Source rate and effective exchange coefficient for each

## Abstract

This chapter presents an investigation of the effectiveness of water cooling a battery module using a heat-sink prototype in the form of a thin copper helix tube within an aluminium block. A thermal model for the module containing six single cells is developed and numerically solved by coupling the heat energy transport equation with the fluid governing equations. The rate of generation of heat from the cells is calculated using a 2D model of a single cell with the resulting heat flux used as a Neumann boundary condition for the energy equation within a computational fluid dynamics code. Particular attention is given to the battery module operating in extreme ambient temperature conditions. The cooling strategy used is shown to satisfy two of the main concerns when managing the thermal performance of a battery module, that is, a suitable operating temperature range is maintained, and there is reasonable uniformity of temperature across the battery module. This should increase the battery cell life cycle together with enhancement of the charge and discharge performances. Variation of parameters such as the velocity of water within the tube and the number of turns used for the helix were investigated.

### Keywords

- Li-ion battery
- convective heat transfer
- clean energy

## 1. Introduction

Due to their outstanding properties regarding high energy density, power density, high service life, low self-discharge and rare pollution, the use of lithium ion batteries for battery electric vehicles (BEVs) and hybrid electric vehicles (HEVs) shows excellent promise [1]. Battery charging and discharging are strongly coupled to the operating temperature with a higher temperature increasing the number of undesired reactions, that is, the decomposition of the electrolyte, thickening of the solid electrolyte interface (SEI) film, and so on, which have the effect of degrading the battery capacity [2, 3, 4]. Lithium-ion battery cells are also highly sensitive to low temperatures. For example, at below −10°C, it has been shown that batteries’ performance deteriorates considerably [5, 6]. Safety is also an issue in that at high temperatures, lithium-ion batteries are prone to uncontrollable temperature build-up (thermal runaway) [7]. In addition, a battery pack is usually composed of up to hundreds of single cells connected in series and/or in parallel to produce output voltage and power/energy capacity to achieve the BEVs’ or HEVs’ operating needs. This contributes to the accumulation of heat and uneven temperature distributions across the battery pack so degrading performance. To counteract these serious problems, it is necessary to cool a battery pack effectively and uniformly.

Important to the development of a realistic thermal model of a battery module is good knowledge of heat generation either from the battery module as a whole or from individual cells within the module. The battery heat generation rate can be estimated by direct measurement [8], by indirect measurement, for example by measuring equilibrium voltage [9], measuring internal electrical resistance [10] or using the electrochemical mechanism [11, 12]. For direct measurement, the results apply to only a few operating points, and for indirect measurements, accuracy is a problem as the heat generation rate is a nonlinear function of the state of charge (SOC), current and operating temperature [13]. Work on single cell thermal-electrochemical modelling has already been done [13, 14, 15, 16], and it is the view here that an essential component for the modelling of battery modules and eventually battery packs is to start with accurate calculations of heat generation within a given single cell.

There are a number of ways of cooling battery modules with the major division being between air cooling and liquid cooling. There are advantages and disadvantages associated with each choice. For liquid cooling systems, a disadvantage is that they have the potential to leak, which could cause an electrical short. Also when liquid is used, maintenance and repair can be more costly and more complicated, and generally liquid cooled systems are more heavy and require more components. However, a design can be used, as in the present application where the battery module and liquid can be separated by aluminium. Air cooling systems are generally less effective at maintaining a uniform temperature within and between cells in a battery module, and they cannot carry as much heat away from the battery as quickly as a liquid-based system. Air convection (natural or forced) quite often is insufficient for effective heat dissipation from batteries under abuse conditions leading often to nonuniform temperature distributions within battery packs [17, 18]. Although air cooling systems are lighter, have a lower cost and generally a longer life, water cooling is favoured for this work due to its much superior cooling effect. There are many investigations of cooling systems reported in the literature with the majority of the work focusing on lumped parameter models [19]. The effectiveness of passive air cooling using phase change materials (PCMs) combined with forced cooling has been investigated [17], as has different single cell spacing arrangements [11, 20, 21]. It has been stated and demonstrated in the literature that indirect liquid cooling of battery packs (both passive and active) can prove an efficient method for dissipation or addition of heat [22, 23, 24, 25].

