Counteracting ring formation in rotary kilns
 M Pisaroni^{1},
 R Sadi^{2} and
 D Lahaye^{1}Email author
https://doi.org/10.1186/2190598323
© Pisaroni et al.; licensee Springer 2012
Received: 27 April 2012
Accepted: 9 October 2012
Published: 24 October 2012
Abstract
Avoiding the formation of rings in rotary kilns is an issue of primary concern to the cement production industry. We developed a numerical combustion model that revealed that in our case study rings are typically formed in zones of maximal radiative heat transfer. This local overheating causes an overproduction of the liquid phase of the granular material, which tends to stick to the oven’s wall and to form rings. To counteract for this phenomenon, we propose to increase the amount of secondary air injected to cool the oven. Experimental validation at the plant has confirmed that our solution is indeed effective. For the first time in years, the kiln has been operating without unscheduled shutdowns, resulting in hugely important cost savings.
Keywords
1 Introduction
1.1 Rotary kilns
We will look into direct fired kilns in which the energy necessary to heat the material to the level required for the intended reactions is generated by the combustion of hydrocarbon fuels continuously fed to a burner placed in the freeboard. This energy is subsequently transferred by heat exchange between the gas phase and the material bed. The lateral surface of the kiln is covered by an isolating lining of refractory material. Hot gases flow in a direction opposite to that of the material bed through the kiln. The heat transfer between the freeboard and the bed is a rather complex phenomenon as it occurs along various paths determined by the physics of radiation. Various transport processes therefore constitute the working principle of the ovens considered.
We study a rotary kiln used by Almatis B.V. in Rotterdam for a production of calciumaluminate cement, a white, high purity hydraulic bonding agent providing controlled setting times and strength required in today’s high performance refractories operating at temperatures up to $1\text{,}800$ degrees Celsius. This cement is made by fusing a mixture of a calciumbearing limestone and an aluminumbearing material. The following two considerations will be important in our approach to the modeling of the kiln. The first is that the material bed occupies no more than five percent of the total volume of the kiln. The second is that the combustion of fuel by the burner is aided by inflow of preheated air through a secondary air inlet.
1.2 Ring formation
As material slides and tumbles slowly through a heated rotary kiln, a thin layer of dust invariably forms on its inner lateral surface. Some zones of the kiln may be particularly prone to particle accumulation in such a way that the combination of particular thermal and flow conditions results in the formation of cylindrical deposits of solid crystalline structures referred to as rings. As such rings grow thicker, they form a dam in the freeboard, hindering the flow of material and flue gasses through the kiln.
In the kiln we consider, we observed in particular socalled frontend/midkiln rings [5]. They are formed close to the burner and are presumably caused by the direct impingement of the burner flame on the lateral surface causing local overheating. These are the most common and most troublesome type of rings as they cannot be reached from the kiln’s exterior and are therefore impossible to remove while the kiln is in operation. In severe cases, ring dams grow rapidly and cause the unscheduled shutdown of the kiln. In the last three years we registered on average at least one ring formation per month, of which seventy percent caused the unforeseen shutdown of the kiln for on average three days. Each of these kiln outages causes very important production and turnover losses.
This paper is structured as follows. In Section 2 we motivate the development of a computational fluid dynamics model for the kiln. In Section 3 we give details of this model’s operational setup and geometry, the polyhedral mesh discretizing the spatial coordinates and the partial differential equations governing the gas flow in the oven, the combustion of hydrocarbon fuel in the burner, the reactions of the chemical species and the radiative heat transfer in the freeboard. In Section 4 we present numerical results that convincingly show that our model allows to localize and counteract the ring formation by increasing the amount of air through the secondary air inlet. In Section 5 finally we report on an experimental validation at the plant that confirms the effectiveness of the change in operating conditions that we propose.
2 Localizing and counteracting ring formation
3 Computational fluid dynamics model
The detailed mathematical model we developed is a multiphysics model that takes the following phenomena into account: the reactive gas flow and temperature, chemical species and radiative heat transfer distribution in the kiln, the turbulent nonpremixed combustion of hydrocarbon gasses in the burner, the insulating properties of the lining, the rotary motion of the kiln and the forced convection on the outside surface.
