The sulfide capacity is a measure for the sulfur-extracting capacity of the slag phase in a situation where the slag and the metal or slag and gas phase are in thermodynamic equilibrium. The sulfide capacity of the slag phase can be defined based on either one of the following reactions[
7]:
$$ \frac{1}{2}\{ {\text{S}}_{2} \} + ({\text{O}}^{2 - } ) = ({\text{S}}^{2 - } ) + \frac{1}{2}\{ {\text{O}}_{2} \}, $$
(14)
$$ [{\text{S}}] + ({\text{O}}^{2 - } ) = ({\text{S}}^{2 - } ) + [{\text{O}}]. $$
(15)
The expression for the sulfide capacity of the slag phase can be derived based on the equilibrium constants aforementioned:
$$ C_{\text{S}} = \left( {{\text{pct}}\,{\text{S}}} \right)\sqrt {\frac{{p_{{\{ {\text{O}}_{2} \} }} }}{{p_{{\{ {\text{S}}_{2} \} }} }}}, $$
(16)
$$ C_{\text{S}}^{\prime} = \left( {{\text{pct}}\,{\text{S}}} \right) \frac{{a_{{[{\text{O}}]}}^{\text{H}} }}{{a_{{[{\text{S}}]}}^{\text{H}} }}, $$
(17)
where
\( C_{\text{S}}^{\prime} \) is the sulfide capacity of the slag phase defined based on the metal–slag equilibrium and
\( a_{{[{\text{S}}]}}^{\text{H}} \) is the activity of sulfur in the metal phase and
pi is the partial pressure of a compound
i. The relation can be simplified further to Reference
7:
$$ { \log }_{10} C_{\text{S}}^{\prime} = { \log }_{10} C_{\text{S}} - \frac{935}{T} + 1.375. $$
(18)
In reference to the expression of equilibrium distribution of sulfur with respect to slag and metal phases, the formulation for the sulfide capacity of the slag phase with respect to sulfur partition ratio can be given as follows:
$$ \log_{10} C_{\text{S}} = \log_{10} L_{\text{S}} + \log_{10} a_{{[{\text{O}}]}}^{\text{H}} + \frac{935}{T} - 1.375 - \log_{10} f_{{[{\text{S}}]}}^{\text{H}} , $$
(19)
where
\( f_{{[{\text{S}}]}}^{\text{H}} \) is the activity coefficient of sulfur in the metal phase.
A vast amount of semi-empirical or theoretical models have been developed for predicting the sulfide capacity of the slag phase.[
6‐
30] The theoretical models intend to describe the effect of chemical interactions between the slag ions and molecules,[
9,
12,
20,
21] whereas semi-empirical correlations use data-driven fitting techniques, namely, the multiple linear regression or artificial neural networks, to identify the effect of slag composition and system properties on the sulfide capacity.[
6‐
8,
10,
11,
13‐
20,
23‐
30] The advantage of semi-empirical models compared to theoretical ones is a lower computational complexity and usually a more sensible model formulation, thus making them more applicable as a part of dynamic process models. In the case of semi-empirical models, probably the most common variable that is used for capturing the interactions between the slag composition, system properties, and sulfide capacity is the optical basicity of the slag.[
7,
8,
10,
11,
13] The optical basicity of the slag can be expressed in such a way that each of the cation fractions is weighted by the corresponding optical basicity of the compound[
8]:
$$ \Lambda = \mathop \sum \limits_{i = 1}^{k} \Lambda_{i} \hat{X}_{i} , $$
(20)
where
\( \hat{X}_{i} \) is the cation fraction of the component
i in the slag phase and
\( \Lambda \) is the optical basicity of the slag phase. The cation fraction of a slag component
i is given as[
8]:
$$ \hat{X}_{i} = \frac{{nX_{i} }}{{\mathop \sum \nolimits_{i = 1}^{k} nX_{i} }}, $$
(21)
where
n is the number of oxygen atoms in the corresponding component and
k is the number of components in the slag phase. To identify the cross-interaction of temperature and chemical composition on the sulfide capacity of the slag phase, Sosinsky and Sommerville[
8] expanded the concept by combining the data gathered from multiple sources. In their study, the prediction model for sulfide capacity of the slag phase is given as[
8]
$$ { \log }_{10} C_{\text{S}} = \left( {\frac{22690 - 54640\Lambda }{T}} \right) + 43.6\Lambda - 25.2, $$
(22)
where
\( C_{\text{S}} \) is the sulfide capacity of the slag phase;
\( \Lambda \) is the optical basicity of the slag phase; and