This chapter presents an investigation of the thermal performance of indirect water cooling, using the proposed design prototype of a thin copper helix tube contained within an aluminium block, for a lithium ion battery module. A thermal model is developed for the battery module where electrochemical equations are solved to provide boundary conditions for a computational fluid dynamics code in which the energy and fluid flow conservation equations are solved. Variation of parameters such as the velocity of water within the tube and the number of turns used for the helix were investigated.

## 2. Mathematical model

### 2.1. Modelling within a single cell

The mathematical model for a single lithium-ion battery developed here is based on the work of Doyle et al. [26]. The battery cells used are cylindrical with a central mandrel, with thin layers of anode, cathode, current collector and separator rolling up on the mandrel and with protection provided by a battery can. The anode is made of graphite derivatives and the cathode material is a metallic oxide such as LiFePO_{4} and LiM_{2}O_{4}. A schematic of a lithium ion cell is shown in Figure 1.

Generally, a lithium ion battery consists of the current collector, the positive electrode, the separator and the negative electrode. A lithiated organic solution fills the porous components and serves as the electrolyte. Several assumptions are needed, that is, the active electrode material is composed of spherical particles with uniform radius and the winding zone of the battery is a lumped model with homogeneous electrochemical properties. The material balance for the Li ions in an active solid material particle is governed by Fick’s second law, here expressed in spherical coordinates

where

where

where

At the interfaces between the positive electrode/separator and separator/negative electrode, the concentration of the binary electrolyte and its flux is continuous

The effective diffusion coefficient,

The charge balance in the solid phase is governed by Ohm’s law

where

The boundary conditions are expressed as

The potential of the solid phase at the right end of the cell (Figure 1) is set to zero,

where

At the two ends of the cell, there is no charge flux in the liquid phase

In the abovementioned equations, the pore wall flux,

where

The open circuit voltage of the electrode materials

with the boundary conditions determined by Newton’s cooling law

where

### 2.2. Modelling within the aluminium block

The battery module cooling system used here is a heat sink approach, where the lithium-ion battery cells are placed in an aluminium block and also surrounded by a copper helix coil through which water is pumped. The method employed is fundamentally to surround the cells with a conducting material, that is, a form of heat sink, and to remove or add heat using fluid. The cooling design is shown in Figure 2. The model solves in 3D, with fluid pumped through a central vertical tube and returned through the copper helix tube just within the aluminium block for efficient heat transfer and protection against damage.

The fluid is conditioned using a heater/refrigerator unit placed on the top surface of the plenum chamber as shown in Figure 3. The aim of the overall thermal management system is to maintain a battery module at an optimum average temperature, as dictated by life and performance trade-off. Important is that an even temperature, perhaps with small variations, is maintained between the cells and within the module. However, when designing such a system, regard must also be paid to the fact that the battery module should be compact, lightweight, have low cost manufacture and maintenance, and have easy access for maintenance. The management system should also have low parasitic power, allow the module to operate under a wide range of climatic conditions and provide ventilation if the battery generates potentially hazardous gases.

The calculation domain has two subdomains, that is, a fluid region and a solid region.

#### 2.2.1. Fluid section

For non-steady flow, the equations of continuity, momentum and energy can be expressed in the general conservation form

where * k*-

Equation | |||

Continuity | 1 | 0 | 0 |

Momentum | |||

Enthalpy | h | ||

Kinetic energy of turbulence | k | ||

Eddy dissipation rate |

In Table 1,

where

In addition to the standard * k*-

*-*k

*-*k

where

where

is the dimensionless velocity, and

is the dimensionless distance from the wall and

where

where

The standard wall functions tend to become less reliable when the flow situations depart from the ideal conditions and are subjected to severe pressure gradients and strong non-equilibrium. The non-equilibrium wall functions are introduced and can potentially improve the results in the above mentioned situations [34]. The law-of-the wall for mean temperature remains the same as in the standard wall functions already described and the log-law for mean velocity sensitised to the pressure gradient is

where

and

where

In this study, the Boussinesq model was used to treat the variable water density in which the water density is taken as a constant in all terms of the solved equations, except for the buoyancy term in the momentum equation

where ^{3});