The material bed only occupies a small fraction of the volume of the kiln and has a negligible limited impact of temperature distribution. We therefore do not take the material bed into account in our model and simulate an empty kiln.
The most important physical phenomenon that takes place in this burner region is the turbulent nonpremixed combustion of the fuel injected from the burner with the secondary air. Combustion, even without turbulence, is an intrinsically complex process involving a large range of chemical time and length scales. Some of the chemical phenomena controlling flames take place in short times over thin layers and are associated with very large mass fractions, temperature and density gradients. The full description of chemical mechanisms in laminar flames may require hundreds of species and thousands of reactions leading to considerable numerical difficulties. Turbulence itself is probably the most complex phenomenon in nonreacting fluid mechanics. Various time and length scales are involved and the description of turbulence remains to date an open questions. The modeling of the kiln therefore requires resorting to a set of assumptions that are described in the remainder of this section.
3.1 The geometry
The geometry model of the kiln is shown in Figure 3. Figure 3(a) and Figure 3(b) give an exterior view on the complete kiln and a more detailed interior view of the burner region, respectively. The challenging aspect of this geometry is that the inlets of the burner are a factor thousand times smaller than the axial length of the kiln, imposing challenges in the mesh generation process.
3.2 Grid generation
The mesh model is shown in Figure 4. Figure 4(a), Figure 4(b) and Figure 4(c) give an exterior view of the mesh in the air inlet region, an interior view of the mesh and a detailed view of the mesh on the burner, respectively. We employed a polyhedral mesh of 2.8 million cells with local refinement in the critical inlets and burner regions. The main difficulties in meshing this geometry were found in balancing the accuracy required capture the flow around small features in the burner with the overall computational cost. Polyhedral meshes provide a balanced solution in complex mesh generation problems of this kind.
Tetrahedra are the simplest type of volume elements. As their faces are plane segments, both face and volume centroid locations are well defined. A disadvantage is that tetrahedra cannot be stretched too much. To achieve a reasonable accuracy a much larger number of control volumes is needed than if structured meshes are used. Furthermore, as tetrahedral control volumes have only four neighbors, and computing gradients at cell centers using standard approximations can be problematic.
Polyhedra offer the same automatic meshing benefits as tetrahedra while overcoming their disadvantages. A major advantage of polyhedral cells is that they have many neighbors (typically of order 10) allowing gradients to be much better approximated. Obviously more neighbors implies more storage and computational operations per cell, but this is more than compensated by a higher accuracy. Polyhedral cells are also less sensitive to stretching than tetrahedra. A polyhedron with 12 faces for instance has six optimal directions which, together with the larger number of neighbors, leads to a more accurate solution with a lower cell count. Comparisons in many practical tests have verified that with polyhedral meshes, one needs about four times fewer cells, half the amount of memory and a tenth to a fifth of computing time compared to tetrahedral meshes to reach solutions of the same accuracy. In addition, solvers on polyhedral meshes were found to converge more robustly with respect to change in their parameters. A more detailed analysis of polyhedral meshes can be found in [6].
3.3 Governing reacting flow equations
In this section we present the conservation equations for reacting flows we used. The equations are derived from the NavierStokes (NS) equations by adding terms that account for reacting flows. The reacting gas is a nonisothermal mixture of multiple species which must be tracked individually. As heat capacities change significantly with temperature and composition, the transport coefficients require specific attention. In this subsection we will describe the NavierStokes and ReynoldsAveraged NavierStokes flow model, the nonrealizable KEpsilon turbulence model and the Standard Eddy Break Up combustion model. A more detailed derivation of these equations can be found in e.g. [7, 8].
