In the sintering of iron ores, the partial substitution of anthracite for coke breeze has been considered to be an effective way of reducing pollutant emissions and production cost. In this study, the basic characteristics of anthracite and coke breeze were compared and the sintering performance at different substitution ratios of anthracite for coke breeze was investigated. The porosity of anthracite is lower than that of coke breeze, but its density and combustion reactivity are higher. The substitution of anthracite for coke breeze has no influence on the granulation effect of the sintering blend. As the anthracite proportion increased, the sintering speed and productivity increased and the sintering yield and tumbler index decreased. As the substitution ratio increased from 0 to 60%, the melting temperature duration and the melt quantity index decreased from 2.59 to 2.03 min and from 3218.28 to 2405.75 °C·min, respectively, leading to insufficient sintering mineralization and bad sintering indexes. For an anthracite substitution ratio of 40%, the sintering speed, sintering productivity, sintering yield and tumbler index were 22.34 mm min−1, 1.49 t·(m2 h)−1, 71.65% and 63.59%, respectively, which entirely satisfies the production requirements. Furthermore, hematite (Fe2O3), calcium ferrite (CaO–Fe2O3), and compound calcium ferrite (CaO–SiO2–Fe2O3) were the major mineral phases, which were embedded with an interwoven structure.
The production of crude steel in the iron and steel industry in China has grown dramatically, which has made the country the world's largest steel producer since 19961,2,3. 40%–60% of the total iron-containing burden in the blast furnace during ironmaking is sinter4. The iron ore sintering process is one of the vital steps -in an integrated steelmaking chain, the goal of which is to agglomerate iron ore fines into porous sinters with a high mechanical strength and high thermal and reducing behaviors. This process is characterized by energy and pollution intensity, accounting for about 9–12% of the total energy used in the iron and steel industries5,6,7.
During the sintering process, sinter fuels are commonly used to provide the required energy. The coke breeze comes from coking plant (typically less than 3 mm in size) and is widely used due to its unique combustion properties, and its mechanical and structural properties. Fuel costs are high for sintering plants because of the expensive price of coke. Moreover, coke breeze causes more environment pollution because of higher NOx emission than that of anthracite. The contradiction between the coke supply and demand, and the environmental problems caused by the coke fines lead to the high price8,9.
To address this problem, researchers are beginning to search for other fuels for completely or partially substituting coke breeze. Biomass is a renewable and sustainable energy source, and it has now become an increasing important alternative energy source in the iron ore sintering process10,11. Unlike traditional fuels, biomass is an environmentally friendly resource that is carbon neutral and has lower CO2, NOX, and SO2 emissions, making it beneficial for alleviating environment-protection pressure. Biomass fuel also differs from conventional fuels with respect to its density, porosity, reactivity, and combustibility12. However, the different biomass fuels used in the sintering process cause issues such as volatile matter pyrolysis of the uncarbonized biomass. This leads to poor fuel utilization, and a higher chemical activity of the charcoal, which damages the sinter quality when a higher proportion of coke breeze is replaced with biomass. Thus, several measures were researched, for example, adding more reactive iron ores, using coarse charcoal, and adjusting the granulation methods to coat the charcoal particles and form granules10,13,14. However, these measures increase operating costs. Moreover, hydrogen-based gaseous fuel has used as another substitution fuel. It can reduce the CO2 emission and improve energy efficiency, but need extra energy efficiency, which also increases the cost in iron ore sintering15,16. Semi-coke, BF dust and sludge have also used as partial substituting fuels, however, when at a high semi-coke proportion problems like fuel combustion efficiency, an increase of SOx and zinc emission for BF dust and sludge substitution enmerges17,18.
Based on the above issues, anthracite has become the main substituting fuel for coke breeze in iron ore sintering due to its reasonable price19,20. When this substitution is made, the particle size of the anthracite needs to be controlled21. The utilization of anthracite increases the thickness of the combustion zone, which influences the quantity and quality of the finished sinter. According to a basic performance study, the reactivity of anthracite is lower than that of coke breeze, which is attributed to the differences in their true surface areas and intrinsic surface reactivities. Through mathematical modeling simulations, the effect of anthracite on iron ore sintering was evaluated, and it was determined that its combustion characteristics are not as good as those of coke breeze19,22. However, the combustion performances of various anthracite differ.