#### 2.2.2. Solid section

The solid section in this work consists of three components, namely, the aluminium block, the wall of the helix coil and the battery module. When the velocity is set to zero in Eq. (20), the equation governing pure conductive heat transfer by diffusion is obtained, that is,

Conjugate heat transfer was used between the solid domain and fluid domain.

### 2.3. Boundary conditions and settings

The cooling fluid is modelled using the material properties of water calculated using the inlet temperature. The settings and boundary conditions are set out in Tables 2 and 3.

Battery module outside dimensions Cooling pipe radius ( Coolant Final mesh size | Radius = 130 mm, height = 360 mm 5–15 mm H _{2}O10 ^{7} |

Cylinder outer wall Coolant/solid interface Cooling pipe inlet Cooling pipe outlet Cell initial temperatures | 293.15 K Conjugate heat transfer 101,325 Pa |

### 2.4. Grid dependence and computer storage

The requirements set out in two recent guidelines referring to good CFD practice [35, 36] were followed in the present work. Non-uniform structured Cartesian grids were used throughout this work with extensive tests for independence of grid size checked by increasing the grid numbers until further refinement was shown not to be of significance. Close to solid surfaces, the grid was refined using geometric progression with an expansion ratio from the solid surfaces of less than 1.1 and with the ^{7}. The overall change in the residual for each variable between the last two numbers of elements was less than 0.1%, indicating grid independence had been achieved. The calculations were performed on a Dell T5500 workstation with 32 nm six-core Intel Xeon 5600 series processor and main memory of 24 GB. A typical CPU time for a transient run with a grid having 10^{6} nodes was just over 24 h.

## 3. Results

### 3.1. Heat generation within a single cell

The thermal characteristics of a Li-ion battery cell are first investigated using Eqs. (1)–(19), which form thermal-electrochemical coupled model. The cell used in these calculations has an electrolyte consisting of zinc and lithium salts dissolved in water. When the battery is fully charged, the anode consists of nonporous zinc and the cathode of porous Mn_{2}O_{4}. It is important to note that some of the electrochemical calculations are strongly dependent on coefficients, which are in turn strongly dependent of experimental results. For example, for the electrolyte just described, the specific conductivity Eq. (11) of the electrolyte is a function of temperature and the concentration of the electrolyte in the liquid phase, and so the ionic conductivity,

The effect of using different current rates during discharge of the battery cell is illustrated in Figure 5. Here temperature on the cell surface is calculated against the depth of discharge (DOD), which indicates the state of discharge of the battery cell starting at 100% fully charged. In these calculations, DOD was calculated as ^{−2} K^{−1}. As would be expected, the cell surface gets hotter as the discharge current rate increases. There is a ‘kink’ in the curve at lower current rates, which is thought to be due to an interaction between the ohmic and reversible heat in the energy balance equation.

Also calculated were the profiles of cell surface temperatures over a long time of discharge. Two limiting cases, that is, adiabatic and isothermal were used as the boundaries for this study with different heat transfer coefficients used for the intervening calculations, as shown in Figure 6. It can be seen that the heat transfer coefficient 1.0 W^{−2} K^{−1} gives a reasonable result and keeps the battery cell well within the desired operating range, while the 0.1 W^{−2} K^{−1} setting allows the battery cell wall temperature to reach the upper region of the desired range.

