Effect of Vanadium-Bearing Slag Aggregates on the Microstructure and Thermo-Mechanical Properties of Alumina Refractory Castables

Abstract

The incorporation of recycled metallurgical slags into refractory materials constitutes a promising approach to enhancing sustainability in the refractory industry. This study investigates the effect of vanadium-bearing slag aggregates as partial replacements for tabular alumina in castables and compares their behaviour with high-alumina and bauxite-based castables. Two vanadium-bearing slags with different mineralogical compositions were introduced in the 1–3 mm aggregate fraction with substitution up to 25 wt.%. Their effects on microstructure, thermo-mechanical performance, and corrosion resistance were evaluated. The introduction of vanadium-bearing slag significantly alters the microstructure of the castables, affecting their performance. Both slags displayed grains with higher porosity, microcracking, and heterogeneity compared with tabular alumina, but showed similarities to bauxite grains. Slag 1, enriched in calcium aluminate phases, provides limited mechanical strength but improved corrosion resistance due to improved bonding with the matrix. Slag 2, containing a higher spinel content, enhances mechanical strength, showing behaviour comparable with bauxite-based castables, particularly at 10 wt.% replacement. Vanadium is mainly present in metallic form and as Mg(Al,V)₂O₄ spinels in both slags. Upon firing, vanadium migrates toward the grain boundaries and reacts with the surrounding calcium aluminate phases to be incorporated in Ca(Al,V)₂O₄ and Ca(Al,V)₄O₇, while the spinel phase remains stable.

1. Introduction

The current environmental and economic landscape of the refractory materials industry is driving the transition towards better resource management, waste valorisation of spent refractories, and the development of new energy-efficient processes [1,2,3]. Global raw material demand is projected to nearly double by 2060 [4], raising concerns over resource depletion [5]. With the refractory demand also increasing [6], coupled with operational costs rising and freight inflation, industries are accelerating research on sourcing alternative raw materials. This aligns with the long-term goal of the European Green Deal requirements [7,8]. In castables, aggregates typically constitute 60–80% of the total volume [9,10], serving as the primary structural skeleton that bears the mechanical loads and determines the critical properties, such as strength, thermal shock resistance, and dimensional stability [11,12]. Tabular alumina (TA) is one of the most widely used raw materials for refractory applications due to its high corrosion resistance and refractoriness. However, its refining process (the Bayer process) has a critical environmental impact [13], generating 1–1.5 tons of highly alkaline red mud per ton of alumina produced [14]. So far, only 15% of red mud is reused, the majority being stockpiled [15]. An alternative is bauxite which contains 85–90 wt.% Al₂O₃, 5–10 wt.% SiO₂, and 3–4 wt.% Fe₂O₃. Less pure than TA, bauxite presents excellent refractoriness and chemical attack resistance [16]. In their study, Matinde et al. investigated the effect of reclaimed bauxite on andalusite-based refractory castables, and they found that 22 wt.% of substitution was a suitable amount while keeping similar properties [16]. At the same time, aggregate demand has reached 438 billion tonnes in 2024 and is predicted to rise to 454 billion tonnes in 2025, intensifying the pressure to find sustainable alternatives [17,18,19,20].

The large quantities of steel slag produced worldwide (≈20 Mt/year in Europe [21]) are being repurposed for a sustainable pathway to comply with environmental regulations limiting disposal waste [22,23]. Currently, metallurgical slags are primarily used as alternative binders due to their cementitious properties [8,24,25], and are partially used in road construction [26,27]. To maximise their resource utilisation, recent studies have explored slags as secondary aggregates in concrete production, reporting promising results for their use as fine aggregates [21,28,29]. A major barrier to the large-scale adoption of metallurgical aggregate residues in refractories is ensuring their compatibility with the existing formulations. The variability in slag composition, the presence of impurities, the nature of interfacial bonding, mismatched thermal expansion coefficients, and residual porosity pose significant technical challenges [21,30]. Nevertheless, a few studies have investigated the recycling of slag aggregates into refractory castables. For instance, Kumar et al. examined ferrochrome slag in bauxite-based castables and reported that the samples with slag and calcined bauxite exhibited good volumetric stability and improved thermo-mechanical properties [31]. Similarly, another study reported the feasibility of employing ferrochrome slag as aggregates up to 1200 °C, beyond which, liquid phase formation limited its application [23]. Although direct contact with molten metal is not recommended, the materials could withstand occasional melt droplets. These results indicate that slags are on a promising path toward reuse as refractory aggregates, although further research is needed to optimize their performance.

Vanadium is a common additive in steelmaking processes, which improves the wear resistance and corrosion protection of the final steel product [32]. Vanadium-bearing slag is a by-product of the steelmaking process formed during molten steel refining in basic oxygen furnaces (BOFs) or electric arc furnaces (EAFs) [33]. It contains a rich composition of oxides such as alumina (Al₂O₃), lime (CaO), and magnesia (MgO). During refining, vanadium migrates into the slag and is incorporated in different phases, depending on the processing conditions and raw materials [34]. Vanadium oxide typically accounts for 5–20% of the slag and is usually present as FeV₂O₄ spinels [35]. Vanadium compounds, especially vanadium pentoxide (V₂O₅), are highly toxic and carcinogenic, posing serious risks to both human health and the environment. This requires careful handling, controlled landfilling, and detailed phase characterisation of vanadium-bearing slags to refute the presence of V₂O₅ in the slags [36]. Considering these materials as aggregates in refractory applications is less well documented, as high-temperature firing conditions may promote reactions between the vanadium-bearing phases and the surrounding oxide matrix. In particular, interaction with CaO can lead to the formation of stable calcium vanadate phases depending on the amount of CaO, such as Ca₃(VO₄)₂, CaV₂O₅, CaV₂O₆, Ca₂V₂O₇, and Ca₃V₂O₈, with an unknown effect on refractories as yet [37]. According to the CALPHAD thermodynamic assessment of the CaO-V₂O₅ binary system [38], these phases have low melting temperatures, weakening the refractory’s hot strength and chemical durability, potentially promoting slag or molten steel corrosion.

