Effect of Calcium Treatment on Inclusions in H08A Welding Rod Steel

Abstract

The effect of calcium treatment on inclusions in H08A welding rod steel was studied by industrial experiment and using thermodynamics theory. The effects of inclusion composition, morphology, quantity, and size in H08A welding rod steel before and after calcium treatment were studied by metallographic microscope, scanning electron microscope (SEM), and energy dispersive spectrometer (EDS). Thermodynamic studies show that the addition of calcium can form various forms of xCaO·yAl₂O₃, under the condition that the composition of molten steel remains unchanged, the control of calcium content is the key to generate low melting point calcium-aluminate complex non-metallic inclusions and improve the quality of molten steel. The production practice in steel plant shows that for welding rod steels, the calcium content in a suitable range can meet the requirements of calcium treatment. Effective calcium treatment can not only transform the high melting point Al₂O₃ inclusions into the low melting point complex non-metallic inclusions between 3CaO·Al₂O₃ and 12CaO·7Al₂O₃, but also make the original shape-diversified inclusions into the spherical calcium-aluminate complex non-metallic inclusions. Meanwhile, the total number of inclusions and large-scale inclusions in welding rod steel are reduced, and the inclusions tend to disperse in the steel, which is very conducive to the improvement of steel quality. The results show that the modification path of magnesium aluminate spinel in steel is as follows: Al₂O₃ → MgO-Al₂O₃ → MgO-CaO-Al₂O₃. In addition, calcium treatment can modify MgO-Al₂O₃ spinel in steel into liquid MgO-CaO-Al₂O₃ complex non-metallic inclusions with low melting point.

1. Introduction

With the rapid development of global infrastructure, the demand for steel in various countries is increasing; welding rod steels are the most consumed steel in the welding material industry [1]. In order to keep up with the pace of continuous updating of steel technology, welding process and welding consumables will be required to have new development. H08A welding rod steel is a kind of low-carbon and low-silicon steel. In order to ensure the weldability of welding rod steels, the requirements of chemical composition of the steel are very strict in the production of welding rod steels, which is difficult to produce. The composition requirements are shown in

Table 1. Chemical composition of welding rod steels (wt%).

Composition of Molten Steel	S	P	Mn	Si	C
National standard	≤0.030	≤0.030	0.300–0.600	≤0.030	≤0.100
Internal control standard	≤0.025	≤0.025	0.350–0.550	≤0.030	0.040–0.090

[2]. In Table 1, the national standard is the technical requirements that are uniform across the country, and internal control standard is the requirement for steel composition of the steel manufacturers participating in the experiment. In general, the internal control standard is more demanding than the national standard.

The type, quantity, size, morphology, and distribution of non-metallic inclusions in steel have great influence on the quality of metal products. The influence of inclusions on steel is mainly reflected in the corrosion resistance, toughness, plasticity, fatigue resistance, and so on [3,4,5,6,7]. For H08A welding rod steel, the type, quantity, and size of inclusions in the steel are important factors to determine whether cracks, folds, scabs, and other defects occur in the steel. Moreover, the inclusions in welding rod steels have an important influence on the microstructure and mechanical strength of the weld deposit during welding. Generally, inclusions have a negative effect on the reliability and safety of welding rod steels’ structural materials [8,9,10,11,12,13,14]. At present, the research of welding rod steels mainly focuses on crack resistance, fatigue, microstructure, and mechanical properties [7]. Hertzberg et al. [15] and Anderson et al. [16] found that the inclusion with stress concentration in welding rod steels can cause fracture at high-stress position, and the inclusion plays a key role in the crack propagation of steel.

At present, the research on inclusions in steel mainly focuses on reoxidation, mould powder, refractory, and the removal and denaturation of inclusions in the smelting process [17,18]. With the idea of oxidation metallurgy put forward, metallurgists think that instead of spending at a high cost to improve the purity of steel, it is better to modify inclusions in the steel to make them harmless, or even to achieve a benefit. Therefore, the size refinement and dispersion distribution of inclusions have become a research focus. Aluminum is often used as a deoxidizer in steel smelting because of its strong deoxidation ability and low cost. However, aluminum deoxidation will produce large size and cluster alumina inclusions, which will not only cause nozzle clogging, but also affect the steel properties during steel processing [19]. Therefore, calcium treatment can transform alumina inclusions into calcium-aluminate complex non-metallic inclusions with low melting point, which is an effective method of avoiding nozzle clogging [20,21,22,23,24,25,26,27,28,29,30,31,32]. N. verma et al. [33] concluded that the inclusion size in steel was minimal after two minutes of calcium treatment and then increased gradually. Yuan Fangming et al. [34] found that when the calcium content was less than 10 ppm, the solid fraction of inclusions in steel was more than 60%.