T is temperature of the slag. Despite applicability for wide range of different slag compositions and temperatures, the Sosinsky and Sommerville model has often been found to be ill-suited for predicting the sulfide capacities of Na
2O-SiO
2[
10,
11,
13] and CaO-SiO
2-Na
2O systems[
6] as well as the sulfide capacity in particular of slag systems in which CaO content is well above the saturation limit.[
8] Later on, Young
et al.[
7] introduced a piecewise-defined quadratic formulation of sulfide capacity with respect to optical basicity, which is given as[
7]
$$ { \log }_{10} C_{\text{S}} = \left\{ {\begin{array}{*{20}l} { - 23.82\Lambda^{2} + 42.84\Lambda - \frac{11710}{T} - 0.02 \cdot \left( {{\text{SiO}}_{2} } \right) - 0.02 \left( {{\text{Al}}_{2} {\text{O}}_{3} } \right) - 13.913,\quad \Lambda < 0.8 } \\ {0.72\Lambda^{2} + 0.48\Lambda - \frac{{\left( {1697 - 2587\Lambda } \right)}}{T} + 0.02 \cdot \left( {{\text{SiO}}_{2} } \right) - 0.0005 \left( {{\text{Al}}_{2} {\text{O}}_{3} } \right) - 0.63,\quad \Lambda \ge 0.8 } \\ \end{array} } \right. $$
(23)
Despite simplifications in the model formulation, the model given in Young
et al.[
7] performs reasonably well in validation with an external data set. A common problem of the model formulations is that models employing the concept of optical basicity do not extrapolate well to slag systems outside the studied composition range. In fact, there are numerous slag compositions that have nearly equal optical basicities, but are known to have unequal sulfide capacities; for instance, there is a large difference in the sulfide capacities of CaO-SiO
2 and Na
2O-SiO
2 systems that cannot be explained by differences in optical basicity.[
6] To address this shortcoming, a thermostatistical model, often referred as the KTH model has been proposed for a thoroughly molten slag. The model is based on the assumption that the sulfide capacity of the slag is defined by equilibrium expression for the pure liquid FeO and with the experimental parameter
\( \varepsilon \) that is dependent on the composition and temperature of the slag.[
14‐
17] The ratio of the free oxygen content and the activity coefficient of the dissolved sulfides in the slag is given in the model with a following relation[
17]:
$$ \frac{{a_{{{\text{O}}^{2 - } }} }}{{f_{{{\text{S}}^{2 - } }} }} = \exp \left( { - \frac{\varepsilon }{RT}} \right), $$
(24)
where
\( \varepsilon \) is a model parameter that is linearly dependent on the molar fractions of the slag compounds as well as on the interactions of cation fractions of slag compounds and temperature of the slag. Thus, the expression for the parameter can be written as[
14]
$$ \varepsilon = \mathop \sum \nolimits X_{i} \varepsilon_{i} + \varepsilon_{\text{mix}}. $$
(25)
By assuming that the Ca
2+ content has a quadratic interaction with the sulfide capacity, the parameterized expression for the
\( \varepsilon \) in the case of system under study would be
$$ \varepsilon = X_{\text{CaO}} \varepsilon_{{{\text{Ca}}^{2 + } }} + X_{{{\text{Na}}_{2} {\text{O}}}} \varepsilon_{{{\text{Na}}^{ + } }} + X_{{{\text{SiO}}_{2} }} \varepsilon_{{{\text{Si}}^{4 + } }} + y^{{{\text{Ca}}^{2 + } }} y^{{{\text{Na}}^{ + } }} \left( {b_{0} + b_{1} T} \right) + y^{{{\text{Ca}}^{2 + } }} y^{{{\text{Si}}^{4 + } }} \left( {b_{2} + b_{3} T} \right) + y^{{{\text{Na}}^{ + } }} y^{{{\text{Si}}^{4 + } }} \left( {b_{4} + b_{5} T} \right) + y^{{{\text{Ca}}^{2 + } }} y^{{{\text{Si}}^{4 + } }} y^{{{\text{Na}}^{ + } }} \left( {b_{6} + b_{7} T + b_{8} y^{{{\text{Ca}}^{2 + } }} } \right). $$
(26)
The advantage of the approach is that it describes all the possible cation interactions for the slag compounds and has been proven fairly accurate.[
14‐
17] However, the previous studies do not address the CaO-SiO
2-Na
2O system, and therefore some of the parameters have not been previously identified. For this reason, the performance of the model is evaluated by
making use of the parameters given in literature[
14‐
17] as well as with the parameters that are identified based on the sulfide capacity measurements for Na
2O-SiO
2 and CaO-SiO
2-Na
2O slag systems. The data for the identification are extracted and combined from References
6,
10,
11, and
31.
