-shaped morphology, as shown in Figure 12A. With continued immersion, lateral growth slowed, and depth propagation became dominant, producing a cylindrical morphology, as shown in Figure 12B.

As growth proceeded, a characteristic lacy cover developed over the pit, as shown in Figure 12C-E. Prior to cover formation, surface observations and 3D reconstructions revealed that the pit mouth width closely matched the maximum pit diameter, and most internal features were visible from the surface. After the cover formed, the 3D model (in blue) revealed protrusions at the uppermost layer corresponding to perforations in the lacy cover (in gray-purple box), with a surface opening much smaller than the pit’s maximum perimeter.

Figure 12F compares 3D pit reconstructions between 10 and 16 h at the same scale. Before the lacy cover developed, pit volume remained relatively small. Once the cover formed, pit volume increased sharply. This transition arises because pit growth requires retention of aggressive ions within the cavity. In the early stage, shallow pits struggle to trap ions and often repassivate. Once depth increases sufficiently, limited ion exchange slows transport to the external solution, enhancing localized attack near the pit mouth. These favors renewed lateral expansion, leading to hemispherical or ellipsoidal morphologies. Weak regions near the surface eventually perforate, forming the lacy cover, which further traps ions, accelerates corrosion, and drives rapid pit volume increase^[27,31,48].

Figure 13 shows 3D reconstructed of pits formed in 6% FeCl₃ + 0.16% HCl solution at 90 °C for immersion times of 4-9 h. Compared with 70 °C, pits grew markedly faster at elevated temperature, and the reconstructed lacy cover appeared larger and more densely perforated, indicating accelerated growth, as shown in Figure 13F. After 4 h, some metastable pits deepened and transitioned into steady-state pits. As shown in Figure 13A, the pits initially displayed a shallow disc-like morphology. With continued immersion, deeper propagation became dominant, and by 5-6 h the pit elongated markedly, evolving into a cylindrical shape, as shown in Figure 13B and C. This morphology enhanced ion retention, promoting sustained localized attack and setting the stage for rapid growth. By 7 h, higher temperature accelerated lacy cover development, producing densely distributed perforations, as shown in Figure 13D. As growth proceeded, the pit transitioned towards a hemispherical morphology with sharply increasing volume. At 9 h, the lacy cover collapsed, exposing the interior cavity and revealing considerable depth and width, as shown in Figure 13E. Such extensive pit growth, if occurring in service environments, could critically undermine corrosion resistance and pose risks of irreversible structural damage.

The 3D feature parameters of pits including surface area, volume, width, and depth with temporal evolution under 70 and 90 °C conditions, illustrated in Figures 14 and 15.

At 70 °C, all parameters increased progressively with immersion time. Before 13 h, however, growth was relatively slow, corresponding to the stage prior to lacy cover formation. During this stage, depth growth had limited impact on pit volume and surface area. For example, from 10-12 h, pit depth nearly doubled (from 45.5-79 μm, +74%), while width increased modestly (from 69.76-83.16 μm, +20%). In contrast, volume and surface area increased only slightly (from 2.20 × 10⁵-2.41 × 10⁵ μm³ +10%; from 2.00 × 10⁴-2.02 × 10⁴ μm², +1%, respectively). Once width expansion was considered, a more pronounced increase in pit volume and surface area was observed. Between 12 and 13 h, depth increased by 23% (from 79-91.7 μm), while width increased by 80% (from 69.76-125.49 μm), driving a fourfold increase in pit volume (from 2.41 × 10⁵-1.20 × 10⁶ μm³) and a 168% increase in surface area (from 2.41 × 10⁴ μm² to 6.45 × 10⁴ μm²).

Following the appearance of the lacy cover, pit growth accelerated sharply. Between 13 and 16 h, both volume and surface area increased exponentially, with a clear inflection between 13 and 15 h, as shown in Figure 14. The emergence of the lacy cover therefore marked a critical transition in pit growth dynamics.

According to the corrosion evaluation standards ASTM G46-2021 and GB 18590-2001, the maximum pit depth (D) as a function of time (t) can be expressed by a power-law relationship:

(1) $$ \begin{equation} \begin{aligned} D=K t^{\beta} \end{aligned} \end{equation} $$

where K is a proportional factor reflecting material, surface, and environmental conditions, and β is the pitting index, also dependent on the material and environment. When the 70 °C data were fitted to this model, not only depth but also surface area, volume, and maximum width were well described, with R² values of 0.979, 0.975, 0.984, and 0.953, respectively, as shown as red curves in Figure 14.