where N is the number of species in the reacting mixture, ${m}_{\ell}$ the mass of species ℓ in a volume V and m the mass of gas in the volume, respectively. The conservation of mass can then be written as
where $\rho =m/V$ is the density of the gas and ${u}_{i}$ its three dimensional velocity field, respectively. The conservation of species ℓ for $\ell =1:N$ can then be written as
where ${V}_{\ell ,i}$ the i th component of the diffusion velocity ${V}_{\ell}$ of species ℓ and ${\dot{\omega}}_{\ell}$ the chemical reaction rate of species ℓ. The conservation of momentum for the gas can for $j=1:3$ be expressed as:
The work done by the gas on the species can be expressed as $\rho {\sum}_{\ell =1}^{N}{Y}_{\ell}{f}_{\ell ,i}{V}_{\ell ,i}$. With all these quantities introduced, the conservation of energy in terms of ${h}_{s}$ can be expressed as:
Turbulent combustion results from the twoway interaction between chemistry and turbulence. When a flame interacts with a turbulent flow, the combustion modifies the turbulence in two ways. The heat released induces high flow accelerations through the flame front and the temperature changes generate large changes in kinematic viscosity. These phenomena may either generate or damp turbulence and are referred to as flamegenerated turbulence and relaminarization due to combustion, respectively. The turbulence conversely modifies the flame structure. This may either enhance the chemical reactions or completely inhibit it, leading to flame quenching. Compared to premixed flames, turbulent nonpremixed flames exhibit some specific features that have to be taken into account. Nonpremixed flames do not propagate as they localized on the fueloxidizer interface. This property is useful for safety purposes but it also has consequences on the chemistryturbulence interaction. Without propagation speed, a nonpremixed flame is unable to impose its own dynamics on the flow field and is therefore more sensitive to turbulence.
The description of the turbulent nonpremixed combustion processes in a computational fluid dynamics model may be achieved using three levels of accuracy in the computations. Either a Reynolds Averaged Navier Stokes (RANS), a Large Eddy Simulations (LES) or a Direct Numerical Simulations (DNS) model can be adopted. In current engineering practice, the RANS model is extensively used because it is less demanding in terms of resources. Its validity however is limited by the closure models describing turbulence and combustion and the need for some form of callibration. Considering the complexities and the dimensions of our kiln, using the RANS model is the only feasible choice.
3.3.1 RANS model
The RANS equations derived from the reacting NavierStokes equation given above are then given by the equation for conservation of mass
the equation for conservation of species ℓ for $\ell =1:N$
the equation for conservation of momentum for $j=1:3$
and finally the equation for conservation of momentum
The averaging procedure introduces unclosed quantities that have to be modeled. Without entering in the details we list here the two main unclosed terms that will be described in the next sections:

Reynolds stresses: $\overline{\rho}\tilde{{u}_{i}^{\u2033}{u}_{j}^{\u2033}}$.

Species chemical reaction rates: ${\overline{\dot{\omega}}}_{\ell}$.
3.3.2 Turbulence model
where ε is the rate of energy dissipation. In this model the critical coefficient ${C}_{\mu}$ is a function of mean flow and turbulence properties, rather than assumed to be constant as in the standard model. This allows to satisfy certain mathematical constraints on the normal stresses consistent with the physics of turbulence and is referred to as realizability.
The easiest way to ensure the realizability is to make ${C}_{\mu}$ in (16) variable [12].
where ${P}_{k}$ is the production term of turbulent kinetic energy due to the mean velocity gradients, ${P}_{b}$ the production of turbulent kinetic energy due to buoyancy, ${Y}_{M}$ the dilatation dissipation term that accounts for the contribution of the fluctuating dilatation in compressible turbulence to the overall dissipation rate, ${S}_{k}$ and ${S}_{\epsilon}$ user defined source terms for turbulent kinetic energy and dissipation, and ${\sigma}_{k}$ and ${\sigma}_{\epsilon}$ the turbulent Prandtl numbers for k and ε, respectively. ${C}_{1\epsilon}$, ${C}_{2\epsilon}$ and ${C}_{3\epsilon}$ are model constants.