Despite previous work on ferrochrome and other slags in refractories, the potential of vanadium-bearing slags in refractory castables remains largely unexplored. This study addresses this gap by evaluating their chemical stability, potential hazards, and mechanical performance in comparison with tabular alumina and bauxite aggregates in refractory castables.

2. Materials and Methods

2.1. Starting Materials

Two vanadium slags from high-vanadium steel production were used for the study. The vanadium slags are named Slag 1 and Slag 2. Slag 1 was obtained from BOF production (Calderys GmbH, Neuwied, Germany) and Slag 2 from a spent catalyst recycled in an electric arc furnace (EAF) (Carl Spaeter GmbH, Duisburg, Germany). The slags were crushed to a particle size ranging from 1 to 3 mm. The size distribution was obtained by sieving the grains for 10 min and repeating each measurement three times. For comparison, tabular alumina (99.5 wt.%, from Imerys, Lyon, France), a high-purity crushed alumina composed of sintered α-Al₂O₃ with large tabular crystals, and calcined bauxite (85% Al₂O₃, impurities: SiO₂, Fe₂O₃, TiO₂; Mineralmahlwerk Hamm GmbH, Hamm, Germany) were used as comparative materials with a size in the same range of 1–3 mm. Figure 1 shows the different raw materials investigated.

2.2. Aggregate Characterisation Methods

The main difficulty in using vanadium-bearing slags lies in their highly variable composition and the uncertain stability of the vanadium phases. These factors make preliminary studies essential, both to understand the nature of these by-products and to address concerns about the potential risks of the vanadium phases to human health and the environment. The chemical composition of the raw materials was measured using X-ray fluorescence (XRF, Spectro Xepos, Kleve, Germany). To ensure representative results, five different sampling spots were analysed for each slag. The crystalline phases were identified using an X-ray diffractometer (D8 Advance, Bruker, Karlsruhe, Germany) with a Cu-Kα radiation source (λ = 1.54059 Å) over a 2θ range of 5–90°. Diffraction data were processed with DiffracEVA software (version 6.0), and quantitative phase analysis was carried out using Rietveld refinement.

A helium pycnometer was used to determine the true density of the aggregates, defined as the ratio of mass to sample volume, excluding both open and closed pores. The open porosity was measured according to Archimedes’ principle (ASTM C20). The specific surface area of the aggregates was obtained using the Brunauer–Emmett–Teller (BET) method, which reflects the total surface area of the grain per unit of mass. The specific surface area is controlled by factors such as porosity, pore distribution, particle morphology and roughness. It strongly influences adsorption capacity of the grains, which, in practice, can increase the water demand during mixing.

Microstructural investigations of the aggregates were performed with a scanning electron microscope (Gemini SEM 500, Zeiss, Oberkochen, Germany) equipped with a backscattered electron detector and coupled with an energy dispersive X-ray spectrometer (EDS, XMax 80, Oxford Instruments, Abingdon, UK) for elemental composition analysis. Data acquisition and analysis were processed with Aztec software (version 4.0). Scanning electron microscopy (SEM) observations were conducted on the aggregates before and after firing in air at 1500 °C for 1 h.

The behaviour of refractory castables is strongly influenced by the morphology of their constituent aggregates. These morphological features are largely determined by the mineral phases present and the stress conditions applied during aggregate preparation [10]. To quantify these effects, roughness, roundness, and angularity were measured for both slags and the reference aggregates, enabling a direct comparison of their geometric and surface characteristics. The surface roughness of the grains was examined using a coaxial laser confocal microscope (VK-X200, Keyence, Osaka, Japan), which scanned the surface with a focused laser beam of 0.4 µm in radius [39]. The arithmetic mean roughness (Sa) was calculated according to Equation (1) [40].

$$S_a={\displaystyle \frac{1}{A}}{\iint }_A\mid z\left(x,y\right)\mid dxdy$$

(1)

where A is the measured surface area, and z(x,y) is the height deviation from the mean plane. There were 20 particles analysed for each slag/alumina. The scanning area was fixed at 700 × 500 µm using a 20× objective lens. To eliminate the pores in the calculation, Gaussian cutoff filtering was applied.

The grain shape parameters were further analysed using ImageJ software (version 1.54g) on the SEM microstructure images (Figure 2). The length-to-width ratio was measured to assess particle elongation, which affects orientation and packing behaviour within the castable. The roundness R was calculated according to Equation (2).

$$R={\displaystyle \frac{P^2}{4\times A\times \pi }}$$

(2)

where P is the grain perimeter, and A is the area of the grain. Roundness affects the rheological behaviour of fresh castables and its mechanical strength afterwards. Combining these measurements reveals how the grains’ characteristics influence the final refractory performance.