Therefore, this paper studies the main source, quantity, and size distribution of inclusions in H08A welding rod steel, and the evolution and deformation of inclusions in H08A welding rod steel before and after calcium treatment. The transformation of inclusions after calcium treatment was predicted by thermodynamic calculation. By deepening the understanding of inclusions in welding rod steels, the theoretical basis for the inclusion conditioning is provided, and the production quality of welding rod steels is improved.

2. Experiment

In this study, the factory experiment of H08A welding rod steel was carried out using “Hot metal and scrap → 40t electric furnace → ladle furnace refining (LF) → vacuum degassing (VD) → 150 mm × 150 mm continuous casting (CC)” production route. The production process flow chart of H08A welding rod steel is shown in Figure 1.

Two heats of experimental steel were selected as the object of study (A furnace and B furnace). Each furnace steel was sampled in LF refining furnace and VD furnace at the end of the smelting. After sampling, the samples were quickly put into water for cooling. The smelting process parameters of the two heats of experimental steel are shown in

Table 2. The operation parameters of calcium treatment in industrial production.

Furnace Times	CaO content in LF Refining Furnace/kg	LF Furnace to Add Mn Amount/kg	LF Furnace to Add Al Amount/kg	Ca addition at VD Furnace	VD Furnace Soft Blow Time/Min
A	550	20	60	100 m (Ca wire)	15
B	600	20	36	200 m (Fe-Ca wire)	8

.

The samples will be processed into a 10 mm × 10 mm × 10 mm cube, which will be coarsely ground, finely ground, and polished. The morphology and size of inclusions were observed by Zeiss–Ultra-55 (Zeiss, Oberkochen, German) field emission scanning electron microscope (SEM). The composition of the inclusion was determined by energy dispersive spectrometer (EDS) (Zeiss, Oberkochen, German). The C and S elements in steel samples were determined by carbon–sulphur detector (Yanrui Instrument Co., Ltd., Chongqing, China); N and O were determined by nitrogen–oxygen determinator (Yanrui Instrument Co., Ltd., Chongqing, China), and ICP-AES (Huapu General Technology Co., Ltd., Shenzhen, China) analysis method was used to detect the selected elements. The main components of different process stages in two furnace steels are shown in

Table 3. The chemical composition of steel samples in different working stations (wt%).

Furnace Number	Work Station	Elements
		C	Si	Mn	P	S	Als	Alt	Ca	[O]
A	LF furnace	0.0540	0.0130	0.4200	0.0050	0.0240	0.0140	0.0160	0.0002	0.0088
	VD furnace	0.0640	0.0310	0.4600	0.0060	0.0030	0.0100	0.0110	0.0004	0.0067
B	LF furnace	0.0690	0.0160	0.4100	0.0040	0.0150	0.0130	0.0170	0.0006	0.0099
	VD furnace	0.0860	0.0170	0.4300	0.0040	0.0050	0.0050	0.0050	0.0014	0.0068

. The chemical composition of LF steel sample is before calcium treatment, and the chemical composition of VD steel sample is after calcium treatment.

3. Experiment Result

3.1. Typical Inclusions in Welding Rod Steel before and after Calcium Treatment

Figure 2 shows the morphology and main composition of typical inclusions observed by scanning electron microscope in different positions of two steels. Figure 2a shows MnS inclusions in steel before calcium treatment, their shapes are mostly oval and a few are a long strip. There are two principal reasons for the introduction of MnS inclusions in H08A welding rod steel: one is that scrap steel is used as raw material in the production of H08A welding rod steel, which makes the elements in the smelting raw material become diversified—it is inevitable to introduce MnS inclusions in the steel; and the other is metal Mn added to LF refining furnace of the smelting process. Figure 2b shows the single precipitated Al₂O₃ inclusions in steel, which are mostly elliptical. Figure 2c shows clusters of MnS-Al₂O₃ complex non-metallic inclusions observed in the steel before calcium treatment.

According to Figure 2d–f, it is obvious that there are CaO-Al₂O₃ complex non-metallic inclusions, MgO-CaO-Al₂O₃ complex non-metallic inclusions, and MgO-Al₂O₃-MnS complex non-metallic inclusions in H08A welding rod steel after calcium treatment. After calcium treatment, the inclusions in the steel are transformed to compounds of calcium, and by comparing the morphology pictures of inclusions, it can be found that the shape of inclusions tends to be more spherical after calcium treatment.