This study focused on determining the basic physical and combustion characteristics of anthracite and the differences between the characteristics of anthracite and those of coke breeze. The combustion characteristics of both were researched by through thermogravimetric analysis (TGA), which covered a wide range of applications in the research, development, and economic assessment of coal and other fuels23,24,25. Experiments involving the substitution of anthracite for coke breeze were conducted to assess the effects on the sintering process, including the granule size distribution, sintering indexes, and thermal bed characteristics, and to study the influences on the mineral composition and microstructure of the sinter.
Experimental materials and methods
In this study, the raw materials consisted of iron-bearing materials (iron concentrates, iron ore fines, and miscellaneous materials), fluxes (limestone, dolomite, quicklime, and serpentine), solid fuels (coke breeze and anthracite), and return fines. The chemical compositions and size distributions of all of the raw materials are presented in Tables 1 and 2. The iron-bearing materials regulated the Fe and SiO2 contents, and the fluxes adjusted the sinter basicity (CaO/SiO2, mass ratio) and MgO content. The basicity of the finished sinter was maintained at 1.70. As can be seen from Table 2, the average particle size of the anthracite was 1.97 mm, which is a little larger than that of the coke breeze. Table 3 shows the results of the proximate analysis of the coke breeze and anthracite. The anthracite contained 7.73% volatiles, and it contained more fixed carbon and had a lower ash content than the coke breeze. It can be seen that the contents of N and S in anthracite are obviously lower than that of coke breeze, indicating that anthracite is more environmentally friendly in sintering process. Moreover, the heating value of the anthracite was higher than that of the coke breeze.
A NETZSCH STA-449C differential thermogravimetric analyzer (precision of temperature measurement ± 1 °C, microbalance sensitivity of 0.1 μg) was used for combustion tests of the coke breeze and anthracite. The weight-loss values and the rates of the fuels as functions of temperature or time were recorded continuously under dynamic conditions. Precisely Weighed 10 ± 0.1 mg samples (particle size of 0.125–0.25 mm) were thinly distributed in an Al2O3 ceramic crucible, which eliminated the effects of the inevitable side reactions and the mass and heat transfer limitations. In the combustion tests on coke breeze and anthracite, the heating temperature ranges from 20 to 1000 °C and the heating rate and flow rate of the artificial air were fixed at 10 °C min−1 and 100 ml min−1, respectively.
The typical parameters generally include the ignition temperature (Ti), the peak temperature of the maximum weight loss rate (Tm), the burnout temperature (Th), the maximum combustion rate (DTGmax), the mean combustion rate (DTGmean) and the burnout time (τ). On the combustion profile, the ignition temperature refers to the start of a sudden decrease in fuel weight; the burnout temperature represents the point at which combustion is complete; and the τ is the time needed for the coke breeze and anthracite combustion to progress from ignition to burnout. The DTGmax is when the weight loss rate reaches the maximum; and the DTGmean is the mean rate of weight loss. In addition, the overlapping combustion interval of the fuel is the weight loss of the anthracite divided by the total weight loss of the coke breeze in the combustion interval23,24,25.
Sintering pot trials
The sintering experiments were conducted in a laboratory-scale sinter pot with a depth of 700 mm and a diameter of 180 mm. A schematic of the experiment is shown in Fig. 16,26,27. The raw materials were blended manually according to the proportions presented in Table 1. During this stage, the sinter mixture’s moisture was controlled at 7.1 ± 0.1% to meet the prescribed level. Then, the sinter mixture was granulated into sinter feed in an electric drum granulator with length a of 1400 mm and a diameter of 600 mm. The revolving speed and duration were 15 rpm and 5 min, respectively. A hearth layer was prepared at the bottom of the sinter pot to protect the grate from high-temperature erosion (1 kg sintering production, size of 10–15 mm). After the sinter feed was placed in the pot, an ignition hood fueled by natural gas was used to ignite the fuels and to supply enough heat. The ignition temperature, time, and negative pressure were the conventional values of 1050 ± 50 °C, 1 min, and 6 kPa, respectively. The pressure drop was immediately adjusted to 12 kPa after ignition and then to 6 kPa for cooling when the flue gas temperature reached the maximum value. Then, the combustion front could move downward, and it was sustained by an induced draft fan. A thermal couple (K-type) was installed 200 mm from the sinter bed’s surface to measure the temperature profile.