Nanoindentation was performed on slag grains to evaluate their hardness and conduct a comparative analysis. A nanoindenter (NHT3 step 300, Anton Paar, Graz, Austria) equipped with a triangular Berkovich tip was used on each material. In total, five matrices of 20 indents were performed on polished grain samples embedded in epoxy at random locations, with a 10 µm indentation spacing. The maximum load applied was 80 mN, with a 10 s pause for all the materials. The approaching speed was 1500 nm min⁻¹. These parameters were determined empirically to ensure successful indentation across the materials. Hardness was calculated from the load–displacement curves using Equation (3).

$$H={\displaystyle \frac{P}{A_c}}$$

(3)

where P is the applied load, and A_c is the projected contact area of the indentation. The data were processed with Python (version 3.13). Due to the heterogeneous nature of the slags and bauxite, the measured hardness values are primarily comparative.

2.3. Preparation of the Castables

Alumina refractory castables were formulated to investigate the incorporation of vanadium-bearing slags. In these mixes, the 1–3 mm aggregate fraction of tabular alumina was partially replaced by slags and bauxite. Reference castables containing only tabular alumina (TA) or bauxite are labelled REF-TA and REF-B, respectively (

Table 1. Formulations of the castables (vol.%).

Raw Material	Grain Size		Sample Code
		REF-TA	REF-B	S1-25	S2-25	S1-10	S2-10
Tabular Alumina	1–3 mm	34.2	34.2	25.7	25.7	30.8	30.8
	0.5–1 mm	9.8
	0.2–0.6 mm	9.8
	0–0.3 mm	17.1
	0–0.045 mm	9.8
Reactive Alumina	<0.001 mm	12.9
Secar 71		6.4
Slag 1	1–3 mm	-	-	8.6	-	3.4	-
Slag 2	1–3 mm	-	-	-	8.6	-	3.4
Water		5
Deflocculant	FS65	0.1

). REF-B differs from REF-TA by substituting the 1–3 mm fraction with 1–3 mm bauxite. To investigate the effect of slag substitution, 10 and 25 wt.% of the 1–3 mm aggregate fraction were replaced with Slag 1 and Slag 2. Although aggregate replacement is more meaningful in volumetric terms, converting these values to volume percentages (approximately 3.4 and 8.6 vol.%, respectively) had little impact on the final composition, as the true densities of Slag 1 and Slag 2 are very similar (3.02 and 3.06 g.cm⁻³). For clarity and readability, the sample codes refer to the nominal weight percentage of substitution. For instance, S1-10 corresponds to Slag 1, replacing 10 wt.% of the 1–3 mm fraction and S2-25 to Slag 2, replacing 25 wt.%. In the formulation, the alumina system consists of a fine reactive alumina powder (sub-micron, primary α-Al₂O₃ crystals) as a matrix, together with tabular alumina grains in graded size fractions from below 100 µm to 0.5–1 mm, ensuring a continuous particle size distribution. Each sample was prepared following the same procedure, which consists of mixing the dry raw materials for homogenisation (2 min), followed by addition of water and the dispersant, and further mixing for 3 min. The samples were fired at 1500 °C for 6 h in air. The maximum feasible slag substitution was determined empirically, as exceeding 25 wt.% in the 1–3 mm fraction prevented the formation of a cohesive castable. Additionally, regulatory limits on vanadium content restricted the final castables to a maximum of 0.1 wt.% vanadium content. Considering both the processing and safety constraints, the upper limit for slag replacement was set at 25 wt.% [41].

2.4. Castables’ Characterisation

The evaluation of the impact of incorporating slag aggregates on the performance of refractory castables was conducted through a set of tests to correlate material composition, microstructural development, and key functional properties. Phase evolution after firing of the slag-based and the reference castables were determined by XRD.

Dilatometric measurements were carried out using a horizontal dilatometer (Dilatometer Platinum Series L75, Linseis, Selb, Germany). Specimens were heated in air from room temperature up to 1450 °C at a rate of 10 °C min⁻¹. Pore structure influences mechanical strength and corrosion resistance in castables. Accordingly, open porosity and true density were measured using Archimedes’ method and a helium pycnometer. The mechanical properties were assessed through cold crushing strength (CCS) and cold modulus of rupture (CMOR) tests following the EN 993-5 and EN 993-6 standards, respectively [42,43]. Hot modulus of rupture (HMOR) was determined in air at 1400 °C with a 0.15 MPa s⁻¹ load, according to the EN 993-7 standard [44]. The reported results represent the average of three measured samples for each formulation.