### 3.2. Cooling the battery module

In this part of the study, the temperature history of the battery module was modelled with ambient conditions (

Several tests were conducted, where the battery module was cooled to find appropriate values for the parameters,

It is important to know the optimum number of turns the helix coil makes for a number of reasons. One is that if too many coils are used, then more expense occurs in the manufacturing stage and also the integrity of the structure may suffer. If the number of coils is too small, then cooling of the battery to its ideal operating temperature range may become unacceptable. As can be seen from Figure 9, there is a big advantage to the cooling system when increasing the number of turns for 5 to say 15, but after that, the cooling effect of increasing the number of turns is greatly diminished. Increasing the number of turns is equal to lengthening the heat transfer path. According to Figure 9, as the number of turns increases, the amount of the heat transfer coefficient decreases significantly and after, say, 15 turns, it remains almost constant. The Prandtl number for water is larger than the one which would make the thermal entrance greater than the hydraulic entrance length. This means that after about 15 turns the thermal entrance length has been passed. An optimum number of turns appear to be around 10. The rest of this study continues with the number of helix turns in the aluminium block to be 10.

It is important for the lengthening of battery cell life and the enhancement of charging and discharging performance that uniformity of temperature is achieved throughout each cell, in addition to uniformity of cell temperatures across the cells within the battery module. To confirm that uniformity of temperature could be achieved across a single cell lodged within the battery module, temperature profiles were calculated in the radial direction through the battery module. As can be seen from Figure 10, where the radius at 0 is the battery module centre and radius at 130 mm is the outer wall of the module, the temperature profiles gradually move from an initial profile distorted by the hot cell to an acceptable final uniform distribution after about 15 s.

Another series of tests were conducted on the battery module which had, in addition to initial temperatures of 313.15 and 349.15 K, an internal heat source for each cell of either 0.25, 0.5 or 1 W. Results for the module with each of the cells having internal heat sources of 1 W are shown in Figures 11 and 12. As with the previous tests, what was important was the control of temperature between acceptable limits and a good uniformity of temperature across each cell.

It can be seen from Figures 11 and 12 that in the early stages of cooling, non-uniformity was found, but after, say, 1 min, uniformity was acceptable throughout each cell, and after 2 min, each cell was within the desired operating temperature limits (Note: each sub-figure has its own temperature scale). At times greater than 2 min, the heat loss to the atmosphere was slightly higher than heat production within the cells, even at 1 W, so reducing the need for further cooling. In the propose prototype, the temperature would be monitored using a thermostat, and further cooling would ensue intermittently as necessary.

## 4. Conclusion(s)

Preliminary results useful to the final design of a prototype battery module have been produced. The values found for the important parameters help in confirming the chosen geometry, and give indications of necessary pump and heating/refrigeration specifications needed when assembling the prototype. The calculations were made first inside a given battery cell to indicate what sort of temperature differences may be expected. It was found that these calculations depended heavily on experimental work to find appropriate coefficients for the coupled equations. After getting the range of temperatures arising from single battery cell calculations, a method was developed to find the temperature characteristics of the battery module, with stress being put on uniformity of temperature both within an individual cell and across the complete battery module.