Another weakness of traditional KEpsilon turbulence models is their modeling of the dissipation rate ε. Indeed, the wellknown spreading (or dispersion) rate anomaly refers to the fact that traditional models do reasonably well in predicting the spreading rate of a planar jet but perform unexpectedly poor for rounds jets. This weakness can be traced back to a deficiency in traditional εequations. The realizable model proposed by Shih [11] was developed to repair this deficiency and addresses as such an issue that is of primary importance in our study.
3.3.3 Combustion model
where ${J}_{\ell}$ is the mass diffusion flux of species ℓ. The previous equation is solved in a CFD code for $N1$ species where N is the total number of fluid phase chemical species present in the system. Since the mass fraction of the species must sum to unity, the N th mass fraction is determined as one minus the sum of the $N1$ solved mass fractions. To minimize numerical error, the N th species should be selected as that species with the overall largest mass fraction.
where ${\mathit{Sc}}_{t}$ is the turbulent Schmidt number and ${D}_{\ell}$ is the molecular diffusivity of species ℓ.
The species chemical reaction rate unclosed term ${\dot{\omega}}_{\ell}$ must be modeled with a combustion model. A combustion model describes the twoway interaction between properties of the turbulent flow produced by the flame and the chemical reactions. It serves to compute the reaction state space and the quantities it influences, namely the fluid density, viscosity, and temperature. It accounts for the processes that occur at length and time scales that we cannot resolve on a grid either in space or time due to limitations in computational resources. The choice of combustion model is decided by knowing the Damkohler number, defined as $\mathit{Da}=\frac{{t}_{\mathrm{mix}}}{{t}_{\mathrm{rxn}}}$, where ${t}_{\mathrm{mix}}$ is the mixing time scale and ${t}_{\mathrm{rxn}}$ is the reaction time scale. When the Damkohler number is very large, as in the case of the kiln, the reaction rate is controlled by the turbulent mixing that brings reactants together at the molecular scale. In this limit, the Standard Eddy Break Up (EBU) [13] model is fairly accurate because it assumes that the reaction occurs instantaneously upon micromixing.
The EBU combustion model tracks individual mean species concentrations on the grid through transport equations. The reaction rates used in these equations are calculated as functions of the mean species concentrations, turbulence characteristics and, depending on the specific model used, temperature. A mean enthalpy equation is solved in addition to the species transport equations. The mean temperature, density and viscosity are then calculated knowing the mean enthalpy and species concentrations. In the EBU used, the individual species in the global reaction are assumed to be transported at different rates according to their own governing equations.
where ${s}_{O}=\frac{{v}_{O}{M}_{O}}{{v}_{F}{M}_{F}}$, ${s}_{Pj}=\frac{{v}_{Pj}{M}_{Pj}}{{v}_{F}{M}_{F}}$, v is the molar stoichiometric coefficient for species j in reaction ℓ, M is molecular weight of species. Equation (30) essentially states that the integrated micromixing rate is proportional to the mean (macroscopic) concentration of the limiting reactant divided by the time scale of the large eddies ($\frac{k}{\epsilon}={\tau}_{\mathrm{mix}}$). ${\overline{Y}}_{F}$, ${\overline{Y}}_{O}$, ${\overline{Y}}_{P}$ are respectively the mean concentrations of fuel, oxidizer, and products. ${A}_{\mathrm{ebu}}$ and ${B}_{\mathrm{ebu}}$ are model constants with typical values of 0.5 and 4.0 respectively. The values of these constants are fitted according to experimental results and they are suitable for most cases of general interest.
In our simulations we used a reduced combustion mechanism with 6 species and 4 reactions to account for a fuel that is a mixture of different alkanes. This mixture consists for 95% of CH_{4} and for 5% of C_{2}H_{6}, C_{3}H_{8} and C_{4}H_{10}.
The above models are discretized by a finite volume technique using second order upwinding for the convective terms [14–16]. The flow equations are solved in a segregated approach in which the SIMPLE algorithm realizes the velocitypressure coupling. The energy equation is solved for the chemical thermal enthalpy using again a segregated approach. The temperature is computed from the enthalpy according to the equation of state. At each outer nonlinear iteration the resulting linear systems are solved using an algebraic multigrid preconditioner for a suitable Krylov subspace acceleration [17].