Elastic properties were evaluated using resonant frequency damping analysis (RFDA), with an IMCE testing device equipped with an automatic impulse unit. This method, following ASTM E1876-22 [45], determines the resonant frequencies of the sample, from which Young’s modulus (E) and the shear modulus (G) can be calculated using a Poisson’s ratio of 0.2. Young’s modulus is determined from the flexural resonant frequency using Equation (4).

$$E=0.9465\left({\displaystyle \frac{m{\left(f_f\right)}^2}{b}}\right)\left({\displaystyle \frac{L^3}{t^3}}\right)T_1$$

(4)

where m represents the sample weight, $f_f$ is the flexural resonant frequency, t is the thickness, b is the width, L is the length of the sample, and $T_1$ is a dimensionless correction factor. The shear modulus G, measured in torsion mode, representing the resistance to shear deformation, is calculated with Equation (5).

$$G={\displaystyle \frac{4Lm{f}_t^2}{bt}}R$$

(5)

where m is the sample weight, $f_t$ is the torsional resonant frequency, L is the length of the sample, b is the width, t is the thickness, and R is the correction factor. The resonant frequencies vary with microstructure, pores, and cracks, thus providing information on the castables’ stiffness and elastic behaviour. Together, E and G describe the elastic behaviour of the castables, which is essential for performance under loads at room and high temperatures. To observe the microstructural effects of slag incorporation, SEM was also used on cross-sections prepared according to the protocol previously described.

Refractoriness under load (RUL) tests were assessed to determine the high-temperature mechanical stability of the castables according to EN 993-8 [46]. The tests were performed under a constant load of 0.2 MPa, and the deformation behaviour was recorded as a function of temperature.

To evaluate the corrosion behaviour of the castables in contact with steel, high-temperature contact experiments were carried out in a heating microscopy device (Carl Zeiss, under a flow of argon (100 L/h)) as schematised in Figure 3. Castable samples (8 × 8 × 3 mm) and cylindrical steel DC01 samples (3 mm height × 3 mm diameter) were placed in contact. DC01 steel was used as received, with a composition of <0.12 wt.% C, <0.60 wt.% Mn, <0.045 wt.% P, <0.045 wt.% S, and <0.03 wt.% Si. The steel samples were stored in isopropanol and polished immediately before testing. Heating was performed at 80 °C/min until 800 °C and then 10 °C/min up to 1600 °C, followed by a 3 min dwell time. After cooling, cross-sections were examined by SEM to characterize the interaction between steel and the castable and to assess possible vanadium diffusion from the slag-containing castables to the steel.

3. Results and Discussion

3.1. Slags’ Characterisation

The composition of the slags and reference materials is presented in

Table 2. Oxide composition of the two slags, the bauxite, and the tabular alumina.

	Composition (wt.%)
	Slag 1	Slag 2	Bauxite	Tabular Alumina
Al2O3	68.5 ± 0.05	71.2 ± 0.05	81.5	99.0
CaO	25.4 ± 0.03	12.8 ± 0.05	0.55	-
MgO	2.86 ± 0.07	12.4 ± 0.09	0.21	-
SiO2	1.34 ± 0.08	1.08 ± 0.05	11.2	0.40
V2O5	0.73 ± 0.02	1.13 ± 0.01	-	-
Na2O	0.24 ± 0 02	0.18 ± 0.01	0.15	-
Fe2O3	0.23 ± 0.01	0.32 ± 0.02	2.18	0.60
TiO2	0.13 ± 0.05	0.21 ± 0.00	3.78	-
SO3	0.04 ± 0	0.39 ± 0	0.02	-
K2O	0.50 ± 0.01	0.22 ± 0	0.22	-
MnO	0.03 ± 0	0.07 ± 0	0.02	-

. On average, Slag 1 contains about 0.73 wt.% of V₂O₅ and Slag 2 contains about 1.13 wt.% of V₂O₅. Bauxite contains a significant amount of SiO₂ and TiO₂, while tabular alumina is composed of 99.0 wt.% Al₂O₃ and sodium coming from the extraction of alumina during the Bayer process.

Figure 4 displays the crystalline phases identified by XRD. Slag 1 is dominated by CaAl₂O₄ (CA), whereas Slag 2 contains a higher fraction of CA₂ (CaAl₄O₇) and MgAl₂O₄. This compositional difference is critical, as CA is highly reactive with water, while CA₂ is significantly less reactive [47]. Tabular alumina exhibits the characteristic peaks of α-Al₂O₃, while bauxite consists of corundum and mullite (3Al₂O₃.2SiO₂) with minor amounts of rutile (TiO₂). Although the slags contain low concentrations of vanadium, its amounts were below the XRD detection limit, and therefore no corresponding peaks were observed.

Standard physical characterisations are summarised in

Table 3. Physical properties of the raw materials.

Raw Material	True Density g cm−3	Porosity %	Specific Surface Area m2 g−1
Slag 1	3.02	7.3	0.59 ± 0.03
Slag 2	3.06	2.1	0.24 ± 0.01
Tabular Alumina	3.92	0.9	1.00 ± 0.06
Bauxite	3.81	8.9	0.74 ± 0.04

. Slag 1 and Slag 2 have a similar true density but differ in porosity, with 7.3 and 2.1%, respectively. Tabular alumina shows the highest density (3.92 g cm⁻³) and lowest porosity (0.9%), consistent with its known resistance to infiltration. Bauxite displays an intermediate density but the highest open porosity, which may affect the castables’ density and mechanical performance. TA also exhibits the highest specific surface area (1.00 m² g⁻¹), implying higher water demand, whereas the lower SSA (specific surface area) of the slags require less water. Therefore, aggregates with higher SSA are expected to have a higher water demand, potentially leading to higher residual porosity in the castable.