The proportions of anthracite substituted for coke breeze in the sinter pot experiments were 0%, 20%, 40%, and 60%, and the effects on the granule size distribution, the sintering indexes, and the thermal characteristics were investigated. The proportion of the sintering blending was set according to the basic values shown in Table 1, including the total solid fuel ratio of 4.5%. The sintering basicity and sinter mixture moisture were 1.7 and 7.1%, respectively.
Evaluation of the sintering performance
The sintering speed, yield, tumbler index, and productivity are four vital indexes used to evaluate the sinter quality28. Sintering speed is the height of the sinter bed divided by the sintering time (mm min−1).The yield is the mass of the > 5 mm sinter divided by the total sinter mass minus the hearth layer mass of 1 kg (%). The productivity is the production capacity that the sintering machines can reach for a specific area and time (t m−2 h−1). The sintering speed, yield and productivity are calculated according to Eqs. (1)–(3):
where H is the height of sintering bed (mm); t is the sintering time (min); M is the mass of sinter cake (kg); M0 is the mass of return fines (kg); S is the cross-sectional area of sinter bed (m2).
The tumbler index is the mass proportion of the > 6.3 mm sinter after 8 min tumbling, which is determined by ISO tumble standard. In addition, the return fines balance is the mass ratio of the produced return fines to the provided return fines; its reference value was within 1 ± 0.05. It was important that each sinter experiment reached the return fines balance, which guaranteed the validity of the four indexes.
It is known that the quality of sinter is highly related to the thermal status of the sintering bed. To quantitatively evaluate the thermal characteristics, the duration time of the melting temperature (DTMT) and the melt quantity index (MQI) were obtained from the temperature–time profile (Fig. 2).
The DTMT was defined as the time interval between the time at which the bed temperature reaches 1200 °C and the time at which the bed temperature decreases to below 1200 °C. The temperature of 1200 °C was selected as the base temperature of the melting zone, because calcium ferrite and compound calcium ferrite (SFCA) were the major bonding phases used to bond separate particles together, during the sintering process, so the melting point was slightly above 1200 °C. Therefore, a sufficient DTMT was a precondition to generate enough of the melting phase.
The MQI is defined as the area above 1200 °C on the sintering bed temperature–time profile. It is a comprehensive parameter reflects the melting zone information. A larger MQI value indicates that more melting phase is formed, thus contributing to sufficiently filling the voids between the separate particles and combining them together after cooling. It is expressed by Eq. (4):
where T0 is the initiating temperature of 1200 °C; T is the bed temperature at time t (°C); t1 and t2 are the starting time and ending time of the 1200 °C (min) phase, respectively.
Characteristics of anthracite and coke breeze
Density and porosity
Figure 3 shows the differences in the densities (bulk density, true density) and porosity of the coke breeze and anthracite used in the experiments. As is shown in the Fig. 3, the bulk density and true density of the anthracite were slightly higher than those of the coke breeze, that is, the volume of the anthracite added to sinter mixture was less than that of the coke breeze for the same mass. The porosity of the anthracite was 37.9%, which was lower than that of the coke breeze (41.4%). In general, the bulk densities, true densities and porosity of coke breeze and anthracitewere similar. These properties have no effect on the substitution anthracite for coke breeze in iron ore sintering.
The TGA experimental conditions, the temperature, and the duration of the high temperature were far different from those of real sintering processes; however, these experiments are a simple but quite effective technique for observing the burning profile of fuels29,30,31. Therefore, the different combustion behaviors of coke breeze and anthracite during the sintering process can be estimated from the combustion characteristics determined from the TGA. Figure 4 shows the results of the combustion behaviors of the coke breeze and anthracite. As is shown in Fig. 4, b, both the anthracite and coke fines exhibit only one combustion peak since the combustion of the fixed carbon contributes greatly to their weight loss. Their basic variation trends during the temperature increase process are similar. As can be seen from Fig. 4c, d , the coke breeze had an ignition temperature of 558 °C and a burnout temperature of 850 °C, while those of anthracite were 566 °C and 842 °C, respectively. Both ignited at a similar temperature. The overlapping combustion interval between the coke breeze and anthracite was 94.52%, indicating that they have similar combustion behaviors. In addition, a meaningful difference in the details. First, anthracite burns completely, leading to a shorter combustion time of 13.8 min; while coke breeze burns out at a longer combustion time of 14.6 min. The DTGmax of anthracite is higher (0.80%/min) than that of coke breeze, indicating that it has a fiercer combustion, but its DTGmean is slightly lower (0.15%/min). The combustion characteristics of these two fossil fuels make it clear that the combustion reactivity of anthracite is greater than that of coke breeze, which can affect the combustion conditions in the sintering bed.