## Nomenclature

a | specific surface area, m−2 |

c | electrolyte concentration in the solution phase, mol−3 |

cs | Li concentration in electrode particles, mol m−3 |

C1,C2 | k -ε turbulence model constants |

Cp | specific heat |

Cμ | turbulence model coefficient |

Deff | effective diffusion coefficient of Li in the electrode |

Ds | diffusion coefficient of Li in electrode particles, m2 s−1 |

E | potential |

F | Faraday’s constant |

h | heat transfer coefficient |

I | current |

J | surface reaction flux, mol m−2 s−1 |

Ji | pore wall flux |

k | turbulence kinetic energy |

kp | turbulence kinetic energy at near wall node |

kT | lumped thermal conductivity of cell |

Ln | anode thickness, m |

Lp | cathode thickness, m |

Ls | separator thickness |

Pr | Prandtl number |

qw | wall heat flux |

Q˙rea | heat generation due to electrochemical reaction |

Q˙rev | reversible heat |

Q˙ohm | ohmic heat |

r | radius/radial |

R | universal gas constant |

t | time |

t+0 | transference number |

T | temperature |

T∞ | ambient temperature |

T0 | reference temperature |

Tw | wall temperature |

U | mean velocity |

Ui | open circuit voltage |

xi | spatial coordinates |

yv | viscous sublayer thickness |

y+ | dimensionless velocity |

β | constant, Boussinesq model |

ε | dissipation |

ε′ | volume fraction of electrolyte |

ηi | overpotential |

κ | von Karman constant |

λ | coefficient, Newton’s cooling law |

μ | absolute viscosity |

ρ | density |

ρ0 | reference density |

σeff | effective electric conductivity |

σk | constant in turbulence model |

σε | constant in turbulence model |

τw | wall shear stress |

ϕ | potential |

Γφ | effective exchange coefficient |

## References

- 1.
Aifantis KE, Hackney SA, Kumar RV. High Energy Density Lithium Batteries: Materials, Engineering, Applications. New York: Wiley; 2010 - 2.
Ramadass P, Haran B, White R, Popov BN. Capacity fade of Sony 18650 cells cycled at elevated temperatures: Part I. Cycling performance. Journal of Power Sources. 2002; 112 (2):606-613 - 3.
Ramadass P, Haran B, White R, Popov BN. Capacity fade of Sony 18650 cells cycled at elevated temperatures: Part II. Capacity fade analysis. Journal of Power Sources. 2002; 112 (2):614-620 - 4.
Pinson MB, Bazant MZ. Theory of SEI formation in rechargeable batteries: Capacity fade, accelerated aging and lifetime prediction. Journal of the Electrochemical Society. 2013; 160 :A243-A250 - 5.
Zhang SS, Xu K, Jow TR. The low temperature performance of Li-ion batteries. Journal of Power Sources. 2003; 115 (1):137-140 - 6.
Fan J. On the discharge capability and its limiting factors of commercial 18650 Li-ion cell at low temperatures. Journal of Power Sources. 2003; 117 :170-178 - 7.
Wang Q, Ping P, Zhao X, Chu G, Sun J, Chen C. Thermal runaway caused fire and explosion of lithium ion battery. Journal of Power Sources. 2012; 208 :210-224 - 8.
Fan L, Khodadadi JM, Pesaraan AA. Parametric study on thermal management of an air-cooled lithium battery module for plug-in hybrid electric vehicles. Journal of Power Sources. 2013; 247 (3):961-966 - 9.
Ling Z, Wang F, Fang X, Gao X, Zhang Z. A hybrid thermal management system for lithium ion batteries combining phase change materials with forced-air cooling. Applied Energy. 2015; 148 :403-409 - 10.
Mahamud R, Park C. Reciprocating air flow for Li-ion battery thermal management to improve temperature uniformity. Journal of Power Sources. 2011; 196 (13):5685-5696 - 11.
Yang N, Zhang X, Li G, Hua D. Assessment of the forced air-cooling performance for cylindrical lithium-ion battery packs: A comparative analysis between aligned and staggered cell arrangements. Applied Thermal Engineering. 2015; 80 :55-65 - 12.
Amiribavandpour P, Shen W, Mu D, Kapoor A. An improved theoretical electrochemical-thermal modelling of lithium-ion battery packs in electric vehicles. Journal of Power Sources. 2015; 284 :328-338 - 13.
Ye Y, Shi Y, Cai N, Lee J, He X. Electro-thermal modeling and experimental validation for lithium-ion battery. Journal of Power Sources. 2012; 199 :227-238 - 14.
Cai L, White RE. Mathematical modelling of lithium ion battery with thermal effects in COMSOL Inc multiphysics software. Journal of Power Sources. 2011; 196 :5985-5989 - 15.