In order to show more intuitively the morphology and distribution of inclusions in calcium-treated steel, the scanning pictures of inclusions are shown in Figure 3. Figure 3a shows the MgO-Al₂O₃-CaO-MnS complex non-metallic inclusions in the steel. The inclusion is centered on MgO-Al₂O₃, and CaO-MnS precipitates around it; the inclusion in Figure 3b is centered on MgO-Al₂O₃, and CaO-Al₂O₃ precipitates around it to form MgO-Al₂O₃-CaO complex non-metallic inclusion.

3.2. Particle Size Distribution and Quantity Variation of Inclusions

After coarse grinding, fine grinding, and polishing, the samples were made into metallographic samples, and the inclusions were analyzed by energy spectrum analysis under a scanning electron microscope. After having a certain understanding of the morphology of different inclusions, the morphology, size, and type of inclusions were observed under an optical microscope. The optical microscope, which has a magnification of 500 times, divides the size of inclusions into four grades, which are m ≤ 1 μm, 1 μm < m ≤ 5 μm, 5 μm < m ≤ 10 μm, and m > 10 μm (m represents the size of inclusions). The number of inclusions with different sizes in the steel at different working positions is obtained by using the method of lines, as shown in Figure 4.

It can be seen in Figure 4 that the number of inclusions of small size (m ≤ 1 μm) accounts for the majority in each process, which is consistent with Ramirez’s [35] conclusion that the average diameter of non-metallic inclusions in welding rod steels is between 0.3 μm and 0.6 μm. The small inclusions are reduced from LF to VD, which indicates that soft blowing treatment of molten steel after feeding aluminum wire has a good effect on the removal of inclusions. For the inclusions with larger size (m > 1 μm), there are more inclusions in the LF refining furnace, but the number decreases after the VD vacuum smelting furnace. One of the reasons is that most of the large inclusions in the initial liquid steel are Al₂O₃ inclusions, but after feeding calcium wire treatment, the calcium-aluminate complex non-metallic inclusions are formed and removed. Second, the soft blowing treatment of molten steel is very beneficial to the floating of large particle inclusions, so the number of inclusions has decreased; it can also be explained by Stokes’s law that large inclusions can be separated faster and easier than small inclusions.

In order to directly describe the distribution of inclusions, according to the data of the two-dimensional coordinates of inclusions on the surface of the samples and the area of each inclusion, the area percentage of inclusions in the steel matrix per unit area on the surface of the samples at different positions was calculated, as shown in Figure 5. Figure 5a,b shows the inclusion area density distribution before and after calcium treatment in A steel, respectively; and Figure 5c,d shows inclusion area densities distribution before or after calcium treatments in B steel, respectively. It can be seen in Figure 5 that the distribution of inclusions in H08A welding rod steel without calcium treatment is obviously uneven; the surface density of inclusions per unit area of steel is relatively high, and there is a segregation area of inclusions, and the maximum area density of inclusions is 0.9650%. The surface density of inclusions in the steel treated with calcium is less than 0.3550%, and the distribution of calcium-aluminate complex non-metallic inclusions is more uniform than that of alumina inclusions.

3.3. Effect of Calcium Treatment on Composition of Magnesium Aluminate Spinel in Steel

The composition of magnesium inclusions in steel samples from LF and VD furnaces (before and after calcium treatment) was analyzed by EDS. The percentages of Mg, Al, Ca, and O elements of non-metallic inclusions in steel were obtained by energy dispersive spectrometer. These percentages were attributed to the mass percentages of MgO, Al₂O_3, and CaO inclusions in the steel. Then the mass percentages of the three oxide inclusions are projected into the ternary phase diagram of the MgO-Al₂O₃-CaO system. The results are shown in Figure 6. In Figure 6, the red curve region is the liquid region of the low melting point inclusion at a temperature of 1873 K.

As can be seen in Figure 6, the MgO-Al₂O₃-CaO complex non-metallic inclusions in the steel before calcium treatment are mainly concentrated in the Al₂O₃ corner of the ternary phase diagram. After calcium treatment, more and more MgO-Al₂O₃-CaO complex non-metallic inclusions in the steel move away from the corner of Al₂O₃ and enrich to the liquid region. From the average composition of inclusions, it can be seen that the contents of MgO and Al₂O₃ in MgO-Al₂O₃-CaO inclusions begin to decrease and the content of CaO increases after calcium treatment. It is shown that the MgO-Al₂O₃ and MgO-Al₂O₃-CaO complex non-metallic inclusions can be effectively modified into liquid inclusions by calcium treatment.