Assessment on the substitution of anthracite for coke breeze
Effect on granule size distribution
The effect of substituting anthracite for coke breeze on the granule size distribution is shown in Fig. 5. As can be seen, the granulating effect was good in all of the experiments32. The ratio of the + 3 mm sintering granules of was much greater than that of the − 3 mm sintering granules, and the 5–8 mm particles accounted for the largest percentage. In particular, the granule distribution proportions of + 8 mm, 5–8 mm and 3–5 mm particles were very similar in the coke breeze experiments and of the experiments in which anthracite was substituted for coke breeze. The mean size of the sinter mixture in each sintering experiment ranged from 5 to 5.5 mm, resulting in a similar granulating effect. In short, the results of the granulating analysis suggest that substituting different amounts of anthracite for coke breeze does not have a negative influence, when the initial sinter bed permeability is the same.
Effect on sintering quality
The influence of substituting anthracite for coke breeze on sintering index is shown in Fig. 6. Compared with the base trial where only coke breeze was used, the sintering speed increased from 19.84 to 24.52 mm min−1 as the proportion of anthracite substitution increased. The improvement of the sintering speed was positively correlated with the shorter combustion time of the anthracite. The sinter yield worsened to a small extent, decreasing from 72.61 to 70.26%, which still meets the production requirement for the laboratory sintering experiment. Taking the sintering speed increase and the yield decrease into consideration, based on our calculations, substituting anthracite for coke breeze improves the productivity by 18.18%. However, the last important indicator, that is, the tumbler index, deteriorated significantly when the replacement percentage reached 60%. For a substitution proportion of 40%, the sinter tumbler index retained at 63.59%, which satisfies the quality requirements. To achieve ideal sintering indexes, the proportion of anthracite substituted for coke breeze should not exceed 40%.
Effect on the thermal characteristic of the sintering bed
The effect of substituting anthracite for coke breeze on the thermal characteristic of the sintering bed was investigated at a position of 200 mm from the top of the sinter pot. The results are shown in Fig. 7. As can be seen from the temperature curves, the sinter bed temperature increased rapidly to the maximum value in about3 min, and then, it decreased relatively slowly because of the heat exchange with the suction air. Due to the different combustion characteristics of anthracite and coke breeze, the maximum temperature was reached in advance because the flame front speed increased with increasing anthracite dosage, which expedited the sintering speed. The faster combustion reactivity of anthracite resulted in a higher maximum temperature and a shorter sintering duration time, which decreases the sinter quality. As the anthracite substitution ratio increased from 0 to 60%, the melting temperature duration time decreased from 2.59 to 2.03 min, and the melt quantity index decreased from 3218.28 to 2405.75 °C·min.
The main reactions involve the sintering process, are listed in Eqs. (5)–(10), and the characteristics and melting temperatures of the fusible compounds and the eutectic mixtures are presented in Table 433. Hematite (Fe2O3), fayalite (2FeO·SiO2), dicalcium silicate (2CaO·SiO2), calcium ferrite (CaO–Fe2O3) and compound calcium ferrite (CaO–SiO2–Fe2O3) are the main mineral phases formed in the sintering process. The fayalite, dicalcium silicate, calcium ferrite, and compound calcium ferrite are in the liquid phase, allowing them to fill in the spaces around the hematite particles and other particles as the sintering temperature increased to about 1200 °C. This binds the particles into a firm amalgamation, especially calcium ferrite and compound calcium ferrite. The Fe2O3–CaO–SiO2 phase diagram was analyzed using the FactSage 7.2 software (Fig. 8). As can be seen from Fig. 8, the lowest melting point of the ternary phase is 1193 °C (point 10). The formation of compound calcium ferrite (Ca3Fe2Si3O12) induced the low melting point. The melting temperatures at points 7 and 8 are 1209 °C and 1205 °C, respectively, which is where calcium ferrites (CaFe4O7 and CaFe2O4) form. It is further demonstrated that the formation of compound calcium ferrite and calcium ferrite are quite important to the sinter quality.