The effect of sodium oxide (Na
2O) on the rate of desulfurization
via transitory and permanent phase contact and on the sulfide capacity of the slag has been reported in several studies.[
2‐
5,
10,
11,
13,
30,
31] It has been concluded that the sulfide capacities of Na
2O/SiO
2-based slags are higher than those of CaO/SiO
2-based slags[
3,
5‐
7] and the rate of desulfurization increases with the increase of the Na
2O content in the slag.[
2,
3] The activity of CaO has been found to be increased with the activity of Na
2O in the slag phase,[
30,
32] which can be associated to increased dissolved fraction of CaO. As regards the sulfide capacity of Na
2O-SiO
2 and CaO-SiO
2-Na
2O-systems, several authors suggest that the Na
2O/SiO
2 ratio is the strongest predictor variable.[
6,
13] In the studies of Chan and Fruehan[
10,
11] and Kunisada and Iwai,[
13] it was observed that the sulfide capacity of a binary Na
2O-SiO
2 slag system in different temperatures can be expressed with the following correlations:
$$ { \log }_{10} C_{\text{S}} = b_{1} \Lambda + b_{0} = \left\{ {\begin{array}{*{20}c} {11.66\Lambda - 11.86 ^{[10]} \quad T = 1423.15\,{\text{K}} } \\ {11.86\Lambda - 11.33 ^{{\left[ {11} \right]}} \quad T = 1673.15\,{\text{K}}} \\ {27.00\Lambda - 21.20^{[13]} \quad T = 1773.15\,{\text{K}}} \\ \end{array} } \right. ,$$
(27)
where
b1 and
b0 are experimentally determined regression coefficients fitted as a function of system temperature. However, as the experimental results are fitted for the binary Na
2O-SiO
2-system, the coefficient related to the interaction of optical basicity and sulfide capacity does not include the effect of various basic compounds,
e.g., CaO, on sulfide capacity. To include the effect of CaO on the sulfur partition ratio for the CaO-SiO
2-Na
2O system, van Niekerk and Dippenaar[
6] proposed the following correlation in the CO atmosphere[
6]:
$$ { \log }_{10} L_{\text{S}} = 1.01\frac{{({\text{Na}}_{2} {\text{O}})}}{{({\text{SiO}}_{2} )}} - 0.07\frac{{\left( {\text{CaO}} \right)}}{{\left( {{\text{Na}}_{2} {\text{O}}} \right)}} + 0.37. $$
(28)
The problem of the formula of van Niekerk and Dippenaar[
6] is that it does not include the effect of activity of oxygen that is well known to explain the changes in the sulfur partition ratio. A more close inspection of the model formulation and their data reveals the existence of a multicollinearity problem in the formulation, as the coefficient of determination between the predictor variables is
R2 = 0.87.[
6] A summary of the sulfide capacity models with relevant compositions in reference to blast furnace-based steelmaking has been given in Table
I.