4. Analysis and Discussion

4.1. Effect of Calcium Treatment on Al₂O₃ Non-Metallic Inclusions in Steel

In the calcium treatment process, its main purpose is to change the high melting point Al₂O₃ inclusion (melting point 2054 °C) into a composition close to 12CaO·7Al₂O₃ inclusion (melting point 1392 °C), so as to reduce the harmful effect of Al₂O₃ inclusion and improve the castability of molten steel. The binary system phase diagram of Al₂O₃-CaO is shown in Figure 7. In Figure 7, it can be seen that the composition of low melting point compound is between C₃A and C₁₂A₇. However, improper calcium treatment process may lead to the formation of CaO, CaS and high melting point calcium-aluminate complex non-metallic inclusions (CA, CA₆, and CA₂). These inclusions are not easy to float and remove in molten steel, which greatly increases the probability of blocking the nozzle. Some researchers have pointed out that improper calcium treatment is more likely to cause clogging than no calcium treatment [36,37].

The Wagner model [24,38] was used to calculate the activity of elements in liquid steel by Equation (1), using the mass fraction of elements in liquid steel (Table 3) and the interaction coefficient of elements in liquid steel (

Table 4. The interaction coefficients between elements.

$\mathit{i}$	$\mathit{j}$
	C	Si	Mn	S	Al	O	Ca
Al	0.091	0.057	0.0065	0.035	−0.043	−1.98	−0.047
Ca	−0.34	−0.097	−0.0156	−28	−0.072	−310	−0.002

) [32,39,40].

$$\lg f_i={\displaystyle \sum (e_i^j\cdot [j\%])}$$

(1)

$$\lg a_{[i]}=\lg f_i+\lg [\%i]$$

(2)

${\mathrm{a}}_{[i]}$—Activity of element $i$.

$f_i$—Activity coefficient of element i.

$e_i^j$—Coefficient of primary interaction of element $j$ with element $i$.

Al₂O₃ inclusions in steel may form under the action of Ca in liquid steel. There are five kinds of calcium-aluminate complex non-metallic inclusions, and the order of their growth and transformation is as follows: Al₂O₃ → CaO·6Al₂O₃(CA₆) → CaO·2Al₂O₃(CA₂) → CaO·Al₂O₃(CA) → 12CaO·7Al₂O₃(C₁₂A₇) → 3CaO·Al₂O₃(C₃A). According to the sequence of calcium-aluminate complex non-metallic isnclusions transformation, the thermodynamic calculation model of the precipitation of different composition of calcium-aluminate complex non-metallic inclusions can be obtained by thermodynamic calculation. The calculation process is shown in Equations (3)–(8) in

Table 5. The equilibrium constants of compound formation.

Reaction Equation	$\mathbf{\Delta }{\mathit{G}}^{\mathit{\theta }}$	Serial Number
${2\left[\mathrm{Al}\right]+3\left[\mathrm{O}\right]=\mathrm{Al}}_2{\mathrm{O}}_3$	$\Delta G^{\theta }=-1202000+386.3T$	(3)
$3[{\mathrm{Ca}]+19\mathrm{Al}}_2{\mathrm{O}}_3=3(\mathrm{CaO}\cdot 6{\mathrm{Al}}_2{\mathrm{O}}_3)+2[\mathrm{Al}]$	$\Delta G^{\theta }=-786553-59.9T$	(4)
$12[\mathrm{Ca}]+7(\mathrm{CaO}\cdot 6{\mathrm{Al}}_2{\mathrm{O}}_3{)}_{\left(\mathrm{s}\right)}=19(\mathrm{CaO}\cdot 2{\mathrm{Al}}_2{\mathrm{O}}_3{)}_{\left(\mathrm{s}\right)}+8[\mathrm{Al}]$	$\Delta G^{\theta }=-3134242-19.58T$	(5)
$3[\mathrm{Ca}]+4(\mathrm{CaO}\cdot 2{\mathrm{Al}}_2{\mathrm{O}}_3{)}_{\left(\mathrm{s}\right)}=7(\mathrm{CaO}\cdot A{\mathrm{l}}_2{\mathrm{O}}_3{)}_{\left(\mathrm{s}\right)}+2\left[\mathrm{Al}\right]$	$\Delta G^{\theta }=-802303+30.7T$	(6)
$15[\mathrm{Ca}]+33(\mathrm{CaO}\cdot {\mathrm{Al}}_2{\mathrm{O}}_3{)}_{\left(\mathrm{s}\right)}=4(12\mathrm{CaO}\cdot 7{\mathrm{Al}}_2{\mathrm{O}}_3{)}_{\left(\mathrm{s}\right)}+10[\mathrm{Al}]$	$\Delta G^{\theta }=-56555-1609.66T$	(7)
$9[\mathrm{Ca}]+2(12\mathrm{CaO}\cdot 7{\mathrm{Al}}_2{\mathrm{O}}_3{)}_{\left(\mathrm{s}\right)}=11(3\mathrm{CaO}\cdot {\mathrm{Al}}_2{\mathrm{O}}_3{)}_{\left(\mathrm{s}\right)}+14\left[\mathrm{Al}\right]$	$\Delta G^{\theta }=-28685511+1108.65T$	(8)