Hence, the temperatures should be maintained at greater than 1200 °C, so that these reactions and the bonding process can be completed, that is, sintering mineralization can occur. When anthracite was substituted for coke breeze, the melting temperature duration time was shorter and the melt quantity index was lower, especially for an anthracite substitution ratio of 60%. Thus, the amount of sintering mineralization insufficient, leading to bad sintering indexes. Appropriate anthracite substitution ratios still meet the demand for obtaining acceptable laboratory indexes. When the anthracite substitution ratio is too high, it has a significant influence on the sintering process and results in a poor sinter quality.
Mineral composition and microstructure
To verify the above analysis, the mineral composition of the sintered sample obtained from the 40% anthracite substitution experiment was analyzed using scanning electron microscopy (SEM) and energy dispersive X-ray spectroscopy (EDS) (Fig. 9). The three primary minerals present were hematite, calcium ferrite, and complex silicate, corresponding to points A, B, and C, respectively. The bonding phases mainly included calcium ferrite, especially SFCA, with lesser amounts of complex silicate, which contains Si, Ca, Fe, and Al.
The microstructure was also a critical factor determining the properties of the sinter, which is shown in Fig. 10. The main bonding phase was acicular and stripped SFCA (Fig. 10a, b), and the granular shape is shown in Fig. 10c, d. SFCA is considered beneficial for the sinter structure (good reducibility, improves shatter index (SI) and Tumbler index (TI))34,35. It is closely linked to the solid particles to form an interwoven structure, which is the principal structure and has a good strength. The silicate liquid phase of the perfect crystallization closely secures the calcium ferrite to the embedded cloth shape, which is another structure with a good strength. Additionally, only a few small holes exist in the sinter. In conclusion, the fine microstructure of the sinter demonstrates that 40% anthracite substitution for coke breeze in the sintering process is feasible.
The basic characteristics of anthracite and coke breeze were compared and the effects of substituting anthracite for coke breeze on the different parameters were determined through sinter pot experiments. The results indicate that anthracite can be used to partially replace coke breeze. The following is a summary of the results obtained in this study.
The density and porosity of anthracite are higher and lower than those of coke breeze, respectively, but they have a similar granulating performance. Both anthracite and coke breeze have similar combustion behaviors, but the combustion reactivity of anthracite is higher; hence, it requires a shorter combustion time.
As the anthracite proportion increases, the sintering speed and the sintering productivity increased and the tumbler index and yield decrease. The melting temperature duration time decreased from 2.59 to 2.03 min and the melt quantity index decreased from 3218.28 to 2405.75 °C·min as the anthracite ratio increased, which is disadvantageous to sintering mineralization and results in bad sintering indexes, especially for a anthracite substitution ratio of 60%.
The finished sinter produced by the 40% anthracite substitution experiment had a good microstructure. Calcium ferrite, Hematite, and complex silicate phase were the major mineral phases. They linked together closely and formed an interwoven structure that ensured the sintering performance.
Hasanbeigi, A., Arens, M., Cardenas, J. C. R., Price, L. & Triolo, R. Comparison of carbon dioxide emissions intensity of steel production in China, Germany, Mexico, and the United States. Resour. Conserv. Recycl. 113, 127–139. https://doi.org/10.1016/j.resconrec.2016.06.008 (2016).
Zhang, F. & Huang, K. The role of government in industrial energy conservation in China: lessons from the iron and steel industry. Energy Sustain. Dev. 39, 101–114. https://doi.org/10.1016/j.esd.2017.05.003 (2017).
Feng, C., Huang, J.-B., Wang, M. & Song, Y. Energy efficiency in China’s iron and steel industry: evidence and policy implications. J. Clean. Prod. 177, 837–845. https://doi.org/10.1016/j.jclepro.2017.12.231 (2018).