Table I
Summary of Studies on the Modeling of the Sulfide Capacity of Slags
Sosinsky and Sommerville[ 8] | RA | CaO-Al2O3, CaO-SiO2, CaO-MgO-Al2O3, CaO-MgO-SiO2, CaO-Al2O3-SiO2, CaO-MgO-Al2O3-SiO2, CaO-SiO2-B2O3, CaO-MgO-TiO2, CaO-TiO2-SiO2, CaO-MgO-TiO2-SiO2, CaO-TiO2-Al2O3-SiO2, CaO-FeO-SiO2, CaO-FeO-Fe2O3-SiO2, CaO-FeO-TiO2, FeO-TiO2-SiO2, FeO-MgO-TiO2, CaO-FeO-MgO-TiO2, CaO-FeO-TiO2-SiO2, FeO-MgO-TiO2-SiO2, MnO-SiO2, CaO-MnO-SiO2 | 1573 to 1923 |
| RA | CaO-Al2O3, CaO-SiO2, CaO-MgO-Al2O3, CaO-MgO-SiO2, CaO-Al2O3-SiO2, CaO-MgO-Al2O3-SiO2, CaO-SiO2-B2O3, CaO-MgO-TiO2, CaO-TiO2-SiO2, CaO-MgO-TiO2-SiO2, CaO-TiO2-Al2O3-SiO2, CaO-FeO-SiO2, CaO-FeO-Fe2O3-SiO2, CaO-FeO-TiO2, FeO-TiO2-SiO2, FeO-MgO-TiO2, CaO-FeO-MgO-TiO2, CaO-FeO-TiO2-SiO2, FeO-MgO-TiO2-SiO2, MnO-SiO2, CaO-MnO-SiO2 | 1573 to 1923 |
| FM | CaO-SiO2, FeO-SiO2, MgO-SiO2 | 1773 to 1923 |
| RA | Na2O-SiO2 | 1473 to 1673 |
| FM | MnO-SiO2 | 1773 to 1923 |
| RA | Na2O-SiO2 | 1773 |
van Niekerk and Dippenaar[ 6] | | Na2O-SiO2, Na2O-SiO2-CaO, Na2O-SiO2-CaF2 | 1623 |
| RA | CaO-SiO2, MnO-SiO2, CaO-MnO-SiO2 | 1723 to 1973 |
| RA | CaO-SiO2, CaO-Al2O3, MnO-SiO2, CaO-MnO-SiO2, CaO-Al2O3-SiO2 | 1773 to 1973 |
| RA | “FeO”-SiO2, “FeO”-CaO, “FeO”-MnO, Al2O3-, Al2O3-MgO-MnO, Al2O3-CaO-MgO-MnO, Al2O3-CaO-MgO-SiO2, Al2O3-CaO-MnO-SiO2, Al2O3-CaO-MgO-MnO-SiO2 | 1623 to 1873 |
| RA | CaO-SiO2-MgO-Al2O3 CaO-SiO2-MgO-Al2O3-TiO2 | 1773 to 1873 |
| RA | CaO-Al2O3-SiO2-MgO-MnO | 1673 to 1773 |
| RA | CaO-SiO2-CrOx | 1823 to 1923 |
| IMCT | CaO-SiO2-MgO-Al2O3 | 1773 to 1873 |
| IMCT | CaO-SiO2-MgO-FeO-MnO-Al2O3 | 1802 to 1935 |
| RA | CaO-SiO2-Al2O3-MgO-CaF2-BaO | 1873 |
| RA | CaO-Al2O3-SiO2 | 1673 to 1773 |
| RA | CaO-SiO2-MnO-Al2O3-MgO | 1873 |
| RA | CaO-MgO-FeO-MnO-TiO2-Al2O3-SiO2-CaF2 | 1773 to 1923 |
| ANN | CaO-MgO-FeO-Al2O3-SiO2, CaO-MgO-TiO2-Al2O3-SiO2, CaO-MgO-MnO-SiO2, CaO-MgO-SiO2, FeO-Al2O3-SiO2, CaO-FeO-SiO2, MgO-Al2O3-SiO2, CaO-MgO-Al2O3, CaO-Al2O3-SiO2, CaO-SiO2, FeO-SiO2, FeO-CaO, FeO, CaO-CaF2-CaCl2, CaO-CaF2-SiO2, CaO-CaF2-Na2O-SiO2, CaO-CaF2-MgO-SiO2, CaO-CaF2-MnO-SiO2, CaO-CaF2-Al2O3, CaO-CaCl2 | 1273 to 1923 |
| ANN | CaO-SiO2-Al2O3-MgO | 1573 to 1973 |