[36].

The activity coefficients and activities of calcium and aluminum in furnace A and furnace B can be calculated by using Equations (1) and (2) combined with the data in Table 4. The results are listed in

Table 6. The activity coefficient and activity of Ca and Al in calcium treated steel.

Furnace Times	${\mathit{f}}_{\mathit{A}\mathit{l}}$	${\mathit{a}}_{\mathit{A}\mathit{l}}$	${\mathit{f}}_{\mathit{C}\mathit{a}}$	${\mathit{a}}_{\mathit{C}\mathit{a}}$
A Furnace—VD	0.9883	0.0208	0.0064	2.572 × 10−6
B Furnace—VD	0.9930	0.0099	0.0052	7.2660 × 10−6

.

The relation between the equilibrium constant k of the reaction and the Gibbs free energy $\Delta G^{\theta }$ is expressed by the following formula:

$$\ln k=-\frac{\Delta G^{\theta }}{RT}$$

(9)

where T is temperature, and unit k; R = 8.314 $\mathrm{Pa}\times {\mathrm{m}}^3\times {(\mathrm{mol}\times \mathrm{K})}^{-1}$.

According to the thermodynamic data of chemical reaction Equations (3)–(9), the classical thermodynamic data calculation method is used. According to the abscissa of aluminum activity and the ordinate of calcium activity, the equilibrium relations of calcium-aluminate complex non-metallic inclusions are obtained, as shown in Figure 8.

Based on the phase diagram of CaO-Al₂O₃ system, it is shown that low melting point calcium-aluminate complex non-metallic inclusions will be formed when inclusions are formed between C₃A and C₁₂A₇. As can be seen in Figure 8, when the aluminum activity in steel is constant, the calcium activity only needs to be within an appropriate range to achieve the desired effect of calcium treatment. According to the activity values of calcium and aluminum in A and B steel VD furnaces in Table 6, two points in Figure 8 are obtained. The results of thermodynamic calculation show that the inclusion types after calcium treatment are C₁₂A₇ and C₃A. This is consistent with the experimental results, indicating that calcium treatment is effective.

4.2. Effect of Calcium Treatment on Magnesium Aluminate Spinel in Steel

In the smelting process of molten steel, because the lining is smelting at high temperature all year round, it is inevitable that magnesium aluminate spinel inclusions will be introduced because of shedding. Aluminum in molten steel can also react with magnesium oxides in slag, resulting in magnesium aluminate spinel. This is also the reason why some MgO-Al₂O₃ is observed in the steel samples collected in the LF furnace (before calcium treatment). The reaction formula can be expressed by Equations (10) and (11). In LF stage, metal aluminum was used for strong deoxidation and high basicity slag was used. The Al in molten steel could reduce MgO in slag or lining. The reduced Mg goes into the molten steel and reacts with the Al₂O₃ inclusions in the steel to form the magnesium aluminate spinel.

$$2[{\mathrm{Al}]+3(\mathrm{MgO})=3[\mathrm{Mg}]+(\mathrm{Al}}_2{\mathrm{O}}_3)$$

(10)

$$3[{\mathrm{Mg}]+4(\mathrm{Al}}_2{\mathrm{O}}_3{)=3(\mathrm{MgO}\times \mathrm{Al}}_2{\mathrm{O}}_3)+2[\mathrm{Al}]$$

(11)

In the steel samples collected in VD stage (after calcium treatment), some CaO-MgO-Al₂O₃ complex inclusions can also be observed. This is mainly the reaction between [Ca] and MgO-Al₂O₃ inclusions in molten steel after calcium treatment to form the CaO-MgO-Al₂O₃ complex non-metallic inclusions. The reaction thereof is shown in Equation (12).