Gu WB, Wang CY. Thermal-electrochemical modeling of battery systems. Journal of the Electrochemical Society. 2000; 147 (8):2910-2922 - 16.
Anwar S, Zou C, Manzie C. Distributed thermal-electrochemical modeling of a lithium-ion battery to study the effect of high charging rates. The International Federation of Automatic Control; 24-29 August, 2014; Cape Town, South Africa - 17.
Sabbah R, Kizilel R, Selman JR, Al-Hallaj S. Active (air-cooled) vs. passive (phase change material) thermal management of high power lithium-ion packs: Limitation of temperature rise and uniformity of temperature distribution. Journal of Power Sources. 2008; 182 (2):630-638 - 18.
Pesaran AA, Burch S, Keyser M. An approach for designing thermal management systems for electric and hybrid vehicle battery packs. Fourth Thermal Management Systems Conference and Exhibition; 24-27 May, 1999; London, UK - 19.
Klien R, Chaturvedi NA, Christensen J, Ahmed J, Findeisen R, Kojic A. Electrochemical model based observer design for a lithium-ion battery. IEEE Transactions on Control Systems Technology. 2013; 21 (2):289-301 - 20.
Karimi G, Li X. Thermal management of lithium-ion batteries for electric vehicles. International Journal of Energy Research. 2013; 37 :13-24 - 21.
Ismailov K, Adair D, Massalin Y, Bakenov Z. On using splitter plates and flow guide-vanes for battery module cooling. Heat and Mass Transfer. 2017; 53 (1):1-10 - 22.
Chen K, Li X. Accurate determination of battery discharge characteristics - a comparison between two battery temperature control methods. Journal of Power Sources. 2014; 247 (3):961-966 - 23.
Yeow K, Teng H, Thelliez M, Tan E. Thermal analysis of a Li-ion battery systems with indirect liquid cooling using finite element analysis approach. SAE International Journal of Alternative Power. 2012; 1 (1):65-78 - 24.
Tong W, Somasundaram K, Birgersson E, Mijumdar AS, Yap C. Numerical investigation of water cooling for a lithium-ion bipolar battery pack. International Journal of Thermal Science. 2015; 94 :259-269 - 25.
Pesaran AA. Battery thermal management in EVs and HEVs: Issues and solutions. Advanced Automotive Battery Conference; 6-8 Feb., 2001; Las Vegas, Nevada - 26.
Doyle M, Fuller TF, Newman J. Modeling of galvanostatic charge and discharge of the lithium/polymer/insertion cell. Journal of the Electrochemical Society. 1993; 140 :1526-1533 - 27.
Valoen LO, Reimers N. Transport properties of LiPF6 - based li-ion battery electrolytes. JES. 2005; 152 :A882-A891 - 28.
Adair D. Numerical calculations of aerial dispersion from elevated sources. Applied Mathematical Modelling. 1990; 14 :459-467 - 29.
Allegrini J, Dorer V, Carmeliet J. Buoyant flows in street canyons: Validation of CFD simulations with wind tunnel measurements. Building and Environment. 2014; 72 :63-74 - 30.
van Hooff T, Blocken B. Coupled urban wind flow and indoor natural ventilation modelling on a high-resolution grid: A case study for the Amsterdam arena stadium. Environment Modelling and Software. 2010; 25 (1):51-65 - 31.
Tao WQ. Numerical Heat Transfer. 2nd ed. Xi’an: Xi’an Jiaotong University Press; 2001 - 32.
Launder BE, Spalding DB. The numerical computational of turbulent flows. Computer Methods in Applied Mechanics and Engineering. 1974; 3 (2):269-289 - 33.
Jayatillaka C. The influence of Prandtl number and surface roughness on the resistance of the laminar sublayer to momentum and heat transfer. Progress in Heat and Mass Transfer. 1969; 1 :193-321 - 34.
Kim SE, Choudhury D. A near-wall treatment using wall functions sensitized to pressure gradient. In F.E.D. ASME, editors, Symp. on Separated and Complex Flows. 1995; 217 :249-256 - 35.
Tominaga Y, Mochida A, Yoshie R, Kataoka H, Nozu T, et al. All guidelines for practical applications of CFD to pedestrian wind environment around buildings. Journal of Wind Engineering and Industrial Aerodynamics. 2008; 96 :1749-1761 - 36.
Meroney R, Ohba R, Leitl B, Kondo H, Grawe D, Tominaga Y. Review of CFD guidelines for dispersion modeling. Fluids. 2016; 1 (14):1-16 - 37.
Patankar SV. Numerical Heat Transfer and Fluid Flow. New York: CRC Press; 1980