Jha, G., Soren, S. & Mehta, K. D. Partial substitution of coke breeze with biomass and charcoal in metallurgical sintering. Fuel https://doi.org/10.1016/j.fuel.2020.118350 (2020).
Tsioutsios, N., Weiß, C., Rieger, J., Schuster, E. & Geier, B. Flame front progress in gas assisted iron ore sintering. Appl. Therm. Eng. 165, 114554. https://doi.org/10.1016/j.applthermaleng.2019.114554 (2020).
Wang, Z.-C., Zhou, Z.-A., Gan, M., Fan, X.-H. & He, G.-Q. Process control technology of low NOx sintering based on coke pretreatment. J. Cent. South Univ. 27, 469–477. https://doi.org/10.1007/s11771-020-4309-y (2020).
Li, G. et al. Energy saving of composite agglomeration process (CAP) by optimized distribution of pelletized feed. Energies 11, 2382 (2018).
Liu, C., Zhang, Y.-Z., Zhao, K., Xing, H.-W. & Kang, Y. Modified biomass fuel instead of coke for iron ore sintering. Ironmak. Steelmak. 47, 188–194. https://doi.org/10.1080/03019233.2018.1507070 (2020).
Taira, K. Two-dimensional temperature distribution in a fixed bed at high spatial resolution visualized by in-situ measurement of iron-ore sintering during combustion. Fuel 272, 117735. https://doi.org/10.1016/j.fuel.2020.117735 (2020).
Cheng, Z., Yang, J., Zhou, L., Liu, Y. & Wang, Q. Characteristics of charcoal combustion and its effects on iron-ore sintering performance. Appl. Energy 161, 364–374. https://doi.org/10.1016/j.apenergy.2015.09.095 (2016).
Cheng, Z. et al. Experimental study of commercial charcoal as alternative fuel for coke breeze in iron ore sintering process. Energy Convers. Manag. 125, 254–263. https://doi.org/10.1016/j.enconman.2016.06.074 (2016).
Lovel, R. R., Vining, K. R. & Dell’amico, M. The influence of fuel reactivity on iron ore sintering. ISIJ Int. 49, 195–202. https://doi.org/10.2355/isijinternational.49.195 (2009).
Hosokai, S. et al. Kinetic study on the reduction reaction of biomass-tar-infiltrated iron ore. Energy Fuels 26, 7274–7279. https://doi.org/10.1021/ef3013272 (2012).
Zhao, J. et al. A fundamental study of the cocombustion of coke and charcoal during iron ore sintering. Energy Fuels 32, 8743–8759. https://doi.org/10.1021/acs.energyfuels.8b00939 (2018).
De Castro, J. A., De Oliveira, E. M., De Campos, M. F., Takano, C. & Yagi, J.-I. Analyzing cleaner alternatives of solid and gaseous fuels for iron ore sintering in compacts machines. J. Clean. Prod. 198, 654–661. https://doi.org/10.1016/j.jclepro.2018.07.082 (2018).
Cheng, Z., Yang, J., Wei, S., Guo, Z. & Wang, Q. In 11th Conference on Sustainable Development of Energy, Water and Environment Systems (SDEWES2016).
Luo, Y. H., Zhu, D. Q., Pan, J. & Zhou, X. L. Utilisation of semi-coke as by-product derived from coal-based direct reduction process in iron ore sintering. Ironmak. Steelmak. 43, 628–634. https://doi.org/10.1080/03019233.2016.1152001 (2016).
Lanzerstorfer, C., Bamberger-Strassmayr, B. & Pilz, K. Recycling of blast furnace dust in the iron ore sintering process: investigation of coke breeze substitution and the influence on off-gas emissions. ISIJ Int. 55, 758–764. https://doi.org/10.2355/isijinternational.55.758 (2015).
Gu, H. et al. Iron ore as oxygen carrier improved with potassium for chemical looping combustion of anthracite coal. Combust. Flame 159, 2480–2490. https://doi.org/10.1016/j.combustflame.2012.03.013 (2012).
Ri, D.-W., Chung, B.-J. & Choi, E.-S. Effects of anthracite replacing coke breeze on iron ore sintering. Revue Métall. 105, 248–254. https://doi.org/10.1051/metal:2008038 (2008).