$$x[\mathrm{Ca}]+(\mathrm{MgO}\cdot {\mathrm{Al}}_2{\mathrm{O}}_3)=x[\mathrm{Mg}]+[x\mathrm{CaO}\cdot (1-x)\mathrm{MgO}\cdot {\mathrm{Al}}_2{\mathrm{O}}_3]$$

(12)

After calcium treatment, most of the MgO-Al₂O₃ complex non-metallic inclusions in molten steel are transformed into CaO-MgO-Al₂O₃ complex non-metallic inclusions with a relatively low melting point. This can be confirmed by the experimental results in Figure 5. This kind of inclusion is a liquid inclusion in the smelting process, and it is easy to be removed by collision and accumulation in the process of rising. The probability of nozzle clogging in the smelting process is reduced. As can be seen in Figure 2e and Figure 3b, the core of CaO-MgO-Al₂O₃ complex non-metallic inclusions is mainly composed of MgO and Al₂O₃, and almost no CaO is found in the center. In contrast, CaO-MgO-Al₂O₃ complex non-metallic inclusions are mainly composed of CaO and Al₂O₃. It is shown that the reaction between Ca and MgO-Al₂O₃ spinel in calcium treated steel is an outward inward process. The reaction mechanism of Ca and MgO-Al₂O₃ spinel in calcium treated steel can be inferred from the experimental results, as shown in Figure 9.

In Figure 9, each type of inclusion is assumed to be spherical. Ca in the molten steel is transferred to the surface of MgO-Al₂O₃ spinel and reacts with it as shown in Process 1 in Figure 9. The reaction process is expressed by formula (12). In this process, Ca reacts with MgO-Al₂O₃ spinel surface to form a complex inclusion outer layer of CaO-MgO-Al₂O₃. Mg from the reaction is transferred to the molten steel.

Ca in the molten steel continues to react with an outer layer of CaO-MgO-Al₂O₃, until all CaO-MgO-Al₂O₃ inclusions in the outer layer are converted to CaO-Al₂O₃ inclusion, that is, process 2 in Figure 9. At this time, the inclusions in the outer layer will be transformed in the order of CA₆ → CA₂ → CA → C₁₂A₇ → C₃A. This is similar to the case of calcium treatment for Al₂O₃ inclusions described previously.

During the reaction process of CaO-MgO-Al₂O₃ outer layer, the content of Ca in the outer layer will increase continuously, which will diffuse into CaO-MgO-Al₂O₃ inner layer. Furthermore, MgO-Al₂O₃ spinel in CaO-MgO-Al₂O₃ continues to react with Ca to obtain the effect of layer-by-layer modification.

5. Conclusions

By adding metallic calcium to the H08A welding rod steel, it was found that MnS, Al₂O_3, and MnS-Al₂O₃ were the main inclusions in H08A welding rod steel before calcium treatment. After calcium treatment, the inclusions in the steel begin to transform into CaO-Al₂O₃ complex non-metallic inclusions, MgO-CaO-Al₂O₃ complex non-metallic inclusions, and MgO-Al₂O₃-MnS complex non-metallic inclusions, and the inclusions morphology presents a spherical shape.

After calcium treatment, the number of inclusions in H08A welding rod steel decreased, and large inclusions in steel also showed a decreasing trend. Through the statistics of the surface density of inclusions in H08A welding rod, it is found that the distribution of inclusions in the steel after calcium treatment is more uniform, achieving fine dispersion of inclusions in the steel.

Different forms of calcium-aluminate will be formed under different calcium treatments with different calcium contents under the condition of certain composition in molten steel. It is verified by the production practice of the steel plant that the inclusion composition of Al₂O₃ with high melting point can be changed between C₃A and C₁₂A₇ with low melting point by proper calcium content in the thermodynamics of calcium treatment. The experimental results are in agreement with the expected thermodynamic calculation results, achieving good results after calcium treatment.

Magnesium aluminate spinel in steel can be modified into liquid MgO-CaO-Al₂O₃ complex non-metallic inclusions with low melting point by calcium treatment. The reaction between Ca and MgO-Al₂O₃ spinel in molten steel is an outward–inward, layer-by-layer reaction process. The process of formation and modification of MgO-Al₂O₃ spinel in steel is as follows: Al₂O₃ → MgO-Al₂O₃ → MgO-CaO-Al₂O₃.