Studying the aggregates before their use in castable formulations is important, as they typically constitute 60–80% of the total solid fraction. The particle size distribution (PSD) of the slags is presented in Figure 5. TA presents a slightly finer particle fraction than Slag 2 and a higher proportion of fines compared with Slag 1. Bauxite and Slag 2 show similar curves, indicating comparable overall grain sizes. The slag PSDs follow a trend consistent with the reference materials. The observed differences likely result from distinct manufacturing routes affecting the fracture patterns and producing various fractions of fine particles. Finer particles can enhance mix packing, but they may also increase the water demand.

The microstructures of the as-received slags are shown in Figure 6a,b for Slag 1 and Slag 2, respectively, with the associated spot EDS analyses listed in

Table 4. EDS point analysis results (at.%) associated with the slags’ microstructures before and after firing.

Point	Phase	O	Mg	Al	Ca	Si	S	V	Fe	Ti	Mn
1	Spinel Mg(Al,V)2O4	55.4	14.6	29.5	0.13	-	-	0.31	-	-
2	Metallic V + Si, Mn, Fe					25.5		71.1	1.8		1.6
3	Spinel Mg(Al,V)2O4	52.5	13.2	31.9				2.38
4	Goldmanite Ca3(Al,V,Ti)2(Si,Mg)3O12	54.6	2.80	21.0	7.00	4.30		6.43		3.64
5	Krotite-type (Ca12(Al,V,Si,S)14O33)	54.8	-	22.8	16.4	2.36	0.55	3.17	-	-
6	Spinel Mg(Al,V)2O4	56.2	14.2	27.9	0.87	-	-	0.57	0.32	-
7	Mayenite-type (Ca12(Al,V,Si,Ti,Fe)14O33	60.9	0.67	10.8	16.6	1.05	-	1.85	0.92	7.21
8	Krotite-type	54.3	-	22.0	15.6	4.23	-	3.87	-	-

. Vanadium is detected in both slags as metallic spherical droplets and within oxide phases, identified in MgAl₂O₄ spinel. In Slag 1, Point 1 (Table 4) associated with spinel contains up to 0.31 at.% vanadium, with an unclear influence on the spinel’s structure. Slag 1 is mainly composed of CA, CA₂, and a small amount of Mg(Al,V)₂O₄, while Slag 2 is dominated by CA₂ and Mg(Al,V)₂O₄, as confirmed by XRD. Slag 2 also shows lamella-shaped phases (Point 4, Table 4) containing 6.5 at.% vanadium, likely corresponding to goldmanite (Ca₃(Al,V,Ti)₂(Si,Mg)₃O₁₂), a garnet-type silicate phase. The higher spinel content in Slag 2 could suggest better mechanical performance in castable applications, as spinel has a high melting point (2135 °C) and resistance to chemical attack.

The effect of temperature on the vanadium phase evolution was monitored by firing the slags at 1500 °C for 1 h in air. The resulting microstructures are presented in Figure 6c,d for Slag 1 and Slag 2, respectively. Metallic vanadium is no longer observed, indicating complete oxidation. At high temperatures, vanadium is present predominantly as V³⁺ and reacts with the surrounding oxides [41]. Figure 6c,d and the EDS results indicate that vanadium concentrates in calcium aluminate phases, particularly krotite (CA), which is stable at 1500 °C. As shown in the Al₂O₃–CaO–MgO ternary phase diagram at 1500 °C in Figure 7, generated with FactSage (FToxid, FactPS databases), Slag 1 and 2 (red and purple dot respectively) are in an equilibrium region where CA, CA₂, and MgAl₂O₄ are the main stable phases. This is supported by the SEM/EDS observations. In both samples, vanadium is incorporated into CaAl₂O₄ forming Ca(Al,V)₂O₄, with V³⁺ substituting for Al³⁺. This substitution is associated with diffusion towards the grain boundaries, identified by a bright interfacial layer. The spinel structure resists the incorporation of trivalent, tetravalent, and pentavalent ions due to its stable octahedral network. Krotite, with a monoclinic structure, allows V³⁺ to occupy tetrahedral Al sites. At high temperatures, vanadium preferentially enters calcium-rich phases, in agreement with the reported diffusion-controlled formation of calcium vanadates in V-slag and CaO systems [48]. The presence of Mg(Al,V)₂O₄ spinel remains stable after firing (ternary diagram, Figure 7) [49]. These micrographs demonstrate that vanadium is redistributed from metallic form into the existing oxide phases of the Al₂O₃–CaO–MgO system, rather than creating new phases. In the ternary system, the phase assemblage is mainly controlled by the overall slag chemistry and would be similar even in the absence of vanadium. Thus, vanadium slightly modifies the existing calcium aluminate and spinel phases.

Aggregate morphology was analysed from SEM micrographs of 50 individual grains per material (Figure 8). Slag aggregates and bauxite show internal porosity and microcracks, which can reduce mechanical strength and compromise thermal shock resistance. Tabular alumina shows homogeneous, elongated grains with uniformly distributed closed pores. This observation is consistent with its narrow roundness distribution. Bauxite grains display morphological heterogeneity, ranging from nearly equiaxed to distinctly elongated, with a high proportion of open and closed pores that may lower high-temperature corrosion resistance. Slag aggregates exhibit sharp and angular grains with a large number of cracks. The micrographs reveal internal heterogeneity associated with the presence of multiple phases and a relatively high density of microcracks compared with TA and bauxite.