Cheng, Z., Tan, Z., Guo, Z., Yang, J. & Wang, Q. Recent progress in sustainable and energy-efficient technologies for sinter production in the iron and steel industry. Renew. Sustain. Energy Rev. 131, 110034 (2020).
Yang, W., Choi, S., Choi, E. S., Ri, D. W. & Kim, S. Combustion characteristics in an iron ore sintering bed—evaluation of fuel substitution. Combust. Flame 145, 447–463. https://doi.org/10.1016/j.combustflame.2006.01.005 (2006).
Zhong, Q. et al. Combustion behavior of coals in rotary Kiln and their interaction on co-combustion. Energy Fuels 32, 3833–3841. https://doi.org/10.1021/acs.energyfuels.7b02761 (2018).
Zhong, Q., Yang, Y., Jiang, T., Li, Q. & Xu, B. Xylene activation of coal tar pitch binding characteristics for production of metallurgical quality briquettes from coke breeze. Fuel Process. Technol. 148, 12–18. https://doi.org/10.1016/j.fuproc.2016.02.026 (2016).
Suopajärvi, H., Kemppainen, A., Haapakangas, J. & Fabritius, T. Extensive review of the opportunities to use biomass-based fuels in iron and steelmaking processes. J. Clean. Prod. 148, 709–734. https://doi.org/10.1016/j.jclepro.2017.02.029 (2017).
Li, G. et al. Behavior of SO2 in the process of flue gas circulation sintering (FGCS) for iron ores. ISIJ Int. 54, 37–42. https://doi.org/10.2355/isijinternational.54.37 (2014).
Jiang, T. et al. Preparation of BF burden from titanomagnetite concentrate by composite agglomeration process (CAP). ISIJ Int. 55, 1599–1607. https://doi.org/10.2355/isijinternational.ISIJINT-2015-094 (2015).
Gan, M., Fan, X. & Chen, X. Calcium Ferrit Generation During Iron Ore Sintering—Crystallization Behavior and Influencing Factors (IntechOpen Press, London, 2015). https://doi.org/10.5772/59659.
Nie, Q. H., Sun, S. Z. & Li, Z. Q. Thermogravimetric analysis on the combustion characteristics of brown coal blends. J. Combust. Technol. 316–317, 23–27 (2001).
Wang, C. A., Zhang, X. M., Liu, Y. H. & Che, D. F. Pyrolysis and combustion characteristics of coals in oxyfuel combustion. Appl. Energy 97, 264–273. https://doi.org/10.1016/j.apenergy.2012.02.011 (2012).
Gani, A. & Naruse, I. Effect of cellulose and lignin content on pyrolysis and combustion characteristics for several types of biomass. Renew. Energy 32, 649–661. https://doi.org/10.1016/j.renene.2006.02.017 (2007).
Fernández-González, D., Ruiz-Bustinza, I., Mochón, J., González-Gasca, C. & Verdeja, L. F. Iron ore sintering: raw materials and granulation. Miner. Process. Extr. Metall. Rev. 38, 36–46. https://doi.org/10.1080/08827508.2016.1244059 (2017).
Jiang, T. Agglomeration of Iron Ore (Central South University Press, Changsha, 2016).
Chen, C. L., Lu, L. M. & Jiao, K. X. Thermodynamic modelling of iron ore sintering reactions. Minerals 9, 13. https://doi.org/10.3390/min9060361 (2019).
Fernández-González, D., Ruiz-Bustinza, I., Mochón, J., González-Gasca, C. & Verdeja, L. F. Iron ore sintering: process. Miner. Process. Extr. Metall. Rev. 38, 215–227. https://doi.org/10.1080/08827508.2017.1288115 (2017).
This work is supported by the National Key R&D Program of China (2017YFB0304301), the Fundamental Research Funds for the Central Universities of Central South University (No. 202044016), and the Co-Innovation Center for Clean and Efficient Utilization of Strategic Metal Mineral Resources.
The authors declare no competing interests.
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Zhang, X., Zhong, Q., Liu, C. et al. Partial substitution of anthracite for coke breeze in iron ore sintering. Sci Rep 11, 1540 (2021). https://doi.org/10.1038/s41598-021-80992-4
Transactions of the Indian Institute of Metals (2021)