3.4 Additional information
In situations in which the media separating hot walls is transparent for thermal radiation as in the case of dry air, radiation can only occur as a surface phenomenon. In the our case however, the gas in the freeboard of the kiln will absorb, emit and scatter the thermal radiation intensity emitted from the hot walls of the kiln. This process is governed by the radiative transfer equation (RTE) that is implemented in a Participating Media Radiation Model. The model is discretized in solid angle by the discrete ordinate method described in detail in [18, 19].
3.5 Software implementation
Simulations were performed using the STARCCM+ software suite [20] on a tennodes Linux cluster having Intel Duo and Quad Core processors at a clock speed between 2.20 GHz and 3.16 GHz running a Slackware 13 64bit distribution. Iterating the threedimensional combustion model to equilibrium state required between $3\text{,}500$ and $4\text{,}000$ nonlinear iterations and between three and three and a half days of computation time.
4 Computational results
Standard and new configuration of operating conditions of the kiln
Operating conditions  Air to fuel ratio 

Standard  9 
New  12 
The objective of this section is to show how according to the combustion model described in the previous section the new configuration is less prone to the development of rings than the standard configuration. The two key arguments in this demonstration are the temperature and radiative heat distribution on the inside wall of the kiln. These will be elaborated separately in the two subsections.
4.1 Effect on temperature
Figure 6 clearly illustrates the effect of switching to the new operating conditions as it shows in the new conditions, the relatively cold preheated air is transported further into the kiln acting as a coolant on the wall. Figure 7 shows that this coolant reduces the wall peak temperature drops by 3.5% from $1\text{,}964$ degrees Celcius to $1\text{,}894$ degrees Celcius. It also shows that switching to the new operating conditions does not significantly alter the global distribution characteristics of the temperature which is of paramount importance in the material production process. Figure 8 is particularly interesting as it shows that in both configurations the peak in temperature is situated in a zone at four and halve to seven meters from the burner. This zone coincides with the zone in which rings are typically formed. It is therefore plausible that a reduction in peak temperature by switching to the new operating conditions will result in a reduction of the amount of liquid phase of the material being formed, and therefore impede the formation of rings. This hypothesis will be confirmed by looking into the computed radiative heat transfer distribution as we will do in the next subsection.
4.2 Effect on radiative heat transfer
Figure 9 confirms that as expected changing to the new operating conditions results in a lowering of the peak in radiative heat transfer. Figure 10 shows that peak in the radiative heat transfer drops by 13.5% from $5\text{,}718\text{,}029$ W/m^{2} to $5\text{,}062\text{,}986$ W/m^{2} and that the region of high values is reduced in size. Figure 11 gives another representation of this fact. By switching to the new operating conditions, the material in the kiln is less likely to absorb an excessive amount of heat, effectively limiting the amount of liquid phase of the material and therefore the formation of rings.
5 Experimental validation at the plant
6 Conclusions
We developed a numerical model allowing to access the effectiveness of measures implemented to counteract the formation of rings in a rotary cement kiln in use by Almatis B.V. in Rotterdam. In this threedimensional combustion model, the gas flow, the temperature profile, radiative heat distribution and the concentration of hydrocarbon species in the kiln is taken into account. Simulations show that deluting the airfuel mixture with air reduces peaks in radiative heat transfer in zones critical to ring formation. This reduction results in turn in less heat being absorbed by the granular material bed, effectively reducing the amount of material liquid phase prone to sticking to the kiln’s surface and to forming rings. The validity of our model has been experimental observed at the Almatis plant in Rotterdam. Since August 28th, 2011, the kiln has been operation without unscheduled shutdowns, resulting in hugely important cost savings.
Declarations
Acknowledgements
We thank Marco Talice for his advice worth more than platina and the CDADAPCO London office for the support in using their software.