The surface roughness measurements of the raw materials presented in Figure 9 indicate similar values ranging from 1.421 µm for bauxite to 2.515 µm for Slag 2. The associated error bars reflect the heterogeneity of the slags and the challenges in characterising roughness accurately, as the parameter can be influenced by grain shape factors such as roundness and angularity. The relatively higher roughness observed for Slag 2 is attributed to its fractured crystalline microstructure, whereas the smoother surface of the bauxite sample corresponds to its predominantly amorphous phases.

Shape parameters strongly influence the slurry rheology, packing, and mechanical performance of refractory castables. Among them, the roundness and length–width ratio (L/W) distinguish geometric elongation from surface irregularity (Figure 10a). The L/W ratio quantifies particle elongation, with values approaching 1 indicating more equiaxed grains. All aggregates exhibit mean L/W values around 1.6, denoting moderately elongated grains, where the major axis is roughly 60% longer than the minor axis. Given the similar L/W ratios for all materials, this parameter alone cannot explain the mechanical differences discussed later. Roundness, as defined by Equation (2), quantifies angularity, with higher values reflecting rougher surfaces. TA and bauxite exhibit comparable mean values (1.7), whereas Slag 1 and Slag 2 display slightly superior values (1.89 and 1.80, respectively), consistent with the more irregular morphologies observed in Figure 8. Such angularity, generally correlated with higher surface roughness, tends to raise the water demand. The morphological distributions shown in Figure 10b,c further reveal that bauxite presents a broad L/W range (1.2–2.0), reflecting its morphological heterogeneity. Both slags reveal a main L/W in the 1.4–1.6 range, while tabular alumina is found predominantly in the 1.6–1.8 range. The similarity between the two slags reflects their analogous solidification and crushing processes. The slightly more angular Slag 2 may enhance interlocking (microstructural rigidity). Previous work [50] demonstrated improved flowability (up to 10%) for aggregates with more equiaxed particles (L/W = 1).

The nanoindentation hardness results of the investigated aggregates are summarised in Figure 11, with the hardness distribution shown in Figure 11a and representative load-depth curves in Figure 11b. Because Slag 2 is highly heterogeneous, hardness values were evaluated separately for the calcium aluminate and spinel phases. An overall average hardness was also calculated. Tabular alumina exhibits the highest hardness, with a narrow distribution centred at 26.8 GPa, reflecting its single-phase corundum microstructure and high uniformity. This result is consistent with reported nanoindentation hardness values for dense α-Al₂O₃, ranging between 23 and 30 GPa, depending on the applied load (1000 µN and 10,000 µN, respectively) [51]. In contrast, bauxite displays a broad hardness range (10 to 30 GPa) with an average value of 17.5 GPa. This is consistent with its multiphase nature consisting of corundum, mullite, and amorphous phases. Slag aggregates demonstrate significantly lower hardness values. Slag 1 shows an average hardness of 11.4 GPa with limited scatter, indicating a predominance of soft CA phases. In Slag 2, the CA phase exhibits similarly low hardness with 11.0 GPa, while the spinel phase reaches higher values of about 20 GPa. Geng et al. measured a hardness of 19.79 GPa for MgAl₂O₄ grain, correlating well with the values obtained in this investigation [52]. Considering all indents, Slag 2 shows an intermediate average hardness of 16.4 GPa. The corresponding load–depth curves shown in Figure 11b corroborate the hardness measurements. Softer CA phases show larger indentation depths under identical loads, indicating enhanced plastic deformation, while spinel and alumina show minimal penetration. These differences highlight the strong dependence of the local mechanical response on phase composition. The observed hardness contrasts are expected to affect castables’ performance, as aggregates form the material’s load-bearing framework.

3.2. Castables’ Characterisation

Figure 12 illustrates the XRD patterns of the fired castables. Mainly α-Al₂O₃ is present in all samples due to the high amount of alumina in the formulation. CA₆ is detected in all samples as a secondary phase formed during firing. Spinel MgAl₂O₄ is detected in castables containing Slag 2. The bauxite-based sample displays Fe₂O₃ and CaAl₂Si₂O₈, coming from the bauxite grains.

The thermal expansion results of the sintered castables, presented in Figure 13, show nearly linear expansion during heating. The expansion coefficient (α), measured from room temperature to 1450 °C, is comparable for slag-containing castables and Ref-TA, which shows the highest thermal expansion coefficient (9.35 × 10⁻⁶ K⁻¹), consistent with its higher sintering activity, promoting stronger particle bonding through CA₆ formation and densification of α-Al₂O₃ grains during firing [53]. Ref-B shows a lower α (8.47 × 10⁻⁶ K⁻¹), attributed to its silica content forming lower expansion phases during firing. The slightly decreased CTE of slag-containing castables compared with Ref-TA is associated with the lower expansion of calcium aluminate and the higher open porosity, as observed in the results in Table 4, which give more free space for expansion and act as a stress relief zone. However, Slag 2-containing castables tend to show higher expansion than Slag 1 formulations. This behaviour may be related to the bonding interaction between CA₆ and spinel grains, which is highly present in Slag 2 [54].

Table 5. Physical and mechanical properties of samples after firing at 1500 °C.