At 90 °C, the overall growth patterns were similar, but higher temperature markedly accelerated pit evolution. Before the lacy cover appeared, pit growth remained relatively slow, with a distinct turning point observed at approximately 6 h [Figure 15], which is characteristic of early-stage pitting behavior reported in the literature^[49]. From 4-5 h, pit width increased from 23.01-60.81 μm (+164%) and depth from 11.12-36.57 μm (+229%). From 5-6 h, width growth slowed (from 60.81-73.66 μm, +21%), while depth increased sharply (from 36.57-88.04 μm, +141%), highlighting the preferential deepening tendency of pits.

Once the lacy cover formed, pit growth entered a rapid expansion phase. From 6-7 h, surface area increased explosively from 2.09 × 10⁴-1.18 × 10⁶ μm² (+5,646%), and volume from 2.45 × 10⁵-7.80 × 10⁷ μm³ (+31,837%). Maximum width increased from 73.66-686.16 μm (+832%), while depth grew from 88.04-369.24 μm (319%). Although both width and depth expanded dramatically, the lateral growth rate was markedly higher than the vertical growth rate, which is consistent with the accelerated pit propagation and lateral spreading behavior associated with passive film degradation reported in the literature^[50]. With prolonged immersion, the lacy cover degraded, and the disparity between lateral and vertical growth gradually diminished.

Power-law fitting of the 90 °C data also yielded excellent agreement, with R² values of 0.990 (surface area), 0.999 (volume), 0.935 (maximum width), and 0.967 (depth) as shown as red curves in Figure 15.

Together, the two datasets demonstrate that surface area, volume, maximum width, and maximum depth can all be reliably described by a power-law model. Among these, pit width is the most accessible experimentally. However, surface observations may markedly underestimate true width due to the shielding effect of lacy covers, underscoring the importance of 3D reconstruction for accurate characterization.

Although the temporal evolution of pit depth has long been described empirically using a power-law relationship in standards such as ASTM G46 and GB 18590, these formulations do not explicitly address the physical origin of such scaling behavior, nor do they explain why multiple geometric parameters may follow similar functional forms. In the present work, the power-law fitting is not intended to serve as a mechanistic corrosion model, but rather as a phenomenological description of pit growth kinetics based on high-fidelity three-dimensional geometric data.

From a physical perspective, the emergence of power-law scaling can be rationalized by the evolution of rate-controlling processes during pit propagation. In the early stage of pit growth, pit geometry is shallow and open, allowing relatively unrestricted exchange of ionic species between the pit interior and the bulk solution. Under these conditions, pit deepening is limited by electrochemical dissolution at the pit bottom, while lateral expansion contributes minimally to volume increase. As the pit deepens, geometric confinement progressively restricts mass transport, leading to the accumulation of aggressive ions (e.g., Cl^-) and corrosion products within the pit cavity. This transition introduces diffusion-limited and ohmic resistance effects, which are widely recognized as key factors controlling steady-state pit growth.

The formation of a lacy cover further amplifies this confinement effect by partially shielding the pit interior from the external environment. Once such transport limitations dominate, pit growth becomes governed by coupled electrochemical kinetics and mass transport processes, resulting in non-linear time dependence that can be well approximated by power-law behavior. Under these conditions, different geometric descriptors—such as depth, width, surface area, and volume—are no longer independent but become geometrically correlated through the evolving pit morphology. Consequently, it is reasonable that these parameters exhibit similar temporal scaling trends, despite representing different aspects of pit geometry.

It should be emphasized that the driving force for pit growth in the present study is purely electrochemical in nature, arising from localized anodic dissolution sustained by aggressive chemistry within the pit environment. No external mechanical loading was applied, and stress-assisted mechanisms are therefore beyond the scope of this work. The fitted prefactors and exponents should thus be interpreted as effective parameters reflecting the combined influence of solution chemistry, temperature, and geometric confinement, rather than intrinsic material constants or direct indicators of a single rate-limiting mechanism.

For lacy covers formed under immersion at 70 and 90 °C, projections were made from the central opening of the cover and from the maximum contour enclosing all perforations onto the interior of the pit, as shown in Figures 16 and 17. In these 3D reconstructions, the green regions represent the projected pit space. Geometric measurements of the projected models were obtained [Tables 2 and 3] and compared with actual pit data, with the comparisons illustrated in Figures 18 and 19.