Authors’ Affiliations
References
 Boateng AA: Rotary Kilns: Transport Phenomena and Transport Processes. ButterworthHeinemann, Stoneham; 2006.Google Scholar
 Mastorakos E, Massias A, Tsakiroglou CD, Goussis DA, Burganos VN, Payatakes AC: CFD predictions for cement kilns including flame modelling, heat transfer and clinker chemistry. Appl Math Model 1999,23(1):55–76. 10.1016/S0307904X(98)100537MATHView ArticleGoogle Scholar
 Marias F, Roustan H, Pichat A: Modelling of a rotary kiln for the pyrolysis of aluminium waste. Chem Eng Sci 2005,60(16):4609–4622. 10.1016/j.ces.2005.03.025View ArticleGoogle Scholar
 Giannopoulos D, Kolaitis DI, Togkalidou A, Skevis G, Founti MA: Quantification of emissions from the coincineration of cutting oil emulsions in cement plants: part i: NO_{ x }, CO and VOC. Fuel 2007,86(7–8):1144–1152. 10.1016/j.fuel.2006.10.025View ArticleGoogle Scholar
 Tran HN, Barham D: An overview of ring formation in lime kilns. Tappi J 1991,74(1):131–136.Google Scholar
 Peric M: Flow simulation using control volumes of arbitrary polyhedral shape. ERCOFTAC Bulletin September 2004, 62. Peric M: Flow simulation using control volumes of arbitrary polyhedral shape. ERCOFTAC Bulletin September 2004, 62.Google Scholar
 Williams FA: Combustion Theory. 2nd edition. Westview Press, New York; 1994.Google Scholar
 Kuo KK: Principles of Combustion. 2nd edition. WileyInterscience, New York; 2005.Google Scholar
 Poinsot T, Veynante D: Theoretical and Numerical Combustion. 2nd edition. Edwards, Ann Arbor; 2005.Google Scholar
 Hinze JO: Turbulence. McGrawHill, New York; 1975.Google Scholar
 Shih TH, Liou WW, Shabbir A, Zhu J: A new k  ϵ Eddyviscosity model for high Reynolds number turbulent flows  model development and validation. Comput Fluids 1995,24(3):227–238. 10.1016/00457930(94)00032TMATHView ArticleGoogle Scholar
 Reynolds WC Lecture Notes for Von Karman Institute. Fundamentals of Turbulence for Turbulence Modeling and Simulation 1987. Agard Report No. 755. Agard Report No. 755.Google Scholar
 Magnussen BF, Mjertager BH: On mathematical modeling of turbulent combustion. In 16th Symp. (Int.) on Combustion. The Combustion Institute, Pittsburgh; 1976:719–727.Google Scholar
 Demirdzic I, Peric M: Finite volume method for prediction of fluid flow in arbitrarily shaped domains with moving boundaries. Int J Numer Methods Fluids 1990,10(7):771–790. 10.1002/fld.1650100705MATHView ArticleGoogle Scholar
 Mathur SR, Murthy JY: A pressurebased method for ustructured meshes. Numer Heat Transf, Part B, Fundam 1997,31(2):195–215. 10.1080/10407799708915105View ArticleGoogle Scholar
 Murthy JY, Mathur SR: Radiative heat transfer in axisymmetric geometries using an unstructured finitevolume method. Numer Heat Transf, Part B, Fundam 1998,33(4):397–416. 10.1080/10407799808915040View ArticleGoogle Scholar
 Trottenberg U, Oosterlee C, Schüller A: Multigrid. Academic Press, San Diego; 2001.MATHGoogle Scholar
 Modest MF: Radiative Heat Transfer. McGrawHill, New York; 1993.Google Scholar
 Siegel R, Howell JR: Thermal Radiation Heat Transfer. 3rd edition. Hemisphere, Washington; 1992.Google Scholar
 StarCCM+ Version 6.06.011 user guide; 2011. StarCCM+Version 6.06.011 user guide; 2011.Google Scholar
Copyright
This article is published under license to BioMed Central Ltd. This is an Open Access article distributed under the terms of the Creative Commons Attribution License (http://creativecommons.org/licenses/by/2.0), which permits unrestricted use, distribution, and reproduction in any medium, provided the original work is properly cited.