Sample	Open Porosity %	True Density g/cm3	CCS (MPa)	CMOR (MPa)	HMOR 1400 °C (MPa)	E Modulus (GPa)	G Modulus (GPa)
REF-TA	17.5	4.02	259.0 ± 16	42.5 ± 2.2	23.8 ± 1.6	133 ± 8.5	59.4 ± 1.8
REF-Bauxite	17.8	3.98	225.3 ± 9.2	34.8 ± 2.2	1.30 ± 0.18	159 ± 4.6	16.2 ± 0.3
S1-10	20.9	3.86	95.38 ± 23	21.8 ± 2.1	7.49 ± 1.89	122 ± 8.2	13.0 ± 0.6
S1-25	22.0	3.86	81.57 ± 11	9.25 ± 1.2	4.69± 0.23	54.7 ± 2.5	21.2 ± 1.7
S2-10	20.9	3.93	204.5 ± 23	24.8 ± 3.5	12.8 ± 1.25	126 ± 1.6	13.6 ± 0.3
S2-25	24.0	3.89	50.10 ± 3.5	12.1 ± 2.4	3.4± 1.48	70.0 ± 3.8	33.1 ± 0.3

summarises the physical and mechanical properties of the castables fired at 1500 °C. Ref-TA exhibits the lowest open porosity (17.5%) and the highest strength and stiffness, while the slag-containing castables and Ref-B show a systematic increase in porosity accompanied by reduced mechanical performance, with the effect becoming more pronounced at higher substitution levels. Despite only a small increase in porosity, Ref-B already shows a noticeable decrease in CCS and CMOR (13.1% and 18.1%, respectively). The introduction of slag aggregates results in a pronounced decrease in mechanical strength, particularly for Slag 1. At 10 wt.% substitution, S1-10 reaches only 95.4 MPa in CCS and 21.8 MPa in MOR, while S2-10 performs considerably better, achieving a CCS of 205 MPa, close to that of Ref-B (225 MPa). This improvement is attributed to its higher true density (3.93 g.cm⁻³) and spinel content, which contribute to better structural integrity and enhance strength [50]. The inferior performance of Slag 1 is due to interfacial reactions between its Ca-rich aggregates and the alumina matrix, leading to reaction rims, internal voids, and aggregate weakening, further intensified by its lower hardness (Figure 11).

Increasing the slag content to 25 wt.% significantly deteriorates mechanical performance, as expected. For Slag 2, CCS drops by nearly 75%, and both slags exhibit approximately 50% reductions in CMOR, mainly caused by excessive pore formation and reduced interfacial bonding. Aggregate morphology also influences packing efficiency, as the smooth surface of tabular alumina (Figure 8) favours dense packing, while the rough and angular slag particles increase interstitial voids, reducing densification, as also highlighted by Wu et al. [10]. High-temperature mechanical behaviour follows similar trends. Ref-TA maintains a high HMOR at 1400 °C (23.8 MPa), whereas Ref-B loses almost all its mechanical integrity (1.30 MPa) due to liquid phase formation. Among the slag-containing castables, S2-10 shows the highest HMOR (12.8 MPa), indicating enhanced thermo-mechanical stability related to its spinel-rich composition. The dynamic elastic properties measured by RFDA depict similar results, with elastic (E) and shear moduli (G) decreasing with addition of slag as a consequence of increased microcracking and reduced matrix stiffness. Although S2-25 displays an unexpectedly high shear modulus (33 GPa), its high porosity limits its overall mechanical performance.

Slag addition increases porosity and reduces the thermo-mechanical properties of alumina castables [51]. However, the performance strongly depends on the slag’s chemistry and substitution level. Slag 2, particularly at 10 wt.% substitution, represent a viable recycled aggregate, while Slag 1 shows limited usability in the as-received state.

Figure 14 and Figure 15 show the microstructures of S1-25 and S2-25, respectively, after sintering at 1500 °C. The micrographs in Figure 15a,b illustrate the overall distribution of Slag 2 aggregates within the alumina matrix. Slag grains exhibit heterogeneous behaviour, some remain largely unreactive with irregular shapes and interfacial microcracks (Figure 15a), resulting in less pronounced bonding between aggregates and the matrix [55]. The slag also presents grains partially reacting with the matrix, forming CA₆ at the interface through diffusion of CA₂ from the slag (Figure 14c for Slag 1 and Figure 15c for Slag 2). This reaction enhances fracture resistance by crack bridging and energy dissipation, in good correlation with the XRD and ternary diagram predictions. Moreover, S1-25 with Slag 1 exhibits more extensive reaction rims and decohesion around the slag grain, generating porosity that compromises mechanical strength (CCS, MOR, and HMOR), resulting from a rapid phase transformation from CA to CA₆. Metallic vanadium inclusions from slags oxidize to form krotite-type and grossite-type phases Ca(Al,V)₂O₄ and Ca(Al,V)₄O₇, further reducing the aggregates’ strength, as observed in Figure 6. Tabular alumina remains intact and presents minimal microcracking and stable interfaces with the matrix, while bauxite-based castables show extensive microcracks at the interface. The bauxite castable (Figure 16b) also displays the presence of CaAl₂Si₂O₈, which is detrimental to refractoriness, in addition to the large amount of pores. From this analysis, it has been observed that the combination of interfacial microcracks, porosity, and phase evolution explains the differences in macroscopic mechanical properties among castables with slag, tabular alumina, and bauxite.