At 70 °C, the central opening of the early-stage lacy cover was relatively small, as shown in Figure 16B. Once the surrounding micropores became blocked by corrosion products, conventional observation methods could lead to substantial underestimation of pit dimensions. At this point, the projected volume accounted for only 10% of the actual pit volume, while the maximum width represented 33%. Using the maximum contour enclosing all holes provided improved estimates, corresponding to 72% of the actual pit width but only 50% of the actual pit volume, as shown in Figure 16C.

As corrosion progressed, micropores gradually expanded and merged, resulting in a larger central opening. At this stage, the projection from the central opening accounted for 68% of the actual pit width and 32% of the actual pit volume, as shown in Figure 16E. Simultaneously, projection from the maximum contour enclosing all holes corresponded to 82% of the actual pit width and 76% of the volume, as shown in Figure 16F. The comparative results are summarized in Figure 18.

In summary, newly formed lacy covers exhibit a strong shielding effect, substantially concealing both pit width and volume. Although this effect diminishes as pores expand and coalesce with continued corrosion, it remains non-negligible even in later stages.

When the temperature was increased to 90 °C, the pores became denser, as shown in Figure 17A. The elevated temperature not only accelerated pit growth but also promoted the development of the lacy cover. At 90 °C/7 h, the projection of the central opening of the lacy cover accounted for 60% of the actual maximum pit width and 31% of the actual pit volume, as shown in Figure 17B. The projection of the maximum contour enclosing all holes accounted for 82% of the actual pit width and 82% of the actual pit volume, as shown in Figure 17C. With increasing corrosion time, more pores gradually interconnected, ultimately leading to the collapse of the lacy cover, as shown in Figure 17D. At this stage, the projection of the central opening accounted for 76% of the actual pit width and 46% of the actual pit volume, as shown in Figure 17E, while the projection of the maximum contour enclosing all holes corresponded to 81% of the actual pit width and 65% of the actual pit volume, as shown in Figure 17F. The comparative results of these data are summarized in Figure 19.

As demonstrated by the comparative study in this paper, obtaining full-information data is essential for establishing high-accuracy predictive models. Full-information data provide all the necessary parameters of materials during service, especially for complex corrosion processes where traditional 2D surface data often fail to comprehensively reveal their internal evolution. Therefore, capturing and analyzing 3D data, particularly the 3D morphology and evolution of localized corrosion features like pitting, can substantially improve the precision and reliability of predictive models. However, the challenge in acquiring full-information data lies in the need for extensive material characterization. These characterizations typically require complex experimental procedures, high-precision equipment, and considerable time investment, making the process costly and labor-intensive.

With the ongoing development of smart material characterization technologies and equipment, especially breakthroughs in automation and high-throughput characterization, the acquisition of large amounts of material characterization data has become increasingly easier. Modern fully automated characterization devices not only complete large-scale experimental data collection in a relatively short time but also efficiently process and analyze vast amounts of data, effectively reducing the difficulty of obtaining full-information data. This advancement makes the collection of full-information data more feasible, providing a solid foundation for the precise characterization and performance prediction of materials. By further promoting and applying these technologies, we can more efficiently establish materials service evaluation and life prediction models in the future, driving the further development of digital twin and intelligent technologies.

In addition to the chemical environment, mechanical loading and microstructural length scales have been widely recognized as important factors influencing pit initiation and propagation, particularly when the characteristic dimensions of corrosion features approach critical microstructural scales. Under coupled mechanical–chemical conditions, local stress concentration at pit mouths or within subsurface regions can enhance localized dissolution, promote pit stabilization, and accelerate damage evolution. Recent studies have demonstrated that externally applied stress or residual stress can markedly alter pit growth kinetics and morphology by modifying the local electrochemical and mechanical fields, especially in small-scale or highly confined corrosion sites^[51,52].

It should be emphasized that the present work intentionally focuses on chemically driven pitting corrosion under stress-free conditions, without any externally applied mechanical loading. The primary objective of this study is to resolve the intrinsic three-dimensional geometric evolution of pits and the associated mass-transport confinement effects using high-resolution continuous-sectioning-based reconstruction. Stress-assisted corrosion mechanisms, including mechanically enhanced dissolution and stress concentration–induced pit stabilization, are therefore beyond the scope of the current experimental design. Consequently, the pit growth behavior reported here reflects the combined effects of electrochemical kinetics, solution chemistry, temperature, and geometric confinement, rather than chemo-mechanical coupling.

From a microstructural perspective, the relative scale between pit dimensions and microstructural features plays a critical role in determining the dominant damage mechanisms. When pit size or contact dimensions are comparable to grain size, inclusion spacing, or phase boundary lengths, microstructure-controlled subsurface deformation and strain localization may markedly influence damage evolution, as revealed by recent crystal plasticity and micromechanical modeling studies^[53]. In the present study, however, the characteristic pit dimensions during most growth stages are substantially larger than individual microstructural features of the Inconel 690 alloy. As a result, pit evolution is primarily governed by electrochemical dissolution and transport-limited processes, with microstructural effects playing a secondary role.

Nevertheless, the three-dimensional pit morphologies reconstructed in this work provide a realistic geometric basis for future investigations incorporating coupled mechanical loading and microstructural effects. By serving as high-fidelity geometric inputs, these data can be readily integrated into stress-assisted corrosion models or chemo-mechanical simulation frameworks to further explore the interactions among pit growth, local stress fields, and subsurface damage evolution under service-relevant conditions.

The present study repeatedly refers to service evaluation, life prediction, and digital twin applications in the context of pitting corrosion. It is therefore necessary to clarify the intended role and limitations of the reported dataset. The corrosion environment employed in this work (6% FeCl₃ + HCl) represents a highly aggressive medium commonly used to accelerate pitting corrosion and promote the formation of well-developed pit morphologies within experimentally accessible timescales. Such conditions are not intended to replicate the exact chemical environment of steam generator tubing in service, but rather to generate representative pit geometries that capture the full three-dimensional evolution of localized corrosion features.

From this perspective, the value of the present dataset lies not in direct life prediction under service conditions, but in providing high-fidelity geometric and morphological information that is typically inaccessible through conventional two-dimensional characterization methods. Parameters such as true pit depth, internal volume, surface area, and the shielding effect of lacy covers constitute essential geometric descriptors that are often missing or underestimated in service databases derived from surface observations alone. These descriptors can serve as critical input variables for corrosion growth models, damage evolution simulations, or digital twin frameworks that require realistic defect geometries.

With regard to uncertainty and statistical variability, it should be noted that the primary objective of this work is to demonstrate a data acquisition and analysis methodology rather than to establish statistically converged lifetime predictions. The number of reconstructed pits and the controlled experimental conditions allow for reliable identification of geometric growth trends and mechanistic transitions, such as the emergence of lacy covers as a turning point in pit growth. A comprehensive statistical treatment across large pit populations, including variability quantification and probabilistic assessment, would require substantially expanded datasets and is therefore beyond the scope of the present study.

Nevertheless, the reconstructed three-dimensional pit data provide a structural foundation that can be readily integrated into predictive modeling workflows. For example, the extracted geometric parameters can be incorporated into semi-empirical pit growth laws, transport-limited corrosion models, or finite-element-based damage simulations as geometry-informed inputs. In the context of digital twin applications, such data contribute to the defect geometry layer, enabling more realistic coupling between corrosion evolution, local environmental conditions, and subsequent mechanical integrity assessments. In this sense, the present work establishes a methodological and data-level basis for future service-oriented modeling, rather than delivering a standalone predictive tool.

The three-dimensional reconstruction strategy employed in this study is not limited to the specific material system or corrosion environment investigated here. Its universality originates from the fundamental principle of continuous cross-sectional information acquisition combined with digital reconstruction, which enables access to internal structural information that is inherently inaccessible to conventional two-dimensional characterization techniques.

From a methodological perspective, serial-sectioning-based 3D reconstruction is independent of the underlying damage mechanism or material class. By appropriately adjusting sectioning parameters, imaging modalities, and segmentation strategies, the same reconstruction framework can be applied to a wide range of material structure characterization problems, including localized corrosion, void and crack evolution, additive manufacturing defects, and heterogeneous microstructural features. In all these cases, the key advantage lies in the ability to resolve true three-dimensional geometries rather than relying on surface projections or apparent two-dimensional metrics.

In the context of the present work, pitting corrosion in Inconel 690 serves as a representative example demonstrating how full-field three-dimensional information can be systematically acquired and quantified. While the observed pit morphologies and growth characteristics are specific to the selected material and corrosive environment, the reconstruction workflow—comprising continuous sectioning, image acquisition, digital alignment, and geometric analysis—remains transferable to other material systems and degradation scenarios. The universality of the approach therefore resides in the reconstruction framework itself, rather than in material-specific outcomes.

Consequently, the serial-sectioning-based 3D reconstruction strategy provides a general pathway for obtaining comprehensive, geometry-resolved data suitable for structure–property–damage correlation studies. When combined with appropriate experimental design and data interpretation, this methodology enables consistent extraction of internal structural descriptors across different materials and damage processes, supporting its broad applicability in advanced material characterization.