The refractoriness under load (RUL) results are presented in Figure 17. All castables exhibit linear thermal expansion up to 1200 °C, followed by divergent behaviour. The bauxite reference softens first, with Tεmax at 1300 °C, attributed to the formation of a low-melting CaAl₂Si₂O₈ glassy phase promoted by SiO₂, limiting its application where refractories are subjected to high temperatures or aggressive environments [53] (Figure 16). Castable containing Slag 2 shows a short plateau at 1356 (S2-10) and 1270 °C (S2-25), followed by a sharp increase in deformation (ε), likely due to the volumetric increase in needle-like calcium aluminate phases and vanadium’s migration to grain boundaries, forming krotite–vanadium reaction rims (Figure 15) [54].

Despite higher deformation, Slag 2-containing castables reach higher maximum temperatures, meaning improved high-temperature resistance under load. This is in correlation with the dilatometry results showing slightly higher thermal expansion compared with Slag 1, indicating better bonding thanks to CA₆ forming within the spinel interface. Nevertheless, such phase transformations and microstructural changes can negatively affect mechanical performance. For instance, S2-25 shows reduced CCS and CMOR (Table 5), whereas S2-10 shows good mechanical properties, highlighting a beneficial effect at lower substitution levels. In comparison, castables containing Slag 1 exhibit continuous and smooth expansion curves, with T_εmax at 1464 °C (S1-10) and 1355 °C (S1-25), indicative of limited phase transformations. Their comparatively lower resistance under load at high temperatures, relative to Slag 2-containing castables, can be attributed to differences in their phase composition, packing, and aggregate hardness.

Figure 18, Figure 19, Figure 20 and Figure 21 show SEM cross-sections of the castables after corrosion testing at 1650 °C in air. The reference castable containing only tabular alumina (Figure 18a) shows limited steel penetration, with a maximum depth of approximately 250 µm, attributed to its dense microstructure and the formation of a CA₆ layer at the aggregate–matrix interface acting as a protective barrier. On the other hand, S1-10 and S2-10 display deeper penetration, reaching about 500 µm and 600 µm, respectively (Figure 19 and Figure 20). Their higher porosity promotes steel infiltration, especially along the aggregate boundaries, where interfacial cracking is evident (Figure 19b). Between the two slag compositions, Slag 1 provides slightly improved resistance compared with Slag 2, likely due to its higher specific surface area, which enhances bonding with the matrix. In Al₂O₃–SiC–C castables, differences in aggregate structure were shown to strongly affect molten slag’s resistance, demonstrating that the aggregate microstructure itself plays a role in the response of refractory systems at high temperatures [51]. Unlike the uncorroded alumina grains in the reference sample (Figure 18a), slag aggregates partially react with molten steel, losing their functions of skeleton and resistance. The bauxite-based reference exhibits the poorest performance, with penetration depths around 900 µm, consistent with mullite formation. EDS mapping reveals that the infiltrated zone in Ref-TA consists mainly of (Fe,Mn)Al₂O₄ spinels formed by reaction between the molten steel and alumina. For both samples with slag, vanadium is incorporated into the spinel phase as (Fe,Mn)(Al,V)₂O₄, without evidence of vanadium transferring to the steel. Local Fe₃O₄ formation is also detected on S1-10 due to oxidation of metallic iron. Additionally, the reaction between slag aggregates and molten steel leads to the formation of a viscous interfacial layer (Figure 19a and Figure 20a), which may locally limit steel’s penetration compared with bauxite-based castable. Overall, these observations suggest that Slag 1 provides improved corrosion resistance compared with Slag 2. However, Slag 1 shows lower mechanical performance, highlighting a trade-off between corrosion resistance and mechanical properties.

4. Conclusions

Tabular alumina is a high-purity yet costly raw material whose production demands large mineral resources. To address the expected depletion of virgin raw material in the coming decade, this study evaluated the feasibility of using vanadium-bearing slag aggregates as sustainable substitutes for conventional alumina aggregates in refractory castables. High-alumina castables were formulated by replacing the 1–3 mm aggregate fraction with 10 wt.% and 25 wt.% of two vanadium-bearing slags with different mineralogical compositions, referred to as Slag 1 and Slag 2. The results indicate that slag chemistry and substitution level strongly influence castables’ performance, with a trade-off between mechanical strength and corrosion resistance. Slag 1, characterised by a higher calcium aluminate content, exhibits slightly better corrosion resistance against molten metal, attributed to its interfacial reactivity and the formation of a viscous reaction layer that limits steel’s penetration, despite the lower mechanical strength. Increasing the slag content to 25 wt.% leads to excessive porosity and interfacial degradation for both slags, resulting in a pronounced deterioration of the mechanical properties. However, Slag 2 up to 10 wt.% substitution has shown promising mechanical properties, similar to bauxite-based castables. Metallic vanadium present in the as-received slags oxidised to form krotite and grossite-type phases, Ca(Al,V)₂O₄ and Ca(Al,V)₄O_7, respectively. They both contained a stable vanadium–spinel Mg(Al,V)₂O₄ phase. The content of vanadium in the slag is not the limiting factor influencing the properties. Overall, the results demonstrate that vanadium-bearing slags can serve as partial substitutes for alumina aggregates, offering a sustainable route for the valorisation of industrial residues, aligning with circular economy principles. Their use as load-bearing aggregates must carefully address issues related to phase reactivity, porosity and mechanical compromise. Future work could address strategies to mitigate these limitations, including pre-treatments of slags, particle size optimisation, or selective particle sorting by heavy-